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Research ArticleEffect of End Friction on the Dynamic Compressive MechanicalBehavior of Concrete under Medium and Low Strain Rates
Liu Jin12 Chengshun Xu1 Yaqiang Han1 and Xiuli Du1
1Key Laboratory of Urban Security and Disaster Engineering Ministry of Education Beijing University of TechnologyBeijing 100124 China2Department of Civil Engineering Tsinghua University Beijing 100084 China
Correspondence should be addressed to Chengshun Xu xuchengshunbjuteducn
Received 8 September 2015 Revised 25 October 2015 Accepted 26 October 2015
Academic Editor Nerio Tullini
Copyright copy 2016 Liu Jin et al This is an open access article distributed under the Creative Commons Attribution License whichpermits unrestricted use distribution and reproduction in any medium provided the original work is properly cited
The objective of the study is to examine the quantitative influence of end friction on the dynamic mechanical behavior of concreteunder medium and low strain rates Considering the concrete heterogeneity a mesoscale mechanical model was established tostudy the confinement effect of end friction in which the concrete was assumed to be composed of aggregates mortar matrixand the interfacial transition zones between them The friction behavior was utilized to describe the interaction between theconcrete specimens and loading apparatus The dynamic axial compressive mechanical behavior of concrete subjected to differentmedium and low strain rates and friction coefficients was simulated Furthermore the confinement mechanism of end frictionon the compressive dynamic increase factor (DIF) of concrete was studied The simulation results indicate that with the increaseof end friction coefficient the uniaxial compressive strength of concrete first increases and then becomes stable the end frictionconfinement changes the local stress state and damage distribution of concrete and it thus contributes to the increase in compressivestrength of concrete the friction contribution factor presents a descending tendency with increasing the strain rate and decreasesobviously when the end friction coefficient increases
1 Introduction
Strain rate effects on the tensile and compressive strengthsof concrete-like materials play an important role in theconstruction of material constitutive models which in turnexert a great deal of influences on the numerical simulationsof concrete structures subjected to intense dynamic loadings[1]The dynamic increase factor [DIF] defined by the ratio ofthe dynamic strength to the quasistatic strength in uniaxialcompression and tension has been widely accepted as animportant parameter to measure the strain-rate effect on thestrength of concrete-like materials [2] A great number oftests have been carried out to find the dependence of DIF onstrain-rate by using various test methods for example drop-hammer techniques servo-hydraulic loading rigs Split Hop-kinson pressure bar [SHPB] and explosive devices [2ndash4]Theobtained test data demonstrates the strain rate sensitivity ofconcrete dynamic strengths and indicates that the tested DIF
increases with strain rate However the test data presentslarge discrepancy which may come from the followingsources (1) different testing techniques (2) specimen sizeeffect (3) materials differences for example concrete qualityaggregate grade curing andmoisture condition and age and(4) dynamic and boundary effects as well as specimen lateralinertial effect
Recentlymany efforts have been conducted to explore themechanism of apparent dynamic strength enhancement ofconcrete such as in the publications [1 2] It is widely agreednow that the DIF obtained from dynamic test is affected bylateral inertia confinement [4 5] The friction at the interfaceof concrete specimen and loading measurement in the testesmay also constrain the lateral deformation of the specimenand changes the internal stress status and thus it might affectthe test results as well The strain rate effect described by thetensile and compressive DIFs should purely reflect the strain-rate-dependence of material itself
Hindawi Publishing CorporationShock and VibrationVolume 2016 Article ID 6309073 20 pageshttpdxdoiorg10115520166309073
2 Shock and Vibration
As known the end friction cannot be completely avoidedwhen conducting dynamic compressive tests The quantita-tive influence of end friction confinement should be deductedin the compressive DIF and it has been an interesting topicTo discover the influence of end friction on the macroscopicmechanical behavior of concrete including the dynamicfailure patterns and the nominal stress-strain curves as well asthe compressive DIF of concrete subjected to dynamic load-ings numerous efforts have been conducted For instanceusing the numerical methods Li and Meng [2] discussed theend friction confinement effect and found that for specimenswith 119871119863 = 05 [119871 means length of specimen and 119863 meansthe diameter of the specimen] the influence of the frictioncoefficient 120583 on DIF is insignificant when 120583 is less than01 but becomes considerable when it is larger than 02 Intheir simulations the strain rate employed ranges from 27times 101 sminus1 to 39 times 102 sminus1 and the friction coefficient utilizedranges from 0 to 07 Mu et al [6] modeled the dynamicmechanical properties of concrete subjected to the strain rateranging from 44 times 101 sminus1 to 147 times 102 sminus1 They found thatthe compressive strain-rate effect of concrete-like materialsis a pseudo property and the main mechanisms that initiatelateral confinement include the material lateral inertia andthe interface friction between the loading apparatus and theloaded specimen In addition in the works of Kim et al [7]Li et al [40] and Hao et al [4] the interface friction betweenthe loading apparatus and the loaded specimen was alsosimulated and examined They concluded that the frictioneffect is another factor in the so-called strain-rate effectThesesimulation efforts contribute to the understandings aboutthe dynamic compressive strength enhancement of concreteHowever these efforts are all focused on high strain ratesand the effect of end friction on the failure of concrete undermedium and low strain rates is rarely involved
The objective of the present study is therefore to examinethe quantitative influence of the confinement due to end fric-tion on the mechanical behavior of concrete under mediumand low strain rates Experimental results show that concreteis a heterogeneous brittle material that fractures throughthe formation growth and coalescence of microcracks [8]Moreover the failure behavior of concrete is closely relatedto the meso-microstructure of concrete and the hetero-geneities should therefore be considered [9ndash13] In this workconcrete was assumed to be a composite material consistingof mortarmatrix coarse aggregates and interfacial transitionzone (ITZ) between the former two phases Including thesecomponents in both experimental and numerical investiga-tions is essential because the mechanical properties of thesematerials are distinct In the computational model the dam-aged plasticity model implemented in a strain-rate sensitiveframework was utilized for the description of the dynamicmechanical behavior of the mortar matrix and the ITZ andelastic model was employed to characterize the mechanicalproperties of the aggregateThe friction behavior was utilizedto describe the interaction between the concrete specimensand loading apparatus By using the material model togetherwith the commercial software ABAQUS the reliability ofthe present approach was verified through the comparison
with the available test data Subsequently the dynamic axialcompressive mechanical behavior of concrete subjected todifferent medium and low strain rates was simulated underdifferent friction coefficients Furthermore the confinementmechanism of end friction on the compressive dynamicincrease factor (DIF) of concrete was studied and discussed
The paper is decomposed as follows The next sectiondescribes the rate-dependent constitutive framework forconcrete Section 3 presents the mesoscale computationalmodel for the simulation of the end friction confinementeffect and illustrates the verification of the present approachIn Section 4 the quantitative influences of the end frictionconfinement on the failure patterns the nominal stress-straincurves and the compressive DIF of concrete are exploredAnd finally the concluding remarks are given in Section 5
2 The Constitutive Framework forConcrete Mesocomponents
21 Concrete Damaged Plasticity Model The behavior ofconcrete is complex due to an array ofmorphological featuresaswell as deformation and failuremechanisms inherent in theconcrete microstructure The complicating factors includeheterogeneous constitution randomphase distribution arbi-trary microcrack patterns and internal granular frictionThecomplexity of the meso- or microscopic processes rendersexplicit resolution of the influences on a highly challengingtask
As known plasticity continuum damage mechanicsfracture mechanics elastic-damage and combined plasticityand damage mechanics are the common theories that havebeen widely used for the description of concrete mechanicalbehavior However the plasticity theory failed to address thedegradation of the material stiffness due to microcrackingthe fracture mechanics method was hard to reflect the nucle-ation of numerousmicrocracks and the growth of themicroc-racks to macrocracks and the continuum damage mechanicswith elasticity also could not describe the irreversible defor-mations and the inelastic volumetric expansion in compres-sion [13] Since both the stiffness degradation behavior andirreversible plastic deformations are contributing to the non-linear behavior of concrete a reasonable constitutive modelshould characterize the two distinct mechanisms In recentyears many coupled plasticity-damage models were pro-posed to describe the mechanical behavior of concrete suchas the work in the references [13 15ndash18] Among these effortsthe concrete damaged plasticity model was first proposed byLubliner et al [15] for monotonic loading and it was devel-oped later by Lee and Fenves [16] to consider the dynamic andcyclic loadings The model is a continuum plasticity basedmodel for concrete and it assumes that themain failuremech-anisms of the concrete are cracking in tension and crushingin compression The model which has been included in theABAQUS package has been widely used for the description ofthe static and dynamic mechanical behaviors of concrete-like materials for example in the publications [11 12 19 20]A brief presentation of the damaged plasticity model fromABAQUS is presented below
Shock and Vibration 3
Crack closure
ft
fc
E0(1 minus dc)(1 minus dt)
E0(1 minus dc)
E0(1 minus dt)
120576
120590c
120590t
E0
E0
Figure 1 Unaxial loading path of concrete plasticity damagemodel
211 Isotropic Damage Model The stress-strain relation forthe general three-dimensional multiaxial condition is givenby the scalar damage elasticity equation
120590 = (1 minus 119889)119863el0 (120576 minus 120576
pl) (1)
in which119863el0is the initial elasticity matrix 119889means the dam-
age variable and 120576pl is the plastic strain tensor Tensile damageand compressive damage are characterized independently bytwo hardening parameters 120576pl
119905and 120576pl119888(subscripts ldquo119905rdquo and ldquo119888rdquo
stand for tension and compression resp) which are referredto as equivalent plastic strains in tension and compressionThe evolution equations of the hardening variables 120576pl
119905and
120576pl119888 are conveniently formulated by considering uniaxial
loading conditions first and then extended to multiaxial con-ditionsThemodel assumes that the uniaxial tensile and com-pressive responses of concrete are characterized by damagedplasticity as shown in Figure 1 It is assumed that the stress-strain response follows a linear elastic relationship under uni-axial tension until the value of the failure stress119891
119905 is reached
The failure stress corresponds to the onset of microcrackingin the concrete material Beyond the failure stress the for-mation of microcracks is often represented macroscopicallywith a softening stress-strain response which induces strainlocalization in the concrete structure The uniaxial stress-strain curves can be converted into stress versus plastic straincurves of the form as
120590119905= 120590119905(120576
pl119905 120576
pl119905 120579 119891119894) (2a)
120590119888= 120590119888(120576
pl119888 120576
pl119888 120579 119891119894) (2b)
where 120576pl119905and 120576
pl119888are the equivalent plastic strain rates 120579 is the
temperature and 119891119894(119894 = 1 2 ) are other predefined field
variablesAs shown in Figure 1 when the specimen is unloaded
from any point on the strain softening branch of the stress-strain curves the unloading response is weakened the elasticstiffness of the material appears to be degraded Herein
the degradation of the elastic stiffness is characterized by twodamage variables tensile damage factor 119889
119905and compressive
damage factor 119889119888 and the stress-strain relationships under
tension and compression are respectively
120590119905= (1 minus 119889
119905) 1198640(120576119905minus 120576
pl119905) (3a)
120590119888= (1 minus 119889
119888) 1198640(120576119888minus 120576
pl119888) (3b)
This representation although somewhat simplified cap-tures the main features of concrete behavior Sometimesin order to avoid unreasonable mesh sensitive results thetensile post-failure behavior is given in terms of a fractureenergy cracking criterion by specifying a stress-displacementcurve instead of a stress-strain curve Under multiaxialloading conditions the evolution equation of the hardeningparameters for uniaxial loading should be extended
According to Lee and Fenvesrsquos work [16] tensile and com-pressive equivalent plastic strains have the following forms
120576pl119905= 119903 () 120576
plmax (4a)
120576pl119888= minus (1 minus 119903 ()) 120576
plmin (4b)
in which 120576plmax and 120576
plmin are the maximum and minimum
plastic strain tensors respectively 119903() means a multiaxialstress weight factor and is defined as
119903 () =
sum3
119894=1⟨119894⟩
sum3
119894=1
10038161003816100381610038161003816119894
10038161003816100381610038161003816
0 le 119903 () le 1 (5)
in which 119894are principal stress components (119894 = 1 2 for 2D
problems and 119894 = 1 2 3 for 3D problems) and the Macauleybracket ldquo⟨sdot⟩rdquo is defined by ⟨119909⟩ = 05 times (|119909| + 119909)
212 Plasticity Yield Surface The model makes use of theyield function of Lubliner et al [15] with the modificationsproposed by Lee and Fenves [16] to account for differentevolution of strength under tension and compression Theevolution of the yield surface is controlled by the two harden-ing variables 120576pl
119905and 120576pl119888 In terms of effective stress the yield
function 119865 is defined as
119865 = 119865 (120590 120576pl)
=1
1 minus 120572[119902 minus 3120572119901 + 120573 (120576
pl) ⟨120590max⟩ minus 120574 ⟨minus120590max⟩]
minus 120590119888(120576
pl119888) = 0
(6)
in which 119901 = minus(13)120590 119868 is the effective hydrostatic pressurestress 119868 is a stress invariant 119902 = radic(32)119878 119878means theMisesequivalent effective stress and 119878 is the effective stress deviatordefined as 119878 = 119901119868 + 120590 120590max is the maximum principaleffective stress Typical yield surface is depicted in Figure 2 forplane stress conditions
4 Shock and Vibration
Uniaxial compression
Uniaxial tension
Biaxial tension
Biaxial compression 120590c
120590t
(120590cc 120590cc)
1205901
1205902
Figure 2 Yield surface for plane stress conditions
1205901
1205902
1205903
Kc = 1
Kc = 23
Figure 3 Yield surfaces in the deviatory plane [119870119888
= 23
corresponds to Rankine formulation and119870119888= 1 corresponds to the
Drucker-Prager criterion]
Moreover parameters of 120572 120573(120576pl) and 120574 respectively canbe calculated by
120572 =120590119888119888120590119888minus 1
2120590119888119888120590119888minus 1
(7a)
120573 (120576pl) =
120590119888(120576
pl119888)
120590119905(120576
pl119905)
(1 minus 120572) minus (1 + 120572) (7b)
120574 =3 (1 minus 119870
119888)
2119870119888minus 1
(7c)
in which 120590119888119888120590119888means the ratio of initial equivalent-biaxial
compressive yield stress to initial uniaxial compressive yieldstress and its default value of the ratio is 116 according to[19 20] 119870
119888is the ratio of the tensile to the compressive
meridian and defines the shape of the yield surface in thedeviatory plane (see Figure 3)
213 Plastic Flow Rule The nonassociated potential plasticflow is employed in the present damaged plasticity modelThe flow potential function 119866(120590) used for this model is
the nonassociatedDrucker-Prager hyperbolic function and isdefined according to
119866 (120590) = radic(120578120590119905tan120595)2 + 1199022 minus 119901 tan120595 (8)
in which 120595 is the dilation angle measured in the 119901-119902 planeat high confining pressure 120590
119905is the uniaxial tensile stress at
failure 120578 is the eccentricity that gives the rate at which theplastic potential function approximates the asymptote (theflow potential tends to a straight line as the eccentricity tendsto zero) and its default value is equal to 01Thenonassociatedflow rule means that the plastic strain vector is normal to theplastic potential function that differs from the yield surface
The plastic strain rate 120576pl and the effective plastic strain
rate 120576pl can be derived as follows
120576pl=
120597119866
120597120590(9a)
120576pl= ℎ (120590 120576
pl) sdot 120576
pl (9b)
where is the plastic multiplierBecause the selected plastic flow is nonassociated to
obtain an acceptable rate of convergence the unsymmetricmatrix storage and solution scheme is used For more detailsabout the constitutive model refer to Lubliner et al [15] Leeand Fenves [16] and Du et al [11]
22 Dynamic Increase Factor (DIF) for Concrete The avail-able experimental and numerical observations have demon-strated that concrete and other cementitiousmaterials are ratesensitive [3 21 22] The strain rate effect has been studiedon different mechanical characteristics of concrete Youngrsquosmodulus Poissonrsquos ratio energy-absorption capacity andaxial strain atmaximumstrength are rate-sensitive quantitiesbut at amuch lower intensity than the compressive and tensilestrengths [3 23] Similar to the work [4 11] only the strengthenhancement was considered in the present study
So far many empirical and theoretical relations have beendeveloped to quantitatively describe the strain rate effect onconcrete properties In particular the code by the ComiteEuro-international du Beton (CEB) recommends variousvalues of the DIF for the tensile and compressive strengthsunder different strain rates based on the available test resultsThe formula of the compressive DIF recommended by CEB[3] has the following form
CDIF =119891cd119891cs
= (120576119889
120576cs)
1026120572
for 120576119889le 30 sminus1 (10a)
CDIF =119891cd119891cs
= 120574 ( 120576119889)13 for 120576
119889gt 30 sminus1 (10b)
where 119891cd is the dynamic compressive strength at the strainrate of 120576
119889(in the range of 30 times 10minus6ndash1000 sminus1) 120576cs = 30 times
10minus6 sminus1 (static strain rate) log 120574 = 6156120572 minus 049 120572 = (5 +
3119891cu4)minus1 119891cs is the static compressive strength and 119891cu is
the static cube compressive strength [in MPa] The DIF for
Shock and Vibration 5
the compressive strength in (10a) and (10b) was oftenadopted for example in the publications [10 11]
The CEB also gives empirical formulae to estimate theDIF for concrete tensile strength However comparisonbetween the available experimental results in the literaturewith the CEB empirical equations indicates that the CEBtensile DIF substantially underestimates the tensile DIF ofconcrete [24 25] In Malvar and Rossrsquos [24] work an empiri-cal formula was proposed and the formula for the tensile DIFcan be written as
TDIF =119891td119891ts
= (120576119889
120576ts)
120575
for 120576119889le 1 sminus1 (11a)
TDIF =119891td119891ts
= 120573(120576119889
120576ts)
13
for 120576119889gt 1 sminus1 (11b)
where 119891td and 119891ts are respectively the dynamic uniaxial ten-sile strength at the strain rate 120576
119889and the quasistatic uniaxial
tensile strength 120576ts = 10minus6 sminus1 (static strain rate) log120573 = 6120575minus2
120575 = 1(1 + 81198911015840
1198881198911015840
1198880) 11989110158401198880= 10MPa and 119891
1015840
119888is the quasistatic
uniaxial compressive strength of concrete (in MPa)
3 Mesoscale ComputationalModel for Concrete
Theoretical experimental and numerical studies indicatethat the failure pattern crack mode and even the velocity ofthe crack propagation are influenced by loading rate [11 26ndash28] The mechanical behaviors of concrete including themacroscopic mechanical properties and the failure patternsare associated with the micro-mesostructure of concreteDue to the complexity of concrete the failure behavior can bestudied numerically In the numerical simulations concreteheterogeneity should be accounted for and thus it requiresthe adoption of a mesoscale mechanical model in which theheterogeneity can be explicitly described
At themesoscale concretewas often assumed to be amul-tiphase composite composed of aggregate mortar matrix theinterfacial transition zones [ITZs] voids and so forth A lot ofwork [9 10 19 29] has demonstrated that the ITZs have a dra-matic influence on the failure pattern and the macromechan-ical properties of concrete However the mechanical proper-ties especially the dynamic mechanical behavior of the ITZsare not well understood yet [13 19 30ndash32] Moreover thereal typical thickness of ITZ is about 10ndash50120583m [9 10] whichlimits the minimum size of the finite element mesh In mostsimulation efforts the ITZ thickness is set as 02ndash08mm[9 10] 05mm [8] 04mm [19] and 1mm [12] for the sake ofsimplicity
31 Mesostructure and Mechanical Model of Concrete Con-crete exhibits heterogeneity in material and mechanicalproperties onmany length scales [29] At the mesoscale con-sidering the effect of heterogeneities of concrete the concretein the present work was regarded as a three-phase compositecomposed of coarse aggregate particles mortar matrix andthe ITZs between the former two phases Random aggregatemodels have long been demonstrated to be an effective
mesomechanical approach to simulating the failure processand the deformation of concrete and they have been widelyutilized in fracturemechanics of concrete for example in [11ndash13 33] Based on the concrete random aggregate model inwhich the shape size and distribution of the coarse aggregateparticles closely resemble real concrete in the statistical senselots of efforts have been carried out to investigate the macro-scopic mechanical behavior and failure mechanism of con-crete [10ndash12 29] In this work the concrete random aggregatemodel was therefore also employed
Due to great computational expense and memorydemand of mesoscale simulations it is in general notpossible to model the full structure at the mesoscale with thecomputational power available nowadays Herein the presentstudy only two-dimensional simulations were thus con-ducted Similar to the work [9ndash12 33] the aggregate particlesare modeled as circles with random spatial distributionenfolded by a thin interface layer of ITZ Similar to those in[11 12] the ldquotake-and-placerdquo method was utilized to generatethe coarse aggregate particles The fine ones and othercomponents (eg air voids) were assumed to be mixed upwith the cement paste establishing the mortar matrix phaseThis matrix phase can thus be regarded as a homogeneouscomponent at the mesoscale The material properties of thepaste phase are thus strongly dependent on the type of cementused amount of pores water to cement ratio and otheradditives present in the concrete which can be determinedby microscale simulation efforts Furthermore the Fullercurve widely utilized for example in [11 12] was selected todetermine the distribution of aggregate with different sizesemployed in the concrete specimen The aggregate particleswere then placed into the matrix one by one at randomlydetermined positions and in such a way that no overlappingwith particles already placed Finally at the mesoscale aggre-gate particles (typically sand or gravel) and the surroundingITZ layers behave as inclusions in the matrix phase of mortarmatrix
Figure 4 presents a typical schematic diagram of concretemesostructure generated by employing the above approachThe size of the heterogeneous concrete specimen is 150mm times
150mm Note that aggregate particles in real concrete arenot perfectly circular However the efforts in [10 11] haveindicated that the effect of aggregate shape on macroscopicstress-strain curve of concrete seems to be very smallSimilar to that in [11 34] the concrete sample contains 6medium stones with a diameter of 30mm and 56 small stoneswith a diameter of 12mm The concrete specimens involveabout 469 of aggregate per volume In Figure 4 the greenareas mean the aggregate phase the red thin-layer zonessurrounding the aggregate particles are the ITZs and the greyzones denote the mortar matrix Herein the interfacial zonesare viewed as uniform thickness shells placed concentricallyaround each aggregate Similar to the work [34] the thicknessof the ITZ was set as 1mm
To describe the influence of end friction confinement onthe dynamic compressive mechanical properties of concretetwo rigid blocks (see the two blue blocks in Figure 4) wereplaced respectively at the top and the bottom of the con-crete specimen The interactions between the heterogeneous
6 Shock and Vibration
y
x
AggregateITZ
Mortar matrixRigid block
Uniaxial compression
Unit mm End
fric
tion
25 25150
2525
150
Figure 4 Mesoscale mechanical model of concrete under dynamic uniaxial compression considering the influence of end frictionconfinement The specimen has 22346 elements [For interpretation of the references to color in this figure legend the reader is referredto the web version of this paper]
concrete specimen and the two rigid blocks that is the twored-line regions are implemented by the classic coulombfriction behavior The friction coefficients considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces ofthe specimen were fixed in the horizontal direction) fora quantitative assessment of the end friction confinementeffect As known the DIF difference obtained from thesimulation results with different friction coefficients canthen be attributed purely to the influence of end frictionconfinement effects
Themeshing of these concrete specimens were conductedwith four node solid elements with a linear strain field Tohave a better understanding of concrete fracture the averagemesh size was l mm which is consistent with that in the workfrom Hentz et al [23] and Du et al [11 12]
32 Mechanical Parameters for the Three MesocomponentsIn Zhou and Haorsquos [11 13] and Snozzi et alrsquos [35] workthe uniaxial tensile and compressive mechanical behaviorof concrete at high strain rate were studied From theirsimulation observations it can be noticed that no damagegenerates in the aggregate phaseMoreover in Pedersen et alrsquos[8] simulation of the dynamic tensile behavior of concretethe aggregate grains were assumed to follow a linear elasticmaterial behaviorThis is because the tensile and compressivestrengths of the aggregate are much larger than those of mor-tar matrix and the ITZs Similar to the work [8 11] the aggre-gate was assumed as elastic in the following simulationsThistreatment should work for the concrete subjected to mediumand low strain rates as discussed in the present study
To the mortar matrix and the ITZs the continuumdamage mechanics theories mentioned previously wereemployed to describe their mechanical properties In contin-uum mechanics the constitutive model is often expressed in
terms of stress-strain relations When the material exhibitsstrain-softening behavior leading to the strain localizationbehavior this formulation leads to a strongmesh dependencyof the finite element results in which the energy dissipateddecreases upon mesh refinement [11 19] Similar to the workin [10 11 19] to avoid or release unreasonable mesh sensitiveresults the tensile postfailure behavior was given in terms ofa fracture energy cracking criterion by specifying a stress-displacement curve instead of a stress-strain curve In addi-tion unlike discrete crack models [36 37] the continuumdamaged plasticity model based on continuum mechanicsuses damage factors such asDAMAGEC for compression andDAMAGET for tension to describe the fracture behavior andit is not capable of providing accurate crack geometry such ascrack width
The main mechanical parameters including the elasticmodulus Poissonrsquos ratio and uniaxial tensilecompressivestrengths of the three mesoconstituents used in this study forthe following numerical analysis were listed in Table 1
It is to be noted that the DIFs given in Section 22 are builtbased on the test results on concrete material The strain rateeffects for the aggregate phase mortar matrix and the ITZare essentially distinct as illustrated in [38 39] NeverthelessGrote et alrsquos [21] experimental observations indicate that thedynamic mechanical behavior of mortar matrix is closelysimilar to that of concrete In addition the ITZ layer can betreated as a kind of mortar matrix with a high(er) porosity[34] and thus its dynamic mechanical behavior can also beregarded as similar to those of mortar matrix and concreteIn summary it is assumed that the ITZ and the mortarmatrix have the same DIFs mentioned previously The treat-ments are consistent with the ones in [9 10] The strainrate effect for both the mortar matrix and the ITZs ontheir tensilecompressive strengths was incorporated intothe plasticity damaged model which was represented by
Shock and Vibration 7
Table 1 Mechanical parameters of the concrete mesocomponentsused in the study
Mortar matrix ITZ AggregateMass density 120588 [kgm3] 275 times 103 275 times 103 288 times 103
Elastic modulus [GPa] 30lowast
25lowast
70lowast
Poissonrsquos ratio 02lowast
022lowast
016lowast
Dilation angle 120595 [∘] 30 30Eccentricity 120578 01 01Shape factor 119870
1198880667 0667
Stress ratio 120590119888119888120590119888
116 116Tensile yield stress 120590
119905[MPa] 143
lowast12lowast
Compressive yield stress 1205901198880
[MPa] 143lowast
12lowast
Ultimate compressive yieldstress 120590cu [MPa] 143 12
Note data with ldquolowastrdquo are quoted from Du et al [12]
a dynamic increase factor (ie the DIF) with respect to strainrate
33 BoundaryLoading Conditions and FE Simulations Toexamine the effects of end friction confinement on themacromechanical behavior of concrete subjected to dynamiccompressive loadings the failure behavior of the concretespecimen was explored The corresponding loading andboundary conditions for the interaction system were illus-trated as follows (1) constant vertical velocity V was appliedon the top surface of the rigid block and the left and rightsides of the specimen are free of stress (2) the movementat the bottom rigid block was fixed at both the vertical andhorizontal directions (3) friction behavior between the twoblocks and the concrete sample was set The nominal strainrate 120576 is defined as the applied velocity divided by the heightof the specimen that is 120576 = Vℎ where ℎ is the height of thespecimen
In the following simulations ABAQUS increased auto-matically the size of step time going from smaller one to themaximumauthorized defined by the user For all the concretespecimens the numerical simulations were performed in aplane strain condition
34 Verification of the Mesoscale Approach In reality theavailable tests on loading rate effect of concrete are not veryrich and the test data is also not complete Comparativelyspeaking Dilger et alrsquos [14] test data is the most completeone and it is often used to verify the reliability of the analysismethod or model such as in [26]
To illustrate the reliability and accuracy of the presentmesoscale simulation method Dilger et alrsquos [14] test on thedynamic uniaxial compressive behavior of concrete was alsoselected for the comparison in this section In Dilger et alrsquos[14] experiment the macroscopic mechanical behavior ofconcrete under different nominal strain rates (ie the strainrates of 333 times 10minus5 sminus1 333 times 10minus3 sminus1 and 02 sminus1) was
explored and the complete compressive stress-strain curvesof concrete were obtained
In the previouswork [33] a series of dynamic compressivetest of concrete under different strain rates were conductedbased on the present mesoscale mechanical method includ-ing 120576 = 333 times 10minus5 sminus1 1 times 10minus4 sminus1 333 times 10minus3 sminus1 1 times 10minus2 sminus15 times 10minus2 sminus1 02 sminus1 1 sminus1 100 sminus1 and 200 sminus1 It is to benoted that in the simulations the concrete specimens werefixed at one end and loaded longitudinally through an appliedconstant velocity at the other end The detailed mechanicalparameters and analysis method can refer to [33]
Figure 5 presents the failure patterns of the concretespecimen subjected to different nominal strain rates Onecan notice that with the increase of strain rate the numberof cracks (ie the red damaged region) increases obviouslyand the crack branching behavior occurs Therefore withthe increase of strain rate the fracture of concrete requiresmore energy demand to reach failure which should be themain reason for the improvement of the dynamic strength ofconcrete
Figure 6(a) reports the comparison between the sim-ulations results (solid curves) and the experimental data(symbols) in terms of nominal stress (applied forces dividedby the specimen cross sectional area) versus nominal strain(the displacement generated at the applied-load end dividedby the length of the specimen) curves and the agreementis very good It should be noted herein that as mentionedpreviously the relatedmechanical and physical parameters ofthe concrete mixture used in the test are not full especiallythe mechanical parameters of the ITZ Accordingly in thepreviouswork [33] themechanical parameters (especially theelasticmodulus and the strength) of the ITZwere determinedby the inversion method on the basis of only two strainrates (333 times 10minus5 sminus1 and 333 times 10minus3 sminus1) The simulationof the third available strain (ie 02 sminus1) can be regarded asa validation of the ability of the model to predict concretestrength outside the range of strain rates used for calibrationThis treatment is similar to that in [26]
Furthermore the compressive DIFs were evaluatedaccording to the simulation results and the comparison of thepresent simulation results and some available experimentalobservations is plotted in Figure 6(b) It can be observedthat the present simulation results agree very well with thecollective experimental data This indicates that the presentanalysis method can well simulate the dynamic compressivebehavior of concrete The validated mesoscale mechanicalapproach would be employed in the following simulations tostudy the effect of end friction confinement on the dynamiccompressive behavior of concrete
4 Dynamic Compressive FailureBehavior of Concrete
On the basis of the mesoscale mechanical model describedin Section 3 the simulations of the dynamic axial com-pression of the concrete specimen with various end fric-tion coefficients were implemented The loading velocitiesadopted on the upper rigid block in the simulations are
8 Shock and Vibration
10Damage
120576 = 333 times 10minus5 120576 = 1 times 10minus4 120576 = 333 times 10minus3 120576 = 1 times 10minus2 120576 = 5 times 10minus2
120576 = 2 times 10minus1 120576 = 1 120576 = 100 120576 = 200
Figure 5 Compressive failure patterns of the concrete specimen under different strain rates ranging from 1 times 10minus5 sminus1 to 200 sminus1
Compression test(Dilger et al 1984) and present model
Nom
inal
com
pres
sive
stre
ss (M
Pa)
0002 00030001 0004 0005 00060Compressive strain
0
10
20
30
40
120576 = 333 times 10minus5 sminus1
120576 = 333 times 10minus3 sminus1
120576 = 02 sminus1
(a)
001 1 100
09
12
15
18
21
24
Com
pres
sive D
IF
Test data Present method
1E minus 6 1E minus 4
Strain rate (sminus1)
(b)
Figure 6 (a) Comparison of the present simulation results and Dilger et alrsquos [14] test data and (b) compressive DIFs for the simulation resultsand some available test data
Shock and Vibration 9
Dynamic loading
0
2
4
6
8
10
12
14
Com
pres
sive
stre
ss (M
Pa)
120576 = 1 times 10minus1 sminus1
times10minus3
Mesh size 15mmMesh size 10mmMesh size 05mm
End friction coefficient 120583 = 06
1 432 5 6 70Strain 120576
(a)
Mesh size 15mmMesh size 10mmMesh size 05mm
Damage factor0 1
(b)
Figure 7 (a) The simulation results of three concrete specimens with the same distribution of aggregates and different mesh sizes and(b) damage distribution of the concrete specimens with different mesh sizes under the same strain rate and friction coefficients at theirpeak stresses
V = 15 times 10minus6ms 15 times 10minus4ms 15 times 10minus3ms 15 times
10minus25ms 15 times 10minus2ms 15 times 10minus15ms and 15 times 10minus1msin an ascending sequence and in every loading cycle the con-stant velocity was utilized The corresponding macroscopicnominal strain rates are 120576 = 1 times 10minus5 sminus1 (quasistatic) 1 times10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1and 1 times 100 sminus1 respectively Moreover as mentioned previ-ously the seven end friction coefficients 120583 considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces of thespecimenwere fixed in the horizontal direction) respectively
To check the mesh sensitivity in the simulations threedifferentmesh sizeswere utilized that is 05mm 10mm and
15mm Figure 7(a) presents the nominal compressive stress-strain curves of the concrete specimen subjected to a nominalstrain rate of 01 sminus1 with the same end friction coefficientand the three different mesh sizes It can be found clearlyfrom Figure 7(a) that the mesh sizes (ie 05mm 10mmand 15mm) have less influence on the stress-strain curvesThe three curves are also overlapped Figure 7(b) shows thedamage distribution of the three concrete specimens men-tioned above with the same distribution of aggregates Onecannotice that the failure patterns of the three specimenswithdifferent mesh sizes are closely similar to each other Conse-quently the mesh size of 15mm was used in the followingsimulations
10 Shock and Vibration
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
Equivalent plastic strain times10minus300 56
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
120576
120576
120576
120576
120576
Figure 8 Equivalent plastic strain distribution within the concrete specimen under different strain rates and end friction coefficients at theirpeak compressive stresses
41 Effects of Strain Rate and End Friction Confinement onFailure Patterns of Concrete Figure 8 presents the equivalentplastic strain distribution within the concrete specimensunder five groups of different strain rates ( 120576 = 1 times 10minus5 sminus11 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus1 sminus1 and 1 times 100 sminus1) and fourgroups of different friction coefficients (120583 = 0 03 08 andinfin) at their peak compressive stresses (ie the compressivestrength) One can note from Figures 8(a)ndash8(d) that for thespecimen with the same friction coefficient with the increase
of nominal strain rate the equivalent plastic strain withinconcrete increases obviously In addition as the frictioncoefficient 120583 increases from 0 to infin the equivalent plasticstrain within concrete at reaching the peak stress varies
For the specimenwith the friction coefficient of 0 and 03the obtained plastic strain distributions within the concretespecimens are obviously different For the one with the fric-tion coefficient of 03 and 08 the obtained plastic strain dis-tributions are slightly different And for that with the friction
Shock and Vibration 11
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
000 49
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Maximum principal stress (MPa)
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 9 Maximum principal stress distribution within the concrete specimen under different strain rates and end friction coefficients attheir peak compressive stresses
coefficient of 08 andinfin the obtained plastic strain distribu-tions are almost totally consistent That is to say when thefriction coefficient becomes larger than 08 the effect of endfriction confinement on the failure patterns of concrete canbe ignored
The maximum principal stress distributions within theconcrete specimens under the five groups of different strainrates and the four different friction coefficients at the peakcompressive stresses are presented in Figure 9 It can be
noted intuitively from Figure 9 that the changes of nominalstrain rate and friction coefficient have a significant influenceon the maximum principal stress distribution of the speci-menWith the increase of end friction coefficient the value ofmaximum principal stress gets large and the distribution areadraws close to central section from the top and bottom of theconcrete specimen respectively at same loading velocity
The damage (ie the cracks) distributions within theconcrete specimens corresponding to Figures 8 and 9 are
12 Shock and Vibration
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
0 1
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Damage factor
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 10 Damage distribution within the concrete specimens under different strain rates and friction coefficients at their peak stresses
presented in Figure 10 for different loading velocities anddifferent end friction coefficients In Figure 10 differentcolors represent different damage indexes The red colordenotes the most serious damage while the blue color meansthat no damage generates The white rounded areas whichare regarded as aggregates in these models have no damage
It can be noticed clearly from Figure 10 that the damagedareas increase with the growth of nominal strain rate Whenthe nominal strain rate is relatively low(er) (eg 1 times 10minus5 sminus1)the damaged area of the specimens is small when reaching
their peak stress Accordingly the damage regions (iecracks) are narrow and short and the number of cracks islimited As the nominal strain rate rises from 1times 10minus5 sminus1 to 1times100 sminus1 the damaged area and the number of cracks increasegradually When the nominal strain rate is relatively high(er)(eg 1 times 100 sminus1) a lot of areas are damaged in different levelsThe cracks widen and link together forming a crack networksimultaneously
Therefore it can be concluded that with the increase ofloading velocity the nominal strain rate increases gradually
Shock and Vibration 13
Table 2 Dynamic compressive strength of concrete under different end friction coefficients
120583Dynamic compressive strength [MPa]
1 times 10minus5 sminus1 1 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1 1 times 100 sminus1
0 793 806 858 919 1042 1197 153901 829 838 906 977 1113 1297 161202 846 857 926 1007 1137 1349 168203 849 864 939 1016 1167 1355 169606 857 877 955 1036 1175 1382 173608 860 881 962 1042 1185 1391 1745infin 875 892 980 1067 1212 1406 1749
and the number of cracks or damaged zones increases whenthe apparent compressive strength of concrete is reachedTheenergy consumption of the loading process increases corre-spondinglyThis should be the major reason for the improve-ment of dynamic compressive strength of concrete materials
It can be found obviously from the comparison amongFigures 10(a)ndash10(d) that the damage states of concrete spec-imens are diverse at their peak stresses for different endfriction conditions
Compared with the concrete specimen without end fric-tion confinement (ie 120583 = 0) the deformation at the end ofthe specimen considering the effect of end friction (ie120583 gt 0)was obviously hindered In addition with the increase of endfriction coefficient the obstruction degree of deformationraises For the specimen with the two ends completely fixed(ie 120583 = infin) there is no horizontal deformation at the endsmaking the confinement effect very strong
From Figure 10 one can note that a larger end frictioncoefficient leads to a lower damage level in the top and bottomof the specimen with a constant nominal strain rate Forlarger end friction coefficient the damaged areas draw closeto the central section from the top and bottom of the concretespecimenThese phenomena should generate due to the effectof the end friction confinement which changes the uniaxialloading state in the local regions of concrete These can alsobe illustrated from the simulation results in Figures 8 and 9
42 Effect of End Friction Confinement on Dynamic Compres-sive Strength The macroscopic nominal compressive stress-strain curves of the concrete specimen under different strainrates and end friction coefficients are plotted and compared inFigure 11 Moreover the corresponding peak stresses that isthe nominal dynamic compressive strengths of concrete arereported in Table 2 Obviously both the stress-strain curvesof concrete in Figure 11 and the axial dynamic compressivestrengths in Table 2 demonstrate the effects of strain rates andend friction coefficients
It can be noted obviously from Figure 11 and Table 2 thatthe dynamic uniaxial compressive strength of concrete isimproved due to the end friction confinement effect Further-more under the same strain rates the ascending curves of theconcrete sample with various friction coefficients are almostoverlapped indicating that the elastic modulus of concreteis almost not influenced by the end friction confinementeffect The obtained compressive strengths and the softening
curves are distinct significantly because the stresses andstrains status as well as the fracture paths within the concretespecimen for different friction coefficients vary
For various strain rates the quantitative relationshipsbetween the obtained dynamic compressive strengths of theconcrete specimen and end friction coefficient are presentedin Figures 12(a) and 12(b) It can be seen clearly fromFigure 12 that the concrete dynamic compressive strengthincreases with the increase of end friction coefficient Whenthe end friction coefficient 120583 grows from 0 to 03 the uniaxialcompressive strength increases rapidly while the uniaxialdynamic compressive strength increases slightly and thengets to be stable when the end friction coefficient exceeds 03This is to say when the end friction coefficient exceeds 03 theend confinement effect on the dynamic compressivemechan-ical behavior of concrete can be ignored This can also beconcluded from the analysis resultsmentioned previously forexample the damage factor distribution of concrete pre-sented in Figure 10
Furthermore the results about the effect of end frictionconfinement on concrete dynamic compressive strength atmedium and low strain rates are similar to those at high strainrate For more information about the end confinement effectfor high strain rate refer to Li et al [40]
Figure 13 presents the damage distribution within theconcrete specimens at their corresponding peak stressesunder different end friction confinement conditions at thesame loading velocities Figure 13(a) shows the results for theloading condition of a relative lower strain rate that is 120576 = 1 times10minus2 sminus1 One can note that for ldquopurerdquo uniaxial compressivebehavior of concrete (ie the end friction 120583 between theconcrete specimen and the rigid block is zero 120583 = 0) thenumber of cracks generated or the damage degree withinthe specimen is very limited when reaching the compressivestrength of the concrete sample With the increase of endfriction coefficient for example 120583 = 01 and 02 the totalnumber of cracks ascends gradually but the number of cracksnear the top and bottom regions of the specimen descendsWhen the end friction coefficient becomes larger than 03(eg 120583 = 03 06 08 and infin) the number of cracks turnsto be stable but the width of the cracks broadens as can beseen in Figure 13(a)
Figure 13(b) shows the simulation results for the loadingcondition of a relative higher strain rate that is 120576 = 1 times10minus05 sminus1 For ldquopurerdquo uniaxial compression (ie the end
14 Shock and Vibration
7252015
9
Quasistatic loading
8
95
85
752515
Dynamic loading
20
Dynamic loading
20
10
9
8
25 30 35302520
11
10
9
8
Dynamic loading
Dynamic loading Dynamic loading= 1 times 10minus1 sminus1
= 1 times 10minus3 sminus1
= 1 times 10minus2 sminus1
= 1 times 10minus5 sminus1
times10minus3
0
3
6
9
12
15
18C
ompr
essiv
e st
ress
(MPa
)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
= 1 times 10minus15 sminus1
= 1 times 10minus05 sminus1
120576
120576
120576
120576
120576
120576
Figure 11 Continued
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
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Shock and Vibration
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2 Shock and Vibration
As known the end friction cannot be completely avoidedwhen conducting dynamic compressive tests The quantita-tive influence of end friction confinement should be deductedin the compressive DIF and it has been an interesting topicTo discover the influence of end friction on the macroscopicmechanical behavior of concrete including the dynamicfailure patterns and the nominal stress-strain curves as well asthe compressive DIF of concrete subjected to dynamic load-ings numerous efforts have been conducted For instanceusing the numerical methods Li and Meng [2] discussed theend friction confinement effect and found that for specimenswith 119871119863 = 05 [119871 means length of specimen and 119863 meansthe diameter of the specimen] the influence of the frictioncoefficient 120583 on DIF is insignificant when 120583 is less than01 but becomes considerable when it is larger than 02 Intheir simulations the strain rate employed ranges from 27times 101 sminus1 to 39 times 102 sminus1 and the friction coefficient utilizedranges from 0 to 07 Mu et al [6] modeled the dynamicmechanical properties of concrete subjected to the strain rateranging from 44 times 101 sminus1 to 147 times 102 sminus1 They found thatthe compressive strain-rate effect of concrete-like materialsis a pseudo property and the main mechanisms that initiatelateral confinement include the material lateral inertia andthe interface friction between the loading apparatus and theloaded specimen In addition in the works of Kim et al [7]Li et al [40] and Hao et al [4] the interface friction betweenthe loading apparatus and the loaded specimen was alsosimulated and examined They concluded that the frictioneffect is another factor in the so-called strain-rate effectThesesimulation efforts contribute to the understandings aboutthe dynamic compressive strength enhancement of concreteHowever these efforts are all focused on high strain ratesand the effect of end friction on the failure of concrete undermedium and low strain rates is rarely involved
The objective of the present study is therefore to examinethe quantitative influence of the confinement due to end fric-tion on the mechanical behavior of concrete under mediumand low strain rates Experimental results show that concreteis a heterogeneous brittle material that fractures throughthe formation growth and coalescence of microcracks [8]Moreover the failure behavior of concrete is closely relatedto the meso-microstructure of concrete and the hetero-geneities should therefore be considered [9ndash13] In this workconcrete was assumed to be a composite material consistingof mortarmatrix coarse aggregates and interfacial transitionzone (ITZ) between the former two phases Including thesecomponents in both experimental and numerical investiga-tions is essential because the mechanical properties of thesematerials are distinct In the computational model the dam-aged plasticity model implemented in a strain-rate sensitiveframework was utilized for the description of the dynamicmechanical behavior of the mortar matrix and the ITZ andelastic model was employed to characterize the mechanicalproperties of the aggregateThe friction behavior was utilizedto describe the interaction between the concrete specimensand loading apparatus By using the material model togetherwith the commercial software ABAQUS the reliability ofthe present approach was verified through the comparison
with the available test data Subsequently the dynamic axialcompressive mechanical behavior of concrete subjected todifferent medium and low strain rates was simulated underdifferent friction coefficients Furthermore the confinementmechanism of end friction on the compressive dynamicincrease factor (DIF) of concrete was studied and discussed
The paper is decomposed as follows The next sectiondescribes the rate-dependent constitutive framework forconcrete Section 3 presents the mesoscale computationalmodel for the simulation of the end friction confinementeffect and illustrates the verification of the present approachIn Section 4 the quantitative influences of the end frictionconfinement on the failure patterns the nominal stress-straincurves and the compressive DIF of concrete are exploredAnd finally the concluding remarks are given in Section 5
2 The Constitutive Framework forConcrete Mesocomponents
21 Concrete Damaged Plasticity Model The behavior ofconcrete is complex due to an array ofmorphological featuresaswell as deformation and failuremechanisms inherent in theconcrete microstructure The complicating factors includeheterogeneous constitution randomphase distribution arbi-trary microcrack patterns and internal granular frictionThecomplexity of the meso- or microscopic processes rendersexplicit resolution of the influences on a highly challengingtask
As known plasticity continuum damage mechanicsfracture mechanics elastic-damage and combined plasticityand damage mechanics are the common theories that havebeen widely used for the description of concrete mechanicalbehavior However the plasticity theory failed to address thedegradation of the material stiffness due to microcrackingthe fracture mechanics method was hard to reflect the nucle-ation of numerousmicrocracks and the growth of themicroc-racks to macrocracks and the continuum damage mechanicswith elasticity also could not describe the irreversible defor-mations and the inelastic volumetric expansion in compres-sion [13] Since both the stiffness degradation behavior andirreversible plastic deformations are contributing to the non-linear behavior of concrete a reasonable constitutive modelshould characterize the two distinct mechanisms In recentyears many coupled plasticity-damage models were pro-posed to describe the mechanical behavior of concrete suchas the work in the references [13 15ndash18] Among these effortsthe concrete damaged plasticity model was first proposed byLubliner et al [15] for monotonic loading and it was devel-oped later by Lee and Fenves [16] to consider the dynamic andcyclic loadings The model is a continuum plasticity basedmodel for concrete and it assumes that themain failuremech-anisms of the concrete are cracking in tension and crushingin compression The model which has been included in theABAQUS package has been widely used for the description ofthe static and dynamic mechanical behaviors of concrete-like materials for example in the publications [11 12 19 20]A brief presentation of the damaged plasticity model fromABAQUS is presented below
Shock and Vibration 3
Crack closure
ft
fc
E0(1 minus dc)(1 minus dt)
E0(1 minus dc)
E0(1 minus dt)
120576
120590c
120590t
E0
E0
Figure 1 Unaxial loading path of concrete plasticity damagemodel
211 Isotropic Damage Model The stress-strain relation forthe general three-dimensional multiaxial condition is givenby the scalar damage elasticity equation
120590 = (1 minus 119889)119863el0 (120576 minus 120576
pl) (1)
in which119863el0is the initial elasticity matrix 119889means the dam-
age variable and 120576pl is the plastic strain tensor Tensile damageand compressive damage are characterized independently bytwo hardening parameters 120576pl
119905and 120576pl119888(subscripts ldquo119905rdquo and ldquo119888rdquo
stand for tension and compression resp) which are referredto as equivalent plastic strains in tension and compressionThe evolution equations of the hardening variables 120576pl
119905and
120576pl119888 are conveniently formulated by considering uniaxial
loading conditions first and then extended to multiaxial con-ditionsThemodel assumes that the uniaxial tensile and com-pressive responses of concrete are characterized by damagedplasticity as shown in Figure 1 It is assumed that the stress-strain response follows a linear elastic relationship under uni-axial tension until the value of the failure stress119891
119905 is reached
The failure stress corresponds to the onset of microcrackingin the concrete material Beyond the failure stress the for-mation of microcracks is often represented macroscopicallywith a softening stress-strain response which induces strainlocalization in the concrete structure The uniaxial stress-strain curves can be converted into stress versus plastic straincurves of the form as
120590119905= 120590119905(120576
pl119905 120576
pl119905 120579 119891119894) (2a)
120590119888= 120590119888(120576
pl119888 120576
pl119888 120579 119891119894) (2b)
where 120576pl119905and 120576
pl119888are the equivalent plastic strain rates 120579 is the
temperature and 119891119894(119894 = 1 2 ) are other predefined field
variablesAs shown in Figure 1 when the specimen is unloaded
from any point on the strain softening branch of the stress-strain curves the unloading response is weakened the elasticstiffness of the material appears to be degraded Herein
the degradation of the elastic stiffness is characterized by twodamage variables tensile damage factor 119889
119905and compressive
damage factor 119889119888 and the stress-strain relationships under
tension and compression are respectively
120590119905= (1 minus 119889
119905) 1198640(120576119905minus 120576
pl119905) (3a)
120590119888= (1 minus 119889
119888) 1198640(120576119888minus 120576
pl119888) (3b)
This representation although somewhat simplified cap-tures the main features of concrete behavior Sometimesin order to avoid unreasonable mesh sensitive results thetensile post-failure behavior is given in terms of a fractureenergy cracking criterion by specifying a stress-displacementcurve instead of a stress-strain curve Under multiaxialloading conditions the evolution equation of the hardeningparameters for uniaxial loading should be extended
According to Lee and Fenvesrsquos work [16] tensile and com-pressive equivalent plastic strains have the following forms
120576pl119905= 119903 () 120576
plmax (4a)
120576pl119888= minus (1 minus 119903 ()) 120576
plmin (4b)
in which 120576plmax and 120576
plmin are the maximum and minimum
plastic strain tensors respectively 119903() means a multiaxialstress weight factor and is defined as
119903 () =
sum3
119894=1⟨119894⟩
sum3
119894=1
10038161003816100381610038161003816119894
10038161003816100381610038161003816
0 le 119903 () le 1 (5)
in which 119894are principal stress components (119894 = 1 2 for 2D
problems and 119894 = 1 2 3 for 3D problems) and the Macauleybracket ldquo⟨sdot⟩rdquo is defined by ⟨119909⟩ = 05 times (|119909| + 119909)
212 Plasticity Yield Surface The model makes use of theyield function of Lubliner et al [15] with the modificationsproposed by Lee and Fenves [16] to account for differentevolution of strength under tension and compression Theevolution of the yield surface is controlled by the two harden-ing variables 120576pl
119905and 120576pl119888 In terms of effective stress the yield
function 119865 is defined as
119865 = 119865 (120590 120576pl)
=1
1 minus 120572[119902 minus 3120572119901 + 120573 (120576
pl) ⟨120590max⟩ minus 120574 ⟨minus120590max⟩]
minus 120590119888(120576
pl119888) = 0
(6)
in which 119901 = minus(13)120590 119868 is the effective hydrostatic pressurestress 119868 is a stress invariant 119902 = radic(32)119878 119878means theMisesequivalent effective stress and 119878 is the effective stress deviatordefined as 119878 = 119901119868 + 120590 120590max is the maximum principaleffective stress Typical yield surface is depicted in Figure 2 forplane stress conditions
4 Shock and Vibration
Uniaxial compression
Uniaxial tension
Biaxial tension
Biaxial compression 120590c
120590t
(120590cc 120590cc)
1205901
1205902
Figure 2 Yield surface for plane stress conditions
1205901
1205902
1205903
Kc = 1
Kc = 23
Figure 3 Yield surfaces in the deviatory plane [119870119888
= 23
corresponds to Rankine formulation and119870119888= 1 corresponds to the
Drucker-Prager criterion]
Moreover parameters of 120572 120573(120576pl) and 120574 respectively canbe calculated by
120572 =120590119888119888120590119888minus 1
2120590119888119888120590119888minus 1
(7a)
120573 (120576pl) =
120590119888(120576
pl119888)
120590119905(120576
pl119905)
(1 minus 120572) minus (1 + 120572) (7b)
120574 =3 (1 minus 119870
119888)
2119870119888minus 1
(7c)
in which 120590119888119888120590119888means the ratio of initial equivalent-biaxial
compressive yield stress to initial uniaxial compressive yieldstress and its default value of the ratio is 116 according to[19 20] 119870
119888is the ratio of the tensile to the compressive
meridian and defines the shape of the yield surface in thedeviatory plane (see Figure 3)
213 Plastic Flow Rule The nonassociated potential plasticflow is employed in the present damaged plasticity modelThe flow potential function 119866(120590) used for this model is
the nonassociatedDrucker-Prager hyperbolic function and isdefined according to
119866 (120590) = radic(120578120590119905tan120595)2 + 1199022 minus 119901 tan120595 (8)
in which 120595 is the dilation angle measured in the 119901-119902 planeat high confining pressure 120590
119905is the uniaxial tensile stress at
failure 120578 is the eccentricity that gives the rate at which theplastic potential function approximates the asymptote (theflow potential tends to a straight line as the eccentricity tendsto zero) and its default value is equal to 01Thenonassociatedflow rule means that the plastic strain vector is normal to theplastic potential function that differs from the yield surface
The plastic strain rate 120576pl and the effective plastic strain
rate 120576pl can be derived as follows
120576pl=
120597119866
120597120590(9a)
120576pl= ℎ (120590 120576
pl) sdot 120576
pl (9b)
where is the plastic multiplierBecause the selected plastic flow is nonassociated to
obtain an acceptable rate of convergence the unsymmetricmatrix storage and solution scheme is used For more detailsabout the constitutive model refer to Lubliner et al [15] Leeand Fenves [16] and Du et al [11]
22 Dynamic Increase Factor (DIF) for Concrete The avail-able experimental and numerical observations have demon-strated that concrete and other cementitiousmaterials are ratesensitive [3 21 22] The strain rate effect has been studiedon different mechanical characteristics of concrete Youngrsquosmodulus Poissonrsquos ratio energy-absorption capacity andaxial strain atmaximumstrength are rate-sensitive quantitiesbut at amuch lower intensity than the compressive and tensilestrengths [3 23] Similar to the work [4 11] only the strengthenhancement was considered in the present study
So far many empirical and theoretical relations have beendeveloped to quantitatively describe the strain rate effect onconcrete properties In particular the code by the ComiteEuro-international du Beton (CEB) recommends variousvalues of the DIF for the tensile and compressive strengthsunder different strain rates based on the available test resultsThe formula of the compressive DIF recommended by CEB[3] has the following form
CDIF =119891cd119891cs
= (120576119889
120576cs)
1026120572
for 120576119889le 30 sminus1 (10a)
CDIF =119891cd119891cs
= 120574 ( 120576119889)13 for 120576
119889gt 30 sminus1 (10b)
where 119891cd is the dynamic compressive strength at the strainrate of 120576
119889(in the range of 30 times 10minus6ndash1000 sminus1) 120576cs = 30 times
10minus6 sminus1 (static strain rate) log 120574 = 6156120572 minus 049 120572 = (5 +
3119891cu4)minus1 119891cs is the static compressive strength and 119891cu is
the static cube compressive strength [in MPa] The DIF for
Shock and Vibration 5
the compressive strength in (10a) and (10b) was oftenadopted for example in the publications [10 11]
The CEB also gives empirical formulae to estimate theDIF for concrete tensile strength However comparisonbetween the available experimental results in the literaturewith the CEB empirical equations indicates that the CEBtensile DIF substantially underestimates the tensile DIF ofconcrete [24 25] In Malvar and Rossrsquos [24] work an empiri-cal formula was proposed and the formula for the tensile DIFcan be written as
TDIF =119891td119891ts
= (120576119889
120576ts)
120575
for 120576119889le 1 sminus1 (11a)
TDIF =119891td119891ts
= 120573(120576119889
120576ts)
13
for 120576119889gt 1 sminus1 (11b)
where 119891td and 119891ts are respectively the dynamic uniaxial ten-sile strength at the strain rate 120576
119889and the quasistatic uniaxial
tensile strength 120576ts = 10minus6 sminus1 (static strain rate) log120573 = 6120575minus2
120575 = 1(1 + 81198911015840
1198881198911015840
1198880) 11989110158401198880= 10MPa and 119891
1015840
119888is the quasistatic
uniaxial compressive strength of concrete (in MPa)
3 Mesoscale ComputationalModel for Concrete
Theoretical experimental and numerical studies indicatethat the failure pattern crack mode and even the velocity ofthe crack propagation are influenced by loading rate [11 26ndash28] The mechanical behaviors of concrete including themacroscopic mechanical properties and the failure patternsare associated with the micro-mesostructure of concreteDue to the complexity of concrete the failure behavior can bestudied numerically In the numerical simulations concreteheterogeneity should be accounted for and thus it requiresthe adoption of a mesoscale mechanical model in which theheterogeneity can be explicitly described
At themesoscale concretewas often assumed to be amul-tiphase composite composed of aggregate mortar matrix theinterfacial transition zones [ITZs] voids and so forth A lot ofwork [9 10 19 29] has demonstrated that the ITZs have a dra-matic influence on the failure pattern and the macromechan-ical properties of concrete However the mechanical proper-ties especially the dynamic mechanical behavior of the ITZsare not well understood yet [13 19 30ndash32] Moreover thereal typical thickness of ITZ is about 10ndash50120583m [9 10] whichlimits the minimum size of the finite element mesh In mostsimulation efforts the ITZ thickness is set as 02ndash08mm[9 10] 05mm [8] 04mm [19] and 1mm [12] for the sake ofsimplicity
31 Mesostructure and Mechanical Model of Concrete Con-crete exhibits heterogeneity in material and mechanicalproperties onmany length scales [29] At the mesoscale con-sidering the effect of heterogeneities of concrete the concretein the present work was regarded as a three-phase compositecomposed of coarse aggregate particles mortar matrix andthe ITZs between the former two phases Random aggregatemodels have long been demonstrated to be an effective
mesomechanical approach to simulating the failure processand the deformation of concrete and they have been widelyutilized in fracturemechanics of concrete for example in [11ndash13 33] Based on the concrete random aggregate model inwhich the shape size and distribution of the coarse aggregateparticles closely resemble real concrete in the statistical senselots of efforts have been carried out to investigate the macro-scopic mechanical behavior and failure mechanism of con-crete [10ndash12 29] In this work the concrete random aggregatemodel was therefore also employed
Due to great computational expense and memorydemand of mesoscale simulations it is in general notpossible to model the full structure at the mesoscale with thecomputational power available nowadays Herein the presentstudy only two-dimensional simulations were thus con-ducted Similar to the work [9ndash12 33] the aggregate particlesare modeled as circles with random spatial distributionenfolded by a thin interface layer of ITZ Similar to those in[11 12] the ldquotake-and-placerdquo method was utilized to generatethe coarse aggregate particles The fine ones and othercomponents (eg air voids) were assumed to be mixed upwith the cement paste establishing the mortar matrix phaseThis matrix phase can thus be regarded as a homogeneouscomponent at the mesoscale The material properties of thepaste phase are thus strongly dependent on the type of cementused amount of pores water to cement ratio and otheradditives present in the concrete which can be determinedby microscale simulation efforts Furthermore the Fullercurve widely utilized for example in [11 12] was selected todetermine the distribution of aggregate with different sizesemployed in the concrete specimen The aggregate particleswere then placed into the matrix one by one at randomlydetermined positions and in such a way that no overlappingwith particles already placed Finally at the mesoscale aggre-gate particles (typically sand or gravel) and the surroundingITZ layers behave as inclusions in the matrix phase of mortarmatrix
Figure 4 presents a typical schematic diagram of concretemesostructure generated by employing the above approachThe size of the heterogeneous concrete specimen is 150mm times
150mm Note that aggregate particles in real concrete arenot perfectly circular However the efforts in [10 11] haveindicated that the effect of aggregate shape on macroscopicstress-strain curve of concrete seems to be very smallSimilar to that in [11 34] the concrete sample contains 6medium stones with a diameter of 30mm and 56 small stoneswith a diameter of 12mm The concrete specimens involveabout 469 of aggregate per volume In Figure 4 the greenareas mean the aggregate phase the red thin-layer zonessurrounding the aggregate particles are the ITZs and the greyzones denote the mortar matrix Herein the interfacial zonesare viewed as uniform thickness shells placed concentricallyaround each aggregate Similar to the work [34] the thicknessof the ITZ was set as 1mm
To describe the influence of end friction confinement onthe dynamic compressive mechanical properties of concretetwo rigid blocks (see the two blue blocks in Figure 4) wereplaced respectively at the top and the bottom of the con-crete specimen The interactions between the heterogeneous
6 Shock and Vibration
y
x
AggregateITZ
Mortar matrixRigid block
Uniaxial compression
Unit mm End
fric
tion
25 25150
2525
150
Figure 4 Mesoscale mechanical model of concrete under dynamic uniaxial compression considering the influence of end frictionconfinement The specimen has 22346 elements [For interpretation of the references to color in this figure legend the reader is referredto the web version of this paper]
concrete specimen and the two rigid blocks that is the twored-line regions are implemented by the classic coulombfriction behavior The friction coefficients considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces ofthe specimen were fixed in the horizontal direction) fora quantitative assessment of the end friction confinementeffect As known the DIF difference obtained from thesimulation results with different friction coefficients canthen be attributed purely to the influence of end frictionconfinement effects
Themeshing of these concrete specimens were conductedwith four node solid elements with a linear strain field Tohave a better understanding of concrete fracture the averagemesh size was l mm which is consistent with that in the workfrom Hentz et al [23] and Du et al [11 12]
32 Mechanical Parameters for the Three MesocomponentsIn Zhou and Haorsquos [11 13] and Snozzi et alrsquos [35] workthe uniaxial tensile and compressive mechanical behaviorof concrete at high strain rate were studied From theirsimulation observations it can be noticed that no damagegenerates in the aggregate phaseMoreover in Pedersen et alrsquos[8] simulation of the dynamic tensile behavior of concretethe aggregate grains were assumed to follow a linear elasticmaterial behaviorThis is because the tensile and compressivestrengths of the aggregate are much larger than those of mor-tar matrix and the ITZs Similar to the work [8 11] the aggre-gate was assumed as elastic in the following simulationsThistreatment should work for the concrete subjected to mediumand low strain rates as discussed in the present study
To the mortar matrix and the ITZs the continuumdamage mechanics theories mentioned previously wereemployed to describe their mechanical properties In contin-uum mechanics the constitutive model is often expressed in
terms of stress-strain relations When the material exhibitsstrain-softening behavior leading to the strain localizationbehavior this formulation leads to a strongmesh dependencyof the finite element results in which the energy dissipateddecreases upon mesh refinement [11 19] Similar to the workin [10 11 19] to avoid or release unreasonable mesh sensitiveresults the tensile postfailure behavior was given in terms ofa fracture energy cracking criterion by specifying a stress-displacement curve instead of a stress-strain curve In addi-tion unlike discrete crack models [36 37] the continuumdamaged plasticity model based on continuum mechanicsuses damage factors such asDAMAGEC for compression andDAMAGET for tension to describe the fracture behavior andit is not capable of providing accurate crack geometry such ascrack width
The main mechanical parameters including the elasticmodulus Poissonrsquos ratio and uniaxial tensilecompressivestrengths of the three mesoconstituents used in this study forthe following numerical analysis were listed in Table 1
It is to be noted that the DIFs given in Section 22 are builtbased on the test results on concrete material The strain rateeffects for the aggregate phase mortar matrix and the ITZare essentially distinct as illustrated in [38 39] NeverthelessGrote et alrsquos [21] experimental observations indicate that thedynamic mechanical behavior of mortar matrix is closelysimilar to that of concrete In addition the ITZ layer can betreated as a kind of mortar matrix with a high(er) porosity[34] and thus its dynamic mechanical behavior can also beregarded as similar to those of mortar matrix and concreteIn summary it is assumed that the ITZ and the mortarmatrix have the same DIFs mentioned previously The treat-ments are consistent with the ones in [9 10] The strainrate effect for both the mortar matrix and the ITZs ontheir tensilecompressive strengths was incorporated intothe plasticity damaged model which was represented by
Shock and Vibration 7
Table 1 Mechanical parameters of the concrete mesocomponentsused in the study
Mortar matrix ITZ AggregateMass density 120588 [kgm3] 275 times 103 275 times 103 288 times 103
Elastic modulus [GPa] 30lowast
25lowast
70lowast
Poissonrsquos ratio 02lowast
022lowast
016lowast
Dilation angle 120595 [∘] 30 30Eccentricity 120578 01 01Shape factor 119870
1198880667 0667
Stress ratio 120590119888119888120590119888
116 116Tensile yield stress 120590
119905[MPa] 143
lowast12lowast
Compressive yield stress 1205901198880
[MPa] 143lowast
12lowast
Ultimate compressive yieldstress 120590cu [MPa] 143 12
Note data with ldquolowastrdquo are quoted from Du et al [12]
a dynamic increase factor (ie the DIF) with respect to strainrate
33 BoundaryLoading Conditions and FE Simulations Toexamine the effects of end friction confinement on themacromechanical behavior of concrete subjected to dynamiccompressive loadings the failure behavior of the concretespecimen was explored The corresponding loading andboundary conditions for the interaction system were illus-trated as follows (1) constant vertical velocity V was appliedon the top surface of the rigid block and the left and rightsides of the specimen are free of stress (2) the movementat the bottom rigid block was fixed at both the vertical andhorizontal directions (3) friction behavior between the twoblocks and the concrete sample was set The nominal strainrate 120576 is defined as the applied velocity divided by the heightof the specimen that is 120576 = Vℎ where ℎ is the height of thespecimen
In the following simulations ABAQUS increased auto-matically the size of step time going from smaller one to themaximumauthorized defined by the user For all the concretespecimens the numerical simulations were performed in aplane strain condition
34 Verification of the Mesoscale Approach In reality theavailable tests on loading rate effect of concrete are not veryrich and the test data is also not complete Comparativelyspeaking Dilger et alrsquos [14] test data is the most completeone and it is often used to verify the reliability of the analysismethod or model such as in [26]
To illustrate the reliability and accuracy of the presentmesoscale simulation method Dilger et alrsquos [14] test on thedynamic uniaxial compressive behavior of concrete was alsoselected for the comparison in this section In Dilger et alrsquos[14] experiment the macroscopic mechanical behavior ofconcrete under different nominal strain rates (ie the strainrates of 333 times 10minus5 sminus1 333 times 10minus3 sminus1 and 02 sminus1) was
explored and the complete compressive stress-strain curvesof concrete were obtained
In the previouswork [33] a series of dynamic compressivetest of concrete under different strain rates were conductedbased on the present mesoscale mechanical method includ-ing 120576 = 333 times 10minus5 sminus1 1 times 10minus4 sminus1 333 times 10minus3 sminus1 1 times 10minus2 sminus15 times 10minus2 sminus1 02 sminus1 1 sminus1 100 sminus1 and 200 sminus1 It is to benoted that in the simulations the concrete specimens werefixed at one end and loaded longitudinally through an appliedconstant velocity at the other end The detailed mechanicalparameters and analysis method can refer to [33]
Figure 5 presents the failure patterns of the concretespecimen subjected to different nominal strain rates Onecan notice that with the increase of strain rate the numberof cracks (ie the red damaged region) increases obviouslyand the crack branching behavior occurs Therefore withthe increase of strain rate the fracture of concrete requiresmore energy demand to reach failure which should be themain reason for the improvement of the dynamic strength ofconcrete
Figure 6(a) reports the comparison between the sim-ulations results (solid curves) and the experimental data(symbols) in terms of nominal stress (applied forces dividedby the specimen cross sectional area) versus nominal strain(the displacement generated at the applied-load end dividedby the length of the specimen) curves and the agreementis very good It should be noted herein that as mentionedpreviously the relatedmechanical and physical parameters ofthe concrete mixture used in the test are not full especiallythe mechanical parameters of the ITZ Accordingly in thepreviouswork [33] themechanical parameters (especially theelasticmodulus and the strength) of the ITZwere determinedby the inversion method on the basis of only two strainrates (333 times 10minus5 sminus1 and 333 times 10minus3 sminus1) The simulationof the third available strain (ie 02 sminus1) can be regarded asa validation of the ability of the model to predict concretestrength outside the range of strain rates used for calibrationThis treatment is similar to that in [26]
Furthermore the compressive DIFs were evaluatedaccording to the simulation results and the comparison of thepresent simulation results and some available experimentalobservations is plotted in Figure 6(b) It can be observedthat the present simulation results agree very well with thecollective experimental data This indicates that the presentanalysis method can well simulate the dynamic compressivebehavior of concrete The validated mesoscale mechanicalapproach would be employed in the following simulations tostudy the effect of end friction confinement on the dynamiccompressive behavior of concrete
4 Dynamic Compressive FailureBehavior of Concrete
On the basis of the mesoscale mechanical model describedin Section 3 the simulations of the dynamic axial com-pression of the concrete specimen with various end fric-tion coefficients were implemented The loading velocitiesadopted on the upper rigid block in the simulations are
8 Shock and Vibration
10Damage
120576 = 333 times 10minus5 120576 = 1 times 10minus4 120576 = 333 times 10minus3 120576 = 1 times 10minus2 120576 = 5 times 10minus2
120576 = 2 times 10minus1 120576 = 1 120576 = 100 120576 = 200
Figure 5 Compressive failure patterns of the concrete specimen under different strain rates ranging from 1 times 10minus5 sminus1 to 200 sminus1
Compression test(Dilger et al 1984) and present model
Nom
inal
com
pres
sive
stre
ss (M
Pa)
0002 00030001 0004 0005 00060Compressive strain
0
10
20
30
40
120576 = 333 times 10minus5 sminus1
120576 = 333 times 10minus3 sminus1
120576 = 02 sminus1
(a)
001 1 100
09
12
15
18
21
24
Com
pres
sive D
IF
Test data Present method
1E minus 6 1E minus 4
Strain rate (sminus1)
(b)
Figure 6 (a) Comparison of the present simulation results and Dilger et alrsquos [14] test data and (b) compressive DIFs for the simulation resultsand some available test data
Shock and Vibration 9
Dynamic loading
0
2
4
6
8
10
12
14
Com
pres
sive
stre
ss (M
Pa)
120576 = 1 times 10minus1 sminus1
times10minus3
Mesh size 15mmMesh size 10mmMesh size 05mm
End friction coefficient 120583 = 06
1 432 5 6 70Strain 120576
(a)
Mesh size 15mmMesh size 10mmMesh size 05mm
Damage factor0 1
(b)
Figure 7 (a) The simulation results of three concrete specimens with the same distribution of aggregates and different mesh sizes and(b) damage distribution of the concrete specimens with different mesh sizes under the same strain rate and friction coefficients at theirpeak stresses
V = 15 times 10minus6ms 15 times 10minus4ms 15 times 10minus3ms 15 times
10minus25ms 15 times 10minus2ms 15 times 10minus15ms and 15 times 10minus1msin an ascending sequence and in every loading cycle the con-stant velocity was utilized The corresponding macroscopicnominal strain rates are 120576 = 1 times 10minus5 sminus1 (quasistatic) 1 times10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1and 1 times 100 sminus1 respectively Moreover as mentioned previ-ously the seven end friction coefficients 120583 considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces of thespecimenwere fixed in the horizontal direction) respectively
To check the mesh sensitivity in the simulations threedifferentmesh sizeswere utilized that is 05mm 10mm and
15mm Figure 7(a) presents the nominal compressive stress-strain curves of the concrete specimen subjected to a nominalstrain rate of 01 sminus1 with the same end friction coefficientand the three different mesh sizes It can be found clearlyfrom Figure 7(a) that the mesh sizes (ie 05mm 10mmand 15mm) have less influence on the stress-strain curvesThe three curves are also overlapped Figure 7(b) shows thedamage distribution of the three concrete specimens men-tioned above with the same distribution of aggregates Onecannotice that the failure patterns of the three specimenswithdifferent mesh sizes are closely similar to each other Conse-quently the mesh size of 15mm was used in the followingsimulations
10 Shock and Vibration
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
Equivalent plastic strain times10minus300 56
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
120576
120576
120576
120576
120576
Figure 8 Equivalent plastic strain distribution within the concrete specimen under different strain rates and end friction coefficients at theirpeak compressive stresses
41 Effects of Strain Rate and End Friction Confinement onFailure Patterns of Concrete Figure 8 presents the equivalentplastic strain distribution within the concrete specimensunder five groups of different strain rates ( 120576 = 1 times 10minus5 sminus11 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus1 sminus1 and 1 times 100 sminus1) and fourgroups of different friction coefficients (120583 = 0 03 08 andinfin) at their peak compressive stresses (ie the compressivestrength) One can note from Figures 8(a)ndash8(d) that for thespecimen with the same friction coefficient with the increase
of nominal strain rate the equivalent plastic strain withinconcrete increases obviously In addition as the frictioncoefficient 120583 increases from 0 to infin the equivalent plasticstrain within concrete at reaching the peak stress varies
For the specimenwith the friction coefficient of 0 and 03the obtained plastic strain distributions within the concretespecimens are obviously different For the one with the fric-tion coefficient of 03 and 08 the obtained plastic strain dis-tributions are slightly different And for that with the friction
Shock and Vibration 11
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
000 49
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Maximum principal stress (MPa)
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 9 Maximum principal stress distribution within the concrete specimen under different strain rates and end friction coefficients attheir peak compressive stresses
coefficient of 08 andinfin the obtained plastic strain distribu-tions are almost totally consistent That is to say when thefriction coefficient becomes larger than 08 the effect of endfriction confinement on the failure patterns of concrete canbe ignored
The maximum principal stress distributions within theconcrete specimens under the five groups of different strainrates and the four different friction coefficients at the peakcompressive stresses are presented in Figure 9 It can be
noted intuitively from Figure 9 that the changes of nominalstrain rate and friction coefficient have a significant influenceon the maximum principal stress distribution of the speci-menWith the increase of end friction coefficient the value ofmaximum principal stress gets large and the distribution areadraws close to central section from the top and bottom of theconcrete specimen respectively at same loading velocity
The damage (ie the cracks) distributions within theconcrete specimens corresponding to Figures 8 and 9 are
12 Shock and Vibration
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
0 1
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Damage factor
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 10 Damage distribution within the concrete specimens under different strain rates and friction coefficients at their peak stresses
presented in Figure 10 for different loading velocities anddifferent end friction coefficients In Figure 10 differentcolors represent different damage indexes The red colordenotes the most serious damage while the blue color meansthat no damage generates The white rounded areas whichare regarded as aggregates in these models have no damage
It can be noticed clearly from Figure 10 that the damagedareas increase with the growth of nominal strain rate Whenthe nominal strain rate is relatively low(er) (eg 1 times 10minus5 sminus1)the damaged area of the specimens is small when reaching
their peak stress Accordingly the damage regions (iecracks) are narrow and short and the number of cracks islimited As the nominal strain rate rises from 1times 10minus5 sminus1 to 1times100 sminus1 the damaged area and the number of cracks increasegradually When the nominal strain rate is relatively high(er)(eg 1 times 100 sminus1) a lot of areas are damaged in different levelsThe cracks widen and link together forming a crack networksimultaneously
Therefore it can be concluded that with the increase ofloading velocity the nominal strain rate increases gradually
Shock and Vibration 13
Table 2 Dynamic compressive strength of concrete under different end friction coefficients
120583Dynamic compressive strength [MPa]
1 times 10minus5 sminus1 1 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1 1 times 100 sminus1
0 793 806 858 919 1042 1197 153901 829 838 906 977 1113 1297 161202 846 857 926 1007 1137 1349 168203 849 864 939 1016 1167 1355 169606 857 877 955 1036 1175 1382 173608 860 881 962 1042 1185 1391 1745infin 875 892 980 1067 1212 1406 1749
and the number of cracks or damaged zones increases whenthe apparent compressive strength of concrete is reachedTheenergy consumption of the loading process increases corre-spondinglyThis should be the major reason for the improve-ment of dynamic compressive strength of concrete materials
It can be found obviously from the comparison amongFigures 10(a)ndash10(d) that the damage states of concrete spec-imens are diverse at their peak stresses for different endfriction conditions
Compared with the concrete specimen without end fric-tion confinement (ie 120583 = 0) the deformation at the end ofthe specimen considering the effect of end friction (ie120583 gt 0)was obviously hindered In addition with the increase of endfriction coefficient the obstruction degree of deformationraises For the specimen with the two ends completely fixed(ie 120583 = infin) there is no horizontal deformation at the endsmaking the confinement effect very strong
From Figure 10 one can note that a larger end frictioncoefficient leads to a lower damage level in the top and bottomof the specimen with a constant nominal strain rate Forlarger end friction coefficient the damaged areas draw closeto the central section from the top and bottom of the concretespecimenThese phenomena should generate due to the effectof the end friction confinement which changes the uniaxialloading state in the local regions of concrete These can alsobe illustrated from the simulation results in Figures 8 and 9
42 Effect of End Friction Confinement on Dynamic Compres-sive Strength The macroscopic nominal compressive stress-strain curves of the concrete specimen under different strainrates and end friction coefficients are plotted and compared inFigure 11 Moreover the corresponding peak stresses that isthe nominal dynamic compressive strengths of concrete arereported in Table 2 Obviously both the stress-strain curvesof concrete in Figure 11 and the axial dynamic compressivestrengths in Table 2 demonstrate the effects of strain rates andend friction coefficients
It can be noted obviously from Figure 11 and Table 2 thatthe dynamic uniaxial compressive strength of concrete isimproved due to the end friction confinement effect Further-more under the same strain rates the ascending curves of theconcrete sample with various friction coefficients are almostoverlapped indicating that the elastic modulus of concreteis almost not influenced by the end friction confinementeffect The obtained compressive strengths and the softening
curves are distinct significantly because the stresses andstrains status as well as the fracture paths within the concretespecimen for different friction coefficients vary
For various strain rates the quantitative relationshipsbetween the obtained dynamic compressive strengths of theconcrete specimen and end friction coefficient are presentedin Figures 12(a) and 12(b) It can be seen clearly fromFigure 12 that the concrete dynamic compressive strengthincreases with the increase of end friction coefficient Whenthe end friction coefficient 120583 grows from 0 to 03 the uniaxialcompressive strength increases rapidly while the uniaxialdynamic compressive strength increases slightly and thengets to be stable when the end friction coefficient exceeds 03This is to say when the end friction coefficient exceeds 03 theend confinement effect on the dynamic compressivemechan-ical behavior of concrete can be ignored This can also beconcluded from the analysis resultsmentioned previously forexample the damage factor distribution of concrete pre-sented in Figure 10
Furthermore the results about the effect of end frictionconfinement on concrete dynamic compressive strength atmedium and low strain rates are similar to those at high strainrate For more information about the end confinement effectfor high strain rate refer to Li et al [40]
Figure 13 presents the damage distribution within theconcrete specimens at their corresponding peak stressesunder different end friction confinement conditions at thesame loading velocities Figure 13(a) shows the results for theloading condition of a relative lower strain rate that is 120576 = 1 times10minus2 sminus1 One can note that for ldquopurerdquo uniaxial compressivebehavior of concrete (ie the end friction 120583 between theconcrete specimen and the rigid block is zero 120583 = 0) thenumber of cracks generated or the damage degree withinthe specimen is very limited when reaching the compressivestrength of the concrete sample With the increase of endfriction coefficient for example 120583 = 01 and 02 the totalnumber of cracks ascends gradually but the number of cracksnear the top and bottom regions of the specimen descendsWhen the end friction coefficient becomes larger than 03(eg 120583 = 03 06 08 and infin) the number of cracks turnsto be stable but the width of the cracks broadens as can beseen in Figure 13(a)
Figure 13(b) shows the simulation results for the loadingcondition of a relative higher strain rate that is 120576 = 1 times10minus05 sminus1 For ldquopurerdquo uniaxial compression (ie the end
14 Shock and Vibration
7252015
9
Quasistatic loading
8
95
85
752515
Dynamic loading
20
Dynamic loading
20
10
9
8
25 30 35302520
11
10
9
8
Dynamic loading
Dynamic loading Dynamic loading= 1 times 10minus1 sminus1
= 1 times 10minus3 sminus1
= 1 times 10minus2 sminus1
= 1 times 10minus5 sminus1
times10minus3
0
3
6
9
12
15
18C
ompr
essiv
e st
ress
(MPa
)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
= 1 times 10minus15 sminus1
= 1 times 10minus05 sminus1
120576
120576
120576
120576
120576
120576
Figure 11 Continued
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
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Shock and Vibration 3
Crack closure
ft
fc
E0(1 minus dc)(1 minus dt)
E0(1 minus dc)
E0(1 minus dt)
120576
120590c
120590t
E0
E0
Figure 1 Unaxial loading path of concrete plasticity damagemodel
211 Isotropic Damage Model The stress-strain relation forthe general three-dimensional multiaxial condition is givenby the scalar damage elasticity equation
120590 = (1 minus 119889)119863el0 (120576 minus 120576
pl) (1)
in which119863el0is the initial elasticity matrix 119889means the dam-
age variable and 120576pl is the plastic strain tensor Tensile damageand compressive damage are characterized independently bytwo hardening parameters 120576pl
119905and 120576pl119888(subscripts ldquo119905rdquo and ldquo119888rdquo
stand for tension and compression resp) which are referredto as equivalent plastic strains in tension and compressionThe evolution equations of the hardening variables 120576pl
119905and
120576pl119888 are conveniently formulated by considering uniaxial
loading conditions first and then extended to multiaxial con-ditionsThemodel assumes that the uniaxial tensile and com-pressive responses of concrete are characterized by damagedplasticity as shown in Figure 1 It is assumed that the stress-strain response follows a linear elastic relationship under uni-axial tension until the value of the failure stress119891
119905 is reached
The failure stress corresponds to the onset of microcrackingin the concrete material Beyond the failure stress the for-mation of microcracks is often represented macroscopicallywith a softening stress-strain response which induces strainlocalization in the concrete structure The uniaxial stress-strain curves can be converted into stress versus plastic straincurves of the form as
120590119905= 120590119905(120576
pl119905 120576
pl119905 120579 119891119894) (2a)
120590119888= 120590119888(120576
pl119888 120576
pl119888 120579 119891119894) (2b)
where 120576pl119905and 120576
pl119888are the equivalent plastic strain rates 120579 is the
temperature and 119891119894(119894 = 1 2 ) are other predefined field
variablesAs shown in Figure 1 when the specimen is unloaded
from any point on the strain softening branch of the stress-strain curves the unloading response is weakened the elasticstiffness of the material appears to be degraded Herein
the degradation of the elastic stiffness is characterized by twodamage variables tensile damage factor 119889
119905and compressive
damage factor 119889119888 and the stress-strain relationships under
tension and compression are respectively
120590119905= (1 minus 119889
119905) 1198640(120576119905minus 120576
pl119905) (3a)
120590119888= (1 minus 119889
119888) 1198640(120576119888minus 120576
pl119888) (3b)
This representation although somewhat simplified cap-tures the main features of concrete behavior Sometimesin order to avoid unreasonable mesh sensitive results thetensile post-failure behavior is given in terms of a fractureenergy cracking criterion by specifying a stress-displacementcurve instead of a stress-strain curve Under multiaxialloading conditions the evolution equation of the hardeningparameters for uniaxial loading should be extended
According to Lee and Fenvesrsquos work [16] tensile and com-pressive equivalent plastic strains have the following forms
120576pl119905= 119903 () 120576
plmax (4a)
120576pl119888= minus (1 minus 119903 ()) 120576
plmin (4b)
in which 120576plmax and 120576
plmin are the maximum and minimum
plastic strain tensors respectively 119903() means a multiaxialstress weight factor and is defined as
119903 () =
sum3
119894=1⟨119894⟩
sum3
119894=1
10038161003816100381610038161003816119894
10038161003816100381610038161003816
0 le 119903 () le 1 (5)
in which 119894are principal stress components (119894 = 1 2 for 2D
problems and 119894 = 1 2 3 for 3D problems) and the Macauleybracket ldquo⟨sdot⟩rdquo is defined by ⟨119909⟩ = 05 times (|119909| + 119909)
212 Plasticity Yield Surface The model makes use of theyield function of Lubliner et al [15] with the modificationsproposed by Lee and Fenves [16] to account for differentevolution of strength under tension and compression Theevolution of the yield surface is controlled by the two harden-ing variables 120576pl
119905and 120576pl119888 In terms of effective stress the yield
function 119865 is defined as
119865 = 119865 (120590 120576pl)
=1
1 minus 120572[119902 minus 3120572119901 + 120573 (120576
pl) ⟨120590max⟩ minus 120574 ⟨minus120590max⟩]
minus 120590119888(120576
pl119888) = 0
(6)
in which 119901 = minus(13)120590 119868 is the effective hydrostatic pressurestress 119868 is a stress invariant 119902 = radic(32)119878 119878means theMisesequivalent effective stress and 119878 is the effective stress deviatordefined as 119878 = 119901119868 + 120590 120590max is the maximum principaleffective stress Typical yield surface is depicted in Figure 2 forplane stress conditions
4 Shock and Vibration
Uniaxial compression
Uniaxial tension
Biaxial tension
Biaxial compression 120590c
120590t
(120590cc 120590cc)
1205901
1205902
Figure 2 Yield surface for plane stress conditions
1205901
1205902
1205903
Kc = 1
Kc = 23
Figure 3 Yield surfaces in the deviatory plane [119870119888
= 23
corresponds to Rankine formulation and119870119888= 1 corresponds to the
Drucker-Prager criterion]
Moreover parameters of 120572 120573(120576pl) and 120574 respectively canbe calculated by
120572 =120590119888119888120590119888minus 1
2120590119888119888120590119888minus 1
(7a)
120573 (120576pl) =
120590119888(120576
pl119888)
120590119905(120576
pl119905)
(1 minus 120572) minus (1 + 120572) (7b)
120574 =3 (1 minus 119870
119888)
2119870119888minus 1
(7c)
in which 120590119888119888120590119888means the ratio of initial equivalent-biaxial
compressive yield stress to initial uniaxial compressive yieldstress and its default value of the ratio is 116 according to[19 20] 119870
119888is the ratio of the tensile to the compressive
meridian and defines the shape of the yield surface in thedeviatory plane (see Figure 3)
213 Plastic Flow Rule The nonassociated potential plasticflow is employed in the present damaged plasticity modelThe flow potential function 119866(120590) used for this model is
the nonassociatedDrucker-Prager hyperbolic function and isdefined according to
119866 (120590) = radic(120578120590119905tan120595)2 + 1199022 minus 119901 tan120595 (8)
in which 120595 is the dilation angle measured in the 119901-119902 planeat high confining pressure 120590
119905is the uniaxial tensile stress at
failure 120578 is the eccentricity that gives the rate at which theplastic potential function approximates the asymptote (theflow potential tends to a straight line as the eccentricity tendsto zero) and its default value is equal to 01Thenonassociatedflow rule means that the plastic strain vector is normal to theplastic potential function that differs from the yield surface
The plastic strain rate 120576pl and the effective plastic strain
rate 120576pl can be derived as follows
120576pl=
120597119866
120597120590(9a)
120576pl= ℎ (120590 120576
pl) sdot 120576
pl (9b)
where is the plastic multiplierBecause the selected plastic flow is nonassociated to
obtain an acceptable rate of convergence the unsymmetricmatrix storage and solution scheme is used For more detailsabout the constitutive model refer to Lubliner et al [15] Leeand Fenves [16] and Du et al [11]
22 Dynamic Increase Factor (DIF) for Concrete The avail-able experimental and numerical observations have demon-strated that concrete and other cementitiousmaterials are ratesensitive [3 21 22] The strain rate effect has been studiedon different mechanical characteristics of concrete Youngrsquosmodulus Poissonrsquos ratio energy-absorption capacity andaxial strain atmaximumstrength are rate-sensitive quantitiesbut at amuch lower intensity than the compressive and tensilestrengths [3 23] Similar to the work [4 11] only the strengthenhancement was considered in the present study
So far many empirical and theoretical relations have beendeveloped to quantitatively describe the strain rate effect onconcrete properties In particular the code by the ComiteEuro-international du Beton (CEB) recommends variousvalues of the DIF for the tensile and compressive strengthsunder different strain rates based on the available test resultsThe formula of the compressive DIF recommended by CEB[3] has the following form
CDIF =119891cd119891cs
= (120576119889
120576cs)
1026120572
for 120576119889le 30 sminus1 (10a)
CDIF =119891cd119891cs
= 120574 ( 120576119889)13 for 120576
119889gt 30 sminus1 (10b)
where 119891cd is the dynamic compressive strength at the strainrate of 120576
119889(in the range of 30 times 10minus6ndash1000 sminus1) 120576cs = 30 times
10minus6 sminus1 (static strain rate) log 120574 = 6156120572 minus 049 120572 = (5 +
3119891cu4)minus1 119891cs is the static compressive strength and 119891cu is
the static cube compressive strength [in MPa] The DIF for
Shock and Vibration 5
the compressive strength in (10a) and (10b) was oftenadopted for example in the publications [10 11]
The CEB also gives empirical formulae to estimate theDIF for concrete tensile strength However comparisonbetween the available experimental results in the literaturewith the CEB empirical equations indicates that the CEBtensile DIF substantially underestimates the tensile DIF ofconcrete [24 25] In Malvar and Rossrsquos [24] work an empiri-cal formula was proposed and the formula for the tensile DIFcan be written as
TDIF =119891td119891ts
= (120576119889
120576ts)
120575
for 120576119889le 1 sminus1 (11a)
TDIF =119891td119891ts
= 120573(120576119889
120576ts)
13
for 120576119889gt 1 sminus1 (11b)
where 119891td and 119891ts are respectively the dynamic uniaxial ten-sile strength at the strain rate 120576
119889and the quasistatic uniaxial
tensile strength 120576ts = 10minus6 sminus1 (static strain rate) log120573 = 6120575minus2
120575 = 1(1 + 81198911015840
1198881198911015840
1198880) 11989110158401198880= 10MPa and 119891
1015840
119888is the quasistatic
uniaxial compressive strength of concrete (in MPa)
3 Mesoscale ComputationalModel for Concrete
Theoretical experimental and numerical studies indicatethat the failure pattern crack mode and even the velocity ofthe crack propagation are influenced by loading rate [11 26ndash28] The mechanical behaviors of concrete including themacroscopic mechanical properties and the failure patternsare associated with the micro-mesostructure of concreteDue to the complexity of concrete the failure behavior can bestudied numerically In the numerical simulations concreteheterogeneity should be accounted for and thus it requiresthe adoption of a mesoscale mechanical model in which theheterogeneity can be explicitly described
At themesoscale concretewas often assumed to be amul-tiphase composite composed of aggregate mortar matrix theinterfacial transition zones [ITZs] voids and so forth A lot ofwork [9 10 19 29] has demonstrated that the ITZs have a dra-matic influence on the failure pattern and the macromechan-ical properties of concrete However the mechanical proper-ties especially the dynamic mechanical behavior of the ITZsare not well understood yet [13 19 30ndash32] Moreover thereal typical thickness of ITZ is about 10ndash50120583m [9 10] whichlimits the minimum size of the finite element mesh In mostsimulation efforts the ITZ thickness is set as 02ndash08mm[9 10] 05mm [8] 04mm [19] and 1mm [12] for the sake ofsimplicity
31 Mesostructure and Mechanical Model of Concrete Con-crete exhibits heterogeneity in material and mechanicalproperties onmany length scales [29] At the mesoscale con-sidering the effect of heterogeneities of concrete the concretein the present work was regarded as a three-phase compositecomposed of coarse aggregate particles mortar matrix andthe ITZs between the former two phases Random aggregatemodels have long been demonstrated to be an effective
mesomechanical approach to simulating the failure processand the deformation of concrete and they have been widelyutilized in fracturemechanics of concrete for example in [11ndash13 33] Based on the concrete random aggregate model inwhich the shape size and distribution of the coarse aggregateparticles closely resemble real concrete in the statistical senselots of efforts have been carried out to investigate the macro-scopic mechanical behavior and failure mechanism of con-crete [10ndash12 29] In this work the concrete random aggregatemodel was therefore also employed
Due to great computational expense and memorydemand of mesoscale simulations it is in general notpossible to model the full structure at the mesoscale with thecomputational power available nowadays Herein the presentstudy only two-dimensional simulations were thus con-ducted Similar to the work [9ndash12 33] the aggregate particlesare modeled as circles with random spatial distributionenfolded by a thin interface layer of ITZ Similar to those in[11 12] the ldquotake-and-placerdquo method was utilized to generatethe coarse aggregate particles The fine ones and othercomponents (eg air voids) were assumed to be mixed upwith the cement paste establishing the mortar matrix phaseThis matrix phase can thus be regarded as a homogeneouscomponent at the mesoscale The material properties of thepaste phase are thus strongly dependent on the type of cementused amount of pores water to cement ratio and otheradditives present in the concrete which can be determinedby microscale simulation efforts Furthermore the Fullercurve widely utilized for example in [11 12] was selected todetermine the distribution of aggregate with different sizesemployed in the concrete specimen The aggregate particleswere then placed into the matrix one by one at randomlydetermined positions and in such a way that no overlappingwith particles already placed Finally at the mesoscale aggre-gate particles (typically sand or gravel) and the surroundingITZ layers behave as inclusions in the matrix phase of mortarmatrix
Figure 4 presents a typical schematic diagram of concretemesostructure generated by employing the above approachThe size of the heterogeneous concrete specimen is 150mm times
150mm Note that aggregate particles in real concrete arenot perfectly circular However the efforts in [10 11] haveindicated that the effect of aggregate shape on macroscopicstress-strain curve of concrete seems to be very smallSimilar to that in [11 34] the concrete sample contains 6medium stones with a diameter of 30mm and 56 small stoneswith a diameter of 12mm The concrete specimens involveabout 469 of aggregate per volume In Figure 4 the greenareas mean the aggregate phase the red thin-layer zonessurrounding the aggregate particles are the ITZs and the greyzones denote the mortar matrix Herein the interfacial zonesare viewed as uniform thickness shells placed concentricallyaround each aggregate Similar to the work [34] the thicknessof the ITZ was set as 1mm
To describe the influence of end friction confinement onthe dynamic compressive mechanical properties of concretetwo rigid blocks (see the two blue blocks in Figure 4) wereplaced respectively at the top and the bottom of the con-crete specimen The interactions between the heterogeneous
6 Shock and Vibration
y
x
AggregateITZ
Mortar matrixRigid block
Uniaxial compression
Unit mm End
fric
tion
25 25150
2525
150
Figure 4 Mesoscale mechanical model of concrete under dynamic uniaxial compression considering the influence of end frictionconfinement The specimen has 22346 elements [For interpretation of the references to color in this figure legend the reader is referredto the web version of this paper]
concrete specimen and the two rigid blocks that is the twored-line regions are implemented by the classic coulombfriction behavior The friction coefficients considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces ofthe specimen were fixed in the horizontal direction) fora quantitative assessment of the end friction confinementeffect As known the DIF difference obtained from thesimulation results with different friction coefficients canthen be attributed purely to the influence of end frictionconfinement effects
Themeshing of these concrete specimens were conductedwith four node solid elements with a linear strain field Tohave a better understanding of concrete fracture the averagemesh size was l mm which is consistent with that in the workfrom Hentz et al [23] and Du et al [11 12]
32 Mechanical Parameters for the Three MesocomponentsIn Zhou and Haorsquos [11 13] and Snozzi et alrsquos [35] workthe uniaxial tensile and compressive mechanical behaviorof concrete at high strain rate were studied From theirsimulation observations it can be noticed that no damagegenerates in the aggregate phaseMoreover in Pedersen et alrsquos[8] simulation of the dynamic tensile behavior of concretethe aggregate grains were assumed to follow a linear elasticmaterial behaviorThis is because the tensile and compressivestrengths of the aggregate are much larger than those of mor-tar matrix and the ITZs Similar to the work [8 11] the aggre-gate was assumed as elastic in the following simulationsThistreatment should work for the concrete subjected to mediumand low strain rates as discussed in the present study
To the mortar matrix and the ITZs the continuumdamage mechanics theories mentioned previously wereemployed to describe their mechanical properties In contin-uum mechanics the constitutive model is often expressed in
terms of stress-strain relations When the material exhibitsstrain-softening behavior leading to the strain localizationbehavior this formulation leads to a strongmesh dependencyof the finite element results in which the energy dissipateddecreases upon mesh refinement [11 19] Similar to the workin [10 11 19] to avoid or release unreasonable mesh sensitiveresults the tensile postfailure behavior was given in terms ofa fracture energy cracking criterion by specifying a stress-displacement curve instead of a stress-strain curve In addi-tion unlike discrete crack models [36 37] the continuumdamaged plasticity model based on continuum mechanicsuses damage factors such asDAMAGEC for compression andDAMAGET for tension to describe the fracture behavior andit is not capable of providing accurate crack geometry such ascrack width
The main mechanical parameters including the elasticmodulus Poissonrsquos ratio and uniaxial tensilecompressivestrengths of the three mesoconstituents used in this study forthe following numerical analysis were listed in Table 1
It is to be noted that the DIFs given in Section 22 are builtbased on the test results on concrete material The strain rateeffects for the aggregate phase mortar matrix and the ITZare essentially distinct as illustrated in [38 39] NeverthelessGrote et alrsquos [21] experimental observations indicate that thedynamic mechanical behavior of mortar matrix is closelysimilar to that of concrete In addition the ITZ layer can betreated as a kind of mortar matrix with a high(er) porosity[34] and thus its dynamic mechanical behavior can also beregarded as similar to those of mortar matrix and concreteIn summary it is assumed that the ITZ and the mortarmatrix have the same DIFs mentioned previously The treat-ments are consistent with the ones in [9 10] The strainrate effect for both the mortar matrix and the ITZs ontheir tensilecompressive strengths was incorporated intothe plasticity damaged model which was represented by
Shock and Vibration 7
Table 1 Mechanical parameters of the concrete mesocomponentsused in the study
Mortar matrix ITZ AggregateMass density 120588 [kgm3] 275 times 103 275 times 103 288 times 103
Elastic modulus [GPa] 30lowast
25lowast
70lowast
Poissonrsquos ratio 02lowast
022lowast
016lowast
Dilation angle 120595 [∘] 30 30Eccentricity 120578 01 01Shape factor 119870
1198880667 0667
Stress ratio 120590119888119888120590119888
116 116Tensile yield stress 120590
119905[MPa] 143
lowast12lowast
Compressive yield stress 1205901198880
[MPa] 143lowast
12lowast
Ultimate compressive yieldstress 120590cu [MPa] 143 12
Note data with ldquolowastrdquo are quoted from Du et al [12]
a dynamic increase factor (ie the DIF) with respect to strainrate
33 BoundaryLoading Conditions and FE Simulations Toexamine the effects of end friction confinement on themacromechanical behavior of concrete subjected to dynamiccompressive loadings the failure behavior of the concretespecimen was explored The corresponding loading andboundary conditions for the interaction system were illus-trated as follows (1) constant vertical velocity V was appliedon the top surface of the rigid block and the left and rightsides of the specimen are free of stress (2) the movementat the bottom rigid block was fixed at both the vertical andhorizontal directions (3) friction behavior between the twoblocks and the concrete sample was set The nominal strainrate 120576 is defined as the applied velocity divided by the heightof the specimen that is 120576 = Vℎ where ℎ is the height of thespecimen
In the following simulations ABAQUS increased auto-matically the size of step time going from smaller one to themaximumauthorized defined by the user For all the concretespecimens the numerical simulations were performed in aplane strain condition
34 Verification of the Mesoscale Approach In reality theavailable tests on loading rate effect of concrete are not veryrich and the test data is also not complete Comparativelyspeaking Dilger et alrsquos [14] test data is the most completeone and it is often used to verify the reliability of the analysismethod or model such as in [26]
To illustrate the reliability and accuracy of the presentmesoscale simulation method Dilger et alrsquos [14] test on thedynamic uniaxial compressive behavior of concrete was alsoselected for the comparison in this section In Dilger et alrsquos[14] experiment the macroscopic mechanical behavior ofconcrete under different nominal strain rates (ie the strainrates of 333 times 10minus5 sminus1 333 times 10minus3 sminus1 and 02 sminus1) was
explored and the complete compressive stress-strain curvesof concrete were obtained
In the previouswork [33] a series of dynamic compressivetest of concrete under different strain rates were conductedbased on the present mesoscale mechanical method includ-ing 120576 = 333 times 10minus5 sminus1 1 times 10minus4 sminus1 333 times 10minus3 sminus1 1 times 10minus2 sminus15 times 10minus2 sminus1 02 sminus1 1 sminus1 100 sminus1 and 200 sminus1 It is to benoted that in the simulations the concrete specimens werefixed at one end and loaded longitudinally through an appliedconstant velocity at the other end The detailed mechanicalparameters and analysis method can refer to [33]
Figure 5 presents the failure patterns of the concretespecimen subjected to different nominal strain rates Onecan notice that with the increase of strain rate the numberof cracks (ie the red damaged region) increases obviouslyand the crack branching behavior occurs Therefore withthe increase of strain rate the fracture of concrete requiresmore energy demand to reach failure which should be themain reason for the improvement of the dynamic strength ofconcrete
Figure 6(a) reports the comparison between the sim-ulations results (solid curves) and the experimental data(symbols) in terms of nominal stress (applied forces dividedby the specimen cross sectional area) versus nominal strain(the displacement generated at the applied-load end dividedby the length of the specimen) curves and the agreementis very good It should be noted herein that as mentionedpreviously the relatedmechanical and physical parameters ofthe concrete mixture used in the test are not full especiallythe mechanical parameters of the ITZ Accordingly in thepreviouswork [33] themechanical parameters (especially theelasticmodulus and the strength) of the ITZwere determinedby the inversion method on the basis of only two strainrates (333 times 10minus5 sminus1 and 333 times 10minus3 sminus1) The simulationof the third available strain (ie 02 sminus1) can be regarded asa validation of the ability of the model to predict concretestrength outside the range of strain rates used for calibrationThis treatment is similar to that in [26]
Furthermore the compressive DIFs were evaluatedaccording to the simulation results and the comparison of thepresent simulation results and some available experimentalobservations is plotted in Figure 6(b) It can be observedthat the present simulation results agree very well with thecollective experimental data This indicates that the presentanalysis method can well simulate the dynamic compressivebehavior of concrete The validated mesoscale mechanicalapproach would be employed in the following simulations tostudy the effect of end friction confinement on the dynamiccompressive behavior of concrete
4 Dynamic Compressive FailureBehavior of Concrete
On the basis of the mesoscale mechanical model describedin Section 3 the simulations of the dynamic axial com-pression of the concrete specimen with various end fric-tion coefficients were implemented The loading velocitiesadopted on the upper rigid block in the simulations are
8 Shock and Vibration
10Damage
120576 = 333 times 10minus5 120576 = 1 times 10minus4 120576 = 333 times 10minus3 120576 = 1 times 10minus2 120576 = 5 times 10minus2
120576 = 2 times 10minus1 120576 = 1 120576 = 100 120576 = 200
Figure 5 Compressive failure patterns of the concrete specimen under different strain rates ranging from 1 times 10minus5 sminus1 to 200 sminus1
Compression test(Dilger et al 1984) and present model
Nom
inal
com
pres
sive
stre
ss (M
Pa)
0002 00030001 0004 0005 00060Compressive strain
0
10
20
30
40
120576 = 333 times 10minus5 sminus1
120576 = 333 times 10minus3 sminus1
120576 = 02 sminus1
(a)
001 1 100
09
12
15
18
21
24
Com
pres
sive D
IF
Test data Present method
1E minus 6 1E minus 4
Strain rate (sminus1)
(b)
Figure 6 (a) Comparison of the present simulation results and Dilger et alrsquos [14] test data and (b) compressive DIFs for the simulation resultsand some available test data
Shock and Vibration 9
Dynamic loading
0
2
4
6
8
10
12
14
Com
pres
sive
stre
ss (M
Pa)
120576 = 1 times 10minus1 sminus1
times10minus3
Mesh size 15mmMesh size 10mmMesh size 05mm
End friction coefficient 120583 = 06
1 432 5 6 70Strain 120576
(a)
Mesh size 15mmMesh size 10mmMesh size 05mm
Damage factor0 1
(b)
Figure 7 (a) The simulation results of three concrete specimens with the same distribution of aggregates and different mesh sizes and(b) damage distribution of the concrete specimens with different mesh sizes under the same strain rate and friction coefficients at theirpeak stresses
V = 15 times 10minus6ms 15 times 10minus4ms 15 times 10minus3ms 15 times
10minus25ms 15 times 10minus2ms 15 times 10minus15ms and 15 times 10minus1msin an ascending sequence and in every loading cycle the con-stant velocity was utilized The corresponding macroscopicnominal strain rates are 120576 = 1 times 10minus5 sminus1 (quasistatic) 1 times10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1and 1 times 100 sminus1 respectively Moreover as mentioned previ-ously the seven end friction coefficients 120583 considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces of thespecimenwere fixed in the horizontal direction) respectively
To check the mesh sensitivity in the simulations threedifferentmesh sizeswere utilized that is 05mm 10mm and
15mm Figure 7(a) presents the nominal compressive stress-strain curves of the concrete specimen subjected to a nominalstrain rate of 01 sminus1 with the same end friction coefficientand the three different mesh sizes It can be found clearlyfrom Figure 7(a) that the mesh sizes (ie 05mm 10mmand 15mm) have less influence on the stress-strain curvesThe three curves are also overlapped Figure 7(b) shows thedamage distribution of the three concrete specimens men-tioned above with the same distribution of aggregates Onecannotice that the failure patterns of the three specimenswithdifferent mesh sizes are closely similar to each other Conse-quently the mesh size of 15mm was used in the followingsimulations
10 Shock and Vibration
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
Equivalent plastic strain times10minus300 56
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
120576
120576
120576
120576
120576
Figure 8 Equivalent plastic strain distribution within the concrete specimen under different strain rates and end friction coefficients at theirpeak compressive stresses
41 Effects of Strain Rate and End Friction Confinement onFailure Patterns of Concrete Figure 8 presents the equivalentplastic strain distribution within the concrete specimensunder five groups of different strain rates ( 120576 = 1 times 10minus5 sminus11 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus1 sminus1 and 1 times 100 sminus1) and fourgroups of different friction coefficients (120583 = 0 03 08 andinfin) at their peak compressive stresses (ie the compressivestrength) One can note from Figures 8(a)ndash8(d) that for thespecimen with the same friction coefficient with the increase
of nominal strain rate the equivalent plastic strain withinconcrete increases obviously In addition as the frictioncoefficient 120583 increases from 0 to infin the equivalent plasticstrain within concrete at reaching the peak stress varies
For the specimenwith the friction coefficient of 0 and 03the obtained plastic strain distributions within the concretespecimens are obviously different For the one with the fric-tion coefficient of 03 and 08 the obtained plastic strain dis-tributions are slightly different And for that with the friction
Shock and Vibration 11
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
000 49
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Maximum principal stress (MPa)
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 9 Maximum principal stress distribution within the concrete specimen under different strain rates and end friction coefficients attheir peak compressive stresses
coefficient of 08 andinfin the obtained plastic strain distribu-tions are almost totally consistent That is to say when thefriction coefficient becomes larger than 08 the effect of endfriction confinement on the failure patterns of concrete canbe ignored
The maximum principal stress distributions within theconcrete specimens under the five groups of different strainrates and the four different friction coefficients at the peakcompressive stresses are presented in Figure 9 It can be
noted intuitively from Figure 9 that the changes of nominalstrain rate and friction coefficient have a significant influenceon the maximum principal stress distribution of the speci-menWith the increase of end friction coefficient the value ofmaximum principal stress gets large and the distribution areadraws close to central section from the top and bottom of theconcrete specimen respectively at same loading velocity
The damage (ie the cracks) distributions within theconcrete specimens corresponding to Figures 8 and 9 are
12 Shock and Vibration
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
0 1
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Damage factor
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 10 Damage distribution within the concrete specimens under different strain rates and friction coefficients at their peak stresses
presented in Figure 10 for different loading velocities anddifferent end friction coefficients In Figure 10 differentcolors represent different damage indexes The red colordenotes the most serious damage while the blue color meansthat no damage generates The white rounded areas whichare regarded as aggregates in these models have no damage
It can be noticed clearly from Figure 10 that the damagedareas increase with the growth of nominal strain rate Whenthe nominal strain rate is relatively low(er) (eg 1 times 10minus5 sminus1)the damaged area of the specimens is small when reaching
their peak stress Accordingly the damage regions (iecracks) are narrow and short and the number of cracks islimited As the nominal strain rate rises from 1times 10minus5 sminus1 to 1times100 sminus1 the damaged area and the number of cracks increasegradually When the nominal strain rate is relatively high(er)(eg 1 times 100 sminus1) a lot of areas are damaged in different levelsThe cracks widen and link together forming a crack networksimultaneously
Therefore it can be concluded that with the increase ofloading velocity the nominal strain rate increases gradually
Shock and Vibration 13
Table 2 Dynamic compressive strength of concrete under different end friction coefficients
120583Dynamic compressive strength [MPa]
1 times 10minus5 sminus1 1 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1 1 times 100 sminus1
0 793 806 858 919 1042 1197 153901 829 838 906 977 1113 1297 161202 846 857 926 1007 1137 1349 168203 849 864 939 1016 1167 1355 169606 857 877 955 1036 1175 1382 173608 860 881 962 1042 1185 1391 1745infin 875 892 980 1067 1212 1406 1749
and the number of cracks or damaged zones increases whenthe apparent compressive strength of concrete is reachedTheenergy consumption of the loading process increases corre-spondinglyThis should be the major reason for the improve-ment of dynamic compressive strength of concrete materials
It can be found obviously from the comparison amongFigures 10(a)ndash10(d) that the damage states of concrete spec-imens are diverse at their peak stresses for different endfriction conditions
Compared with the concrete specimen without end fric-tion confinement (ie 120583 = 0) the deformation at the end ofthe specimen considering the effect of end friction (ie120583 gt 0)was obviously hindered In addition with the increase of endfriction coefficient the obstruction degree of deformationraises For the specimen with the two ends completely fixed(ie 120583 = infin) there is no horizontal deformation at the endsmaking the confinement effect very strong
From Figure 10 one can note that a larger end frictioncoefficient leads to a lower damage level in the top and bottomof the specimen with a constant nominal strain rate Forlarger end friction coefficient the damaged areas draw closeto the central section from the top and bottom of the concretespecimenThese phenomena should generate due to the effectof the end friction confinement which changes the uniaxialloading state in the local regions of concrete These can alsobe illustrated from the simulation results in Figures 8 and 9
42 Effect of End Friction Confinement on Dynamic Compres-sive Strength The macroscopic nominal compressive stress-strain curves of the concrete specimen under different strainrates and end friction coefficients are plotted and compared inFigure 11 Moreover the corresponding peak stresses that isthe nominal dynamic compressive strengths of concrete arereported in Table 2 Obviously both the stress-strain curvesof concrete in Figure 11 and the axial dynamic compressivestrengths in Table 2 demonstrate the effects of strain rates andend friction coefficients
It can be noted obviously from Figure 11 and Table 2 thatthe dynamic uniaxial compressive strength of concrete isimproved due to the end friction confinement effect Further-more under the same strain rates the ascending curves of theconcrete sample with various friction coefficients are almostoverlapped indicating that the elastic modulus of concreteis almost not influenced by the end friction confinementeffect The obtained compressive strengths and the softening
curves are distinct significantly because the stresses andstrains status as well as the fracture paths within the concretespecimen for different friction coefficients vary
For various strain rates the quantitative relationshipsbetween the obtained dynamic compressive strengths of theconcrete specimen and end friction coefficient are presentedin Figures 12(a) and 12(b) It can be seen clearly fromFigure 12 that the concrete dynamic compressive strengthincreases with the increase of end friction coefficient Whenthe end friction coefficient 120583 grows from 0 to 03 the uniaxialcompressive strength increases rapidly while the uniaxialdynamic compressive strength increases slightly and thengets to be stable when the end friction coefficient exceeds 03This is to say when the end friction coefficient exceeds 03 theend confinement effect on the dynamic compressivemechan-ical behavior of concrete can be ignored This can also beconcluded from the analysis resultsmentioned previously forexample the damage factor distribution of concrete pre-sented in Figure 10
Furthermore the results about the effect of end frictionconfinement on concrete dynamic compressive strength atmedium and low strain rates are similar to those at high strainrate For more information about the end confinement effectfor high strain rate refer to Li et al [40]
Figure 13 presents the damage distribution within theconcrete specimens at their corresponding peak stressesunder different end friction confinement conditions at thesame loading velocities Figure 13(a) shows the results for theloading condition of a relative lower strain rate that is 120576 = 1 times10minus2 sminus1 One can note that for ldquopurerdquo uniaxial compressivebehavior of concrete (ie the end friction 120583 between theconcrete specimen and the rigid block is zero 120583 = 0) thenumber of cracks generated or the damage degree withinthe specimen is very limited when reaching the compressivestrength of the concrete sample With the increase of endfriction coefficient for example 120583 = 01 and 02 the totalnumber of cracks ascends gradually but the number of cracksnear the top and bottom regions of the specimen descendsWhen the end friction coefficient becomes larger than 03(eg 120583 = 03 06 08 and infin) the number of cracks turnsto be stable but the width of the cracks broadens as can beseen in Figure 13(a)
Figure 13(b) shows the simulation results for the loadingcondition of a relative higher strain rate that is 120576 = 1 times10minus05 sminus1 For ldquopurerdquo uniaxial compression (ie the end
14 Shock and Vibration
7252015
9
Quasistatic loading
8
95
85
752515
Dynamic loading
20
Dynamic loading
20
10
9
8
25 30 35302520
11
10
9
8
Dynamic loading
Dynamic loading Dynamic loading= 1 times 10minus1 sminus1
= 1 times 10minus3 sminus1
= 1 times 10minus2 sminus1
= 1 times 10minus5 sminus1
times10minus3
0
3
6
9
12
15
18C
ompr
essiv
e st
ress
(MPa
)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
= 1 times 10minus15 sminus1
= 1 times 10minus05 sminus1
120576
120576
120576
120576
120576
120576
Figure 11 Continued
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
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Shock and Vibration
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4 Shock and Vibration
Uniaxial compression
Uniaxial tension
Biaxial tension
Biaxial compression 120590c
120590t
(120590cc 120590cc)
1205901
1205902
Figure 2 Yield surface for plane stress conditions
1205901
1205902
1205903
Kc = 1
Kc = 23
Figure 3 Yield surfaces in the deviatory plane [119870119888
= 23
corresponds to Rankine formulation and119870119888= 1 corresponds to the
Drucker-Prager criterion]
Moreover parameters of 120572 120573(120576pl) and 120574 respectively canbe calculated by
120572 =120590119888119888120590119888minus 1
2120590119888119888120590119888minus 1
(7a)
120573 (120576pl) =
120590119888(120576
pl119888)
120590119905(120576
pl119905)
(1 minus 120572) minus (1 + 120572) (7b)
120574 =3 (1 minus 119870
119888)
2119870119888minus 1
(7c)
in which 120590119888119888120590119888means the ratio of initial equivalent-biaxial
compressive yield stress to initial uniaxial compressive yieldstress and its default value of the ratio is 116 according to[19 20] 119870
119888is the ratio of the tensile to the compressive
meridian and defines the shape of the yield surface in thedeviatory plane (see Figure 3)
213 Plastic Flow Rule The nonassociated potential plasticflow is employed in the present damaged plasticity modelThe flow potential function 119866(120590) used for this model is
the nonassociatedDrucker-Prager hyperbolic function and isdefined according to
119866 (120590) = radic(120578120590119905tan120595)2 + 1199022 minus 119901 tan120595 (8)
in which 120595 is the dilation angle measured in the 119901-119902 planeat high confining pressure 120590
119905is the uniaxial tensile stress at
failure 120578 is the eccentricity that gives the rate at which theplastic potential function approximates the asymptote (theflow potential tends to a straight line as the eccentricity tendsto zero) and its default value is equal to 01Thenonassociatedflow rule means that the plastic strain vector is normal to theplastic potential function that differs from the yield surface
The plastic strain rate 120576pl and the effective plastic strain
rate 120576pl can be derived as follows
120576pl=
120597119866
120597120590(9a)
120576pl= ℎ (120590 120576
pl) sdot 120576
pl (9b)
where is the plastic multiplierBecause the selected plastic flow is nonassociated to
obtain an acceptable rate of convergence the unsymmetricmatrix storage and solution scheme is used For more detailsabout the constitutive model refer to Lubliner et al [15] Leeand Fenves [16] and Du et al [11]
22 Dynamic Increase Factor (DIF) for Concrete The avail-able experimental and numerical observations have demon-strated that concrete and other cementitiousmaterials are ratesensitive [3 21 22] The strain rate effect has been studiedon different mechanical characteristics of concrete Youngrsquosmodulus Poissonrsquos ratio energy-absorption capacity andaxial strain atmaximumstrength are rate-sensitive quantitiesbut at amuch lower intensity than the compressive and tensilestrengths [3 23] Similar to the work [4 11] only the strengthenhancement was considered in the present study
So far many empirical and theoretical relations have beendeveloped to quantitatively describe the strain rate effect onconcrete properties In particular the code by the ComiteEuro-international du Beton (CEB) recommends variousvalues of the DIF for the tensile and compressive strengthsunder different strain rates based on the available test resultsThe formula of the compressive DIF recommended by CEB[3] has the following form
CDIF =119891cd119891cs
= (120576119889
120576cs)
1026120572
for 120576119889le 30 sminus1 (10a)
CDIF =119891cd119891cs
= 120574 ( 120576119889)13 for 120576
119889gt 30 sminus1 (10b)
where 119891cd is the dynamic compressive strength at the strainrate of 120576
119889(in the range of 30 times 10minus6ndash1000 sminus1) 120576cs = 30 times
10minus6 sminus1 (static strain rate) log 120574 = 6156120572 minus 049 120572 = (5 +
3119891cu4)minus1 119891cs is the static compressive strength and 119891cu is
the static cube compressive strength [in MPa] The DIF for
Shock and Vibration 5
the compressive strength in (10a) and (10b) was oftenadopted for example in the publications [10 11]
The CEB also gives empirical formulae to estimate theDIF for concrete tensile strength However comparisonbetween the available experimental results in the literaturewith the CEB empirical equations indicates that the CEBtensile DIF substantially underestimates the tensile DIF ofconcrete [24 25] In Malvar and Rossrsquos [24] work an empiri-cal formula was proposed and the formula for the tensile DIFcan be written as
TDIF =119891td119891ts
= (120576119889
120576ts)
120575
for 120576119889le 1 sminus1 (11a)
TDIF =119891td119891ts
= 120573(120576119889
120576ts)
13
for 120576119889gt 1 sminus1 (11b)
where 119891td and 119891ts are respectively the dynamic uniaxial ten-sile strength at the strain rate 120576
119889and the quasistatic uniaxial
tensile strength 120576ts = 10minus6 sminus1 (static strain rate) log120573 = 6120575minus2
120575 = 1(1 + 81198911015840
1198881198911015840
1198880) 11989110158401198880= 10MPa and 119891
1015840
119888is the quasistatic
uniaxial compressive strength of concrete (in MPa)
3 Mesoscale ComputationalModel for Concrete
Theoretical experimental and numerical studies indicatethat the failure pattern crack mode and even the velocity ofthe crack propagation are influenced by loading rate [11 26ndash28] The mechanical behaviors of concrete including themacroscopic mechanical properties and the failure patternsare associated with the micro-mesostructure of concreteDue to the complexity of concrete the failure behavior can bestudied numerically In the numerical simulations concreteheterogeneity should be accounted for and thus it requiresthe adoption of a mesoscale mechanical model in which theheterogeneity can be explicitly described
At themesoscale concretewas often assumed to be amul-tiphase composite composed of aggregate mortar matrix theinterfacial transition zones [ITZs] voids and so forth A lot ofwork [9 10 19 29] has demonstrated that the ITZs have a dra-matic influence on the failure pattern and the macromechan-ical properties of concrete However the mechanical proper-ties especially the dynamic mechanical behavior of the ITZsare not well understood yet [13 19 30ndash32] Moreover thereal typical thickness of ITZ is about 10ndash50120583m [9 10] whichlimits the minimum size of the finite element mesh In mostsimulation efforts the ITZ thickness is set as 02ndash08mm[9 10] 05mm [8] 04mm [19] and 1mm [12] for the sake ofsimplicity
31 Mesostructure and Mechanical Model of Concrete Con-crete exhibits heterogeneity in material and mechanicalproperties onmany length scales [29] At the mesoscale con-sidering the effect of heterogeneities of concrete the concretein the present work was regarded as a three-phase compositecomposed of coarse aggregate particles mortar matrix andthe ITZs between the former two phases Random aggregatemodels have long been demonstrated to be an effective
mesomechanical approach to simulating the failure processand the deformation of concrete and they have been widelyutilized in fracturemechanics of concrete for example in [11ndash13 33] Based on the concrete random aggregate model inwhich the shape size and distribution of the coarse aggregateparticles closely resemble real concrete in the statistical senselots of efforts have been carried out to investigate the macro-scopic mechanical behavior and failure mechanism of con-crete [10ndash12 29] In this work the concrete random aggregatemodel was therefore also employed
Due to great computational expense and memorydemand of mesoscale simulations it is in general notpossible to model the full structure at the mesoscale with thecomputational power available nowadays Herein the presentstudy only two-dimensional simulations were thus con-ducted Similar to the work [9ndash12 33] the aggregate particlesare modeled as circles with random spatial distributionenfolded by a thin interface layer of ITZ Similar to those in[11 12] the ldquotake-and-placerdquo method was utilized to generatethe coarse aggregate particles The fine ones and othercomponents (eg air voids) were assumed to be mixed upwith the cement paste establishing the mortar matrix phaseThis matrix phase can thus be regarded as a homogeneouscomponent at the mesoscale The material properties of thepaste phase are thus strongly dependent on the type of cementused amount of pores water to cement ratio and otheradditives present in the concrete which can be determinedby microscale simulation efforts Furthermore the Fullercurve widely utilized for example in [11 12] was selected todetermine the distribution of aggregate with different sizesemployed in the concrete specimen The aggregate particleswere then placed into the matrix one by one at randomlydetermined positions and in such a way that no overlappingwith particles already placed Finally at the mesoscale aggre-gate particles (typically sand or gravel) and the surroundingITZ layers behave as inclusions in the matrix phase of mortarmatrix
Figure 4 presents a typical schematic diagram of concretemesostructure generated by employing the above approachThe size of the heterogeneous concrete specimen is 150mm times
150mm Note that aggregate particles in real concrete arenot perfectly circular However the efforts in [10 11] haveindicated that the effect of aggregate shape on macroscopicstress-strain curve of concrete seems to be very smallSimilar to that in [11 34] the concrete sample contains 6medium stones with a diameter of 30mm and 56 small stoneswith a diameter of 12mm The concrete specimens involveabout 469 of aggregate per volume In Figure 4 the greenareas mean the aggregate phase the red thin-layer zonessurrounding the aggregate particles are the ITZs and the greyzones denote the mortar matrix Herein the interfacial zonesare viewed as uniform thickness shells placed concentricallyaround each aggregate Similar to the work [34] the thicknessof the ITZ was set as 1mm
To describe the influence of end friction confinement onthe dynamic compressive mechanical properties of concretetwo rigid blocks (see the two blue blocks in Figure 4) wereplaced respectively at the top and the bottom of the con-crete specimen The interactions between the heterogeneous
6 Shock and Vibration
y
x
AggregateITZ
Mortar matrixRigid block
Uniaxial compression
Unit mm End
fric
tion
25 25150
2525
150
Figure 4 Mesoscale mechanical model of concrete under dynamic uniaxial compression considering the influence of end frictionconfinement The specimen has 22346 elements [For interpretation of the references to color in this figure legend the reader is referredto the web version of this paper]
concrete specimen and the two rigid blocks that is the twored-line regions are implemented by the classic coulombfriction behavior The friction coefficients considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces ofthe specimen were fixed in the horizontal direction) fora quantitative assessment of the end friction confinementeffect As known the DIF difference obtained from thesimulation results with different friction coefficients canthen be attributed purely to the influence of end frictionconfinement effects
Themeshing of these concrete specimens were conductedwith four node solid elements with a linear strain field Tohave a better understanding of concrete fracture the averagemesh size was l mm which is consistent with that in the workfrom Hentz et al [23] and Du et al [11 12]
32 Mechanical Parameters for the Three MesocomponentsIn Zhou and Haorsquos [11 13] and Snozzi et alrsquos [35] workthe uniaxial tensile and compressive mechanical behaviorof concrete at high strain rate were studied From theirsimulation observations it can be noticed that no damagegenerates in the aggregate phaseMoreover in Pedersen et alrsquos[8] simulation of the dynamic tensile behavior of concretethe aggregate grains were assumed to follow a linear elasticmaterial behaviorThis is because the tensile and compressivestrengths of the aggregate are much larger than those of mor-tar matrix and the ITZs Similar to the work [8 11] the aggre-gate was assumed as elastic in the following simulationsThistreatment should work for the concrete subjected to mediumand low strain rates as discussed in the present study
To the mortar matrix and the ITZs the continuumdamage mechanics theories mentioned previously wereemployed to describe their mechanical properties In contin-uum mechanics the constitutive model is often expressed in
terms of stress-strain relations When the material exhibitsstrain-softening behavior leading to the strain localizationbehavior this formulation leads to a strongmesh dependencyof the finite element results in which the energy dissipateddecreases upon mesh refinement [11 19] Similar to the workin [10 11 19] to avoid or release unreasonable mesh sensitiveresults the tensile postfailure behavior was given in terms ofa fracture energy cracking criterion by specifying a stress-displacement curve instead of a stress-strain curve In addi-tion unlike discrete crack models [36 37] the continuumdamaged plasticity model based on continuum mechanicsuses damage factors such asDAMAGEC for compression andDAMAGET for tension to describe the fracture behavior andit is not capable of providing accurate crack geometry such ascrack width
The main mechanical parameters including the elasticmodulus Poissonrsquos ratio and uniaxial tensilecompressivestrengths of the three mesoconstituents used in this study forthe following numerical analysis were listed in Table 1
It is to be noted that the DIFs given in Section 22 are builtbased on the test results on concrete material The strain rateeffects for the aggregate phase mortar matrix and the ITZare essentially distinct as illustrated in [38 39] NeverthelessGrote et alrsquos [21] experimental observations indicate that thedynamic mechanical behavior of mortar matrix is closelysimilar to that of concrete In addition the ITZ layer can betreated as a kind of mortar matrix with a high(er) porosity[34] and thus its dynamic mechanical behavior can also beregarded as similar to those of mortar matrix and concreteIn summary it is assumed that the ITZ and the mortarmatrix have the same DIFs mentioned previously The treat-ments are consistent with the ones in [9 10] The strainrate effect for both the mortar matrix and the ITZs ontheir tensilecompressive strengths was incorporated intothe plasticity damaged model which was represented by
Shock and Vibration 7
Table 1 Mechanical parameters of the concrete mesocomponentsused in the study
Mortar matrix ITZ AggregateMass density 120588 [kgm3] 275 times 103 275 times 103 288 times 103
Elastic modulus [GPa] 30lowast
25lowast
70lowast
Poissonrsquos ratio 02lowast
022lowast
016lowast
Dilation angle 120595 [∘] 30 30Eccentricity 120578 01 01Shape factor 119870
1198880667 0667
Stress ratio 120590119888119888120590119888
116 116Tensile yield stress 120590
119905[MPa] 143
lowast12lowast
Compressive yield stress 1205901198880
[MPa] 143lowast
12lowast
Ultimate compressive yieldstress 120590cu [MPa] 143 12
Note data with ldquolowastrdquo are quoted from Du et al [12]
a dynamic increase factor (ie the DIF) with respect to strainrate
33 BoundaryLoading Conditions and FE Simulations Toexamine the effects of end friction confinement on themacromechanical behavior of concrete subjected to dynamiccompressive loadings the failure behavior of the concretespecimen was explored The corresponding loading andboundary conditions for the interaction system were illus-trated as follows (1) constant vertical velocity V was appliedon the top surface of the rigid block and the left and rightsides of the specimen are free of stress (2) the movementat the bottom rigid block was fixed at both the vertical andhorizontal directions (3) friction behavior between the twoblocks and the concrete sample was set The nominal strainrate 120576 is defined as the applied velocity divided by the heightof the specimen that is 120576 = Vℎ where ℎ is the height of thespecimen
In the following simulations ABAQUS increased auto-matically the size of step time going from smaller one to themaximumauthorized defined by the user For all the concretespecimens the numerical simulations were performed in aplane strain condition
34 Verification of the Mesoscale Approach In reality theavailable tests on loading rate effect of concrete are not veryrich and the test data is also not complete Comparativelyspeaking Dilger et alrsquos [14] test data is the most completeone and it is often used to verify the reliability of the analysismethod or model such as in [26]
To illustrate the reliability and accuracy of the presentmesoscale simulation method Dilger et alrsquos [14] test on thedynamic uniaxial compressive behavior of concrete was alsoselected for the comparison in this section In Dilger et alrsquos[14] experiment the macroscopic mechanical behavior ofconcrete under different nominal strain rates (ie the strainrates of 333 times 10minus5 sminus1 333 times 10minus3 sminus1 and 02 sminus1) was
explored and the complete compressive stress-strain curvesof concrete were obtained
In the previouswork [33] a series of dynamic compressivetest of concrete under different strain rates were conductedbased on the present mesoscale mechanical method includ-ing 120576 = 333 times 10minus5 sminus1 1 times 10minus4 sminus1 333 times 10minus3 sminus1 1 times 10minus2 sminus15 times 10minus2 sminus1 02 sminus1 1 sminus1 100 sminus1 and 200 sminus1 It is to benoted that in the simulations the concrete specimens werefixed at one end and loaded longitudinally through an appliedconstant velocity at the other end The detailed mechanicalparameters and analysis method can refer to [33]
Figure 5 presents the failure patterns of the concretespecimen subjected to different nominal strain rates Onecan notice that with the increase of strain rate the numberof cracks (ie the red damaged region) increases obviouslyand the crack branching behavior occurs Therefore withthe increase of strain rate the fracture of concrete requiresmore energy demand to reach failure which should be themain reason for the improvement of the dynamic strength ofconcrete
Figure 6(a) reports the comparison between the sim-ulations results (solid curves) and the experimental data(symbols) in terms of nominal stress (applied forces dividedby the specimen cross sectional area) versus nominal strain(the displacement generated at the applied-load end dividedby the length of the specimen) curves and the agreementis very good It should be noted herein that as mentionedpreviously the relatedmechanical and physical parameters ofthe concrete mixture used in the test are not full especiallythe mechanical parameters of the ITZ Accordingly in thepreviouswork [33] themechanical parameters (especially theelasticmodulus and the strength) of the ITZwere determinedby the inversion method on the basis of only two strainrates (333 times 10minus5 sminus1 and 333 times 10minus3 sminus1) The simulationof the third available strain (ie 02 sminus1) can be regarded asa validation of the ability of the model to predict concretestrength outside the range of strain rates used for calibrationThis treatment is similar to that in [26]
Furthermore the compressive DIFs were evaluatedaccording to the simulation results and the comparison of thepresent simulation results and some available experimentalobservations is plotted in Figure 6(b) It can be observedthat the present simulation results agree very well with thecollective experimental data This indicates that the presentanalysis method can well simulate the dynamic compressivebehavior of concrete The validated mesoscale mechanicalapproach would be employed in the following simulations tostudy the effect of end friction confinement on the dynamiccompressive behavior of concrete
4 Dynamic Compressive FailureBehavior of Concrete
On the basis of the mesoscale mechanical model describedin Section 3 the simulations of the dynamic axial com-pression of the concrete specimen with various end fric-tion coefficients were implemented The loading velocitiesadopted on the upper rigid block in the simulations are
8 Shock and Vibration
10Damage
120576 = 333 times 10minus5 120576 = 1 times 10minus4 120576 = 333 times 10minus3 120576 = 1 times 10minus2 120576 = 5 times 10minus2
120576 = 2 times 10minus1 120576 = 1 120576 = 100 120576 = 200
Figure 5 Compressive failure patterns of the concrete specimen under different strain rates ranging from 1 times 10minus5 sminus1 to 200 sminus1
Compression test(Dilger et al 1984) and present model
Nom
inal
com
pres
sive
stre
ss (M
Pa)
0002 00030001 0004 0005 00060Compressive strain
0
10
20
30
40
120576 = 333 times 10minus5 sminus1
120576 = 333 times 10minus3 sminus1
120576 = 02 sminus1
(a)
001 1 100
09
12
15
18
21
24
Com
pres
sive D
IF
Test data Present method
1E minus 6 1E minus 4
Strain rate (sminus1)
(b)
Figure 6 (a) Comparison of the present simulation results and Dilger et alrsquos [14] test data and (b) compressive DIFs for the simulation resultsand some available test data
Shock and Vibration 9
Dynamic loading
0
2
4
6
8
10
12
14
Com
pres
sive
stre
ss (M
Pa)
120576 = 1 times 10minus1 sminus1
times10minus3
Mesh size 15mmMesh size 10mmMesh size 05mm
End friction coefficient 120583 = 06
1 432 5 6 70Strain 120576
(a)
Mesh size 15mmMesh size 10mmMesh size 05mm
Damage factor0 1
(b)
Figure 7 (a) The simulation results of three concrete specimens with the same distribution of aggregates and different mesh sizes and(b) damage distribution of the concrete specimens with different mesh sizes under the same strain rate and friction coefficients at theirpeak stresses
V = 15 times 10minus6ms 15 times 10minus4ms 15 times 10minus3ms 15 times
10minus25ms 15 times 10minus2ms 15 times 10minus15ms and 15 times 10minus1msin an ascending sequence and in every loading cycle the con-stant velocity was utilized The corresponding macroscopicnominal strain rates are 120576 = 1 times 10minus5 sminus1 (quasistatic) 1 times10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1and 1 times 100 sminus1 respectively Moreover as mentioned previ-ously the seven end friction coefficients 120583 considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces of thespecimenwere fixed in the horizontal direction) respectively
To check the mesh sensitivity in the simulations threedifferentmesh sizeswere utilized that is 05mm 10mm and
15mm Figure 7(a) presents the nominal compressive stress-strain curves of the concrete specimen subjected to a nominalstrain rate of 01 sminus1 with the same end friction coefficientand the three different mesh sizes It can be found clearlyfrom Figure 7(a) that the mesh sizes (ie 05mm 10mmand 15mm) have less influence on the stress-strain curvesThe three curves are also overlapped Figure 7(b) shows thedamage distribution of the three concrete specimens men-tioned above with the same distribution of aggregates Onecannotice that the failure patterns of the three specimenswithdifferent mesh sizes are closely similar to each other Conse-quently the mesh size of 15mm was used in the followingsimulations
10 Shock and Vibration
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
Equivalent plastic strain times10minus300 56
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
120576
120576
120576
120576
120576
Figure 8 Equivalent plastic strain distribution within the concrete specimen under different strain rates and end friction coefficients at theirpeak compressive stresses
41 Effects of Strain Rate and End Friction Confinement onFailure Patterns of Concrete Figure 8 presents the equivalentplastic strain distribution within the concrete specimensunder five groups of different strain rates ( 120576 = 1 times 10minus5 sminus11 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus1 sminus1 and 1 times 100 sminus1) and fourgroups of different friction coefficients (120583 = 0 03 08 andinfin) at their peak compressive stresses (ie the compressivestrength) One can note from Figures 8(a)ndash8(d) that for thespecimen with the same friction coefficient with the increase
of nominal strain rate the equivalent plastic strain withinconcrete increases obviously In addition as the frictioncoefficient 120583 increases from 0 to infin the equivalent plasticstrain within concrete at reaching the peak stress varies
For the specimenwith the friction coefficient of 0 and 03the obtained plastic strain distributions within the concretespecimens are obviously different For the one with the fric-tion coefficient of 03 and 08 the obtained plastic strain dis-tributions are slightly different And for that with the friction
Shock and Vibration 11
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
000 49
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Maximum principal stress (MPa)
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 9 Maximum principal stress distribution within the concrete specimen under different strain rates and end friction coefficients attheir peak compressive stresses
coefficient of 08 andinfin the obtained plastic strain distribu-tions are almost totally consistent That is to say when thefriction coefficient becomes larger than 08 the effect of endfriction confinement on the failure patterns of concrete canbe ignored
The maximum principal stress distributions within theconcrete specimens under the five groups of different strainrates and the four different friction coefficients at the peakcompressive stresses are presented in Figure 9 It can be
noted intuitively from Figure 9 that the changes of nominalstrain rate and friction coefficient have a significant influenceon the maximum principal stress distribution of the speci-menWith the increase of end friction coefficient the value ofmaximum principal stress gets large and the distribution areadraws close to central section from the top and bottom of theconcrete specimen respectively at same loading velocity
The damage (ie the cracks) distributions within theconcrete specimens corresponding to Figures 8 and 9 are
12 Shock and Vibration
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
0 1
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Damage factor
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 10 Damage distribution within the concrete specimens under different strain rates and friction coefficients at their peak stresses
presented in Figure 10 for different loading velocities anddifferent end friction coefficients In Figure 10 differentcolors represent different damage indexes The red colordenotes the most serious damage while the blue color meansthat no damage generates The white rounded areas whichare regarded as aggregates in these models have no damage
It can be noticed clearly from Figure 10 that the damagedareas increase with the growth of nominal strain rate Whenthe nominal strain rate is relatively low(er) (eg 1 times 10minus5 sminus1)the damaged area of the specimens is small when reaching
their peak stress Accordingly the damage regions (iecracks) are narrow and short and the number of cracks islimited As the nominal strain rate rises from 1times 10minus5 sminus1 to 1times100 sminus1 the damaged area and the number of cracks increasegradually When the nominal strain rate is relatively high(er)(eg 1 times 100 sminus1) a lot of areas are damaged in different levelsThe cracks widen and link together forming a crack networksimultaneously
Therefore it can be concluded that with the increase ofloading velocity the nominal strain rate increases gradually
Shock and Vibration 13
Table 2 Dynamic compressive strength of concrete under different end friction coefficients
120583Dynamic compressive strength [MPa]
1 times 10minus5 sminus1 1 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1 1 times 100 sminus1
0 793 806 858 919 1042 1197 153901 829 838 906 977 1113 1297 161202 846 857 926 1007 1137 1349 168203 849 864 939 1016 1167 1355 169606 857 877 955 1036 1175 1382 173608 860 881 962 1042 1185 1391 1745infin 875 892 980 1067 1212 1406 1749
and the number of cracks or damaged zones increases whenthe apparent compressive strength of concrete is reachedTheenergy consumption of the loading process increases corre-spondinglyThis should be the major reason for the improve-ment of dynamic compressive strength of concrete materials
It can be found obviously from the comparison amongFigures 10(a)ndash10(d) that the damage states of concrete spec-imens are diverse at their peak stresses for different endfriction conditions
Compared with the concrete specimen without end fric-tion confinement (ie 120583 = 0) the deformation at the end ofthe specimen considering the effect of end friction (ie120583 gt 0)was obviously hindered In addition with the increase of endfriction coefficient the obstruction degree of deformationraises For the specimen with the two ends completely fixed(ie 120583 = infin) there is no horizontal deformation at the endsmaking the confinement effect very strong
From Figure 10 one can note that a larger end frictioncoefficient leads to a lower damage level in the top and bottomof the specimen with a constant nominal strain rate Forlarger end friction coefficient the damaged areas draw closeto the central section from the top and bottom of the concretespecimenThese phenomena should generate due to the effectof the end friction confinement which changes the uniaxialloading state in the local regions of concrete These can alsobe illustrated from the simulation results in Figures 8 and 9
42 Effect of End Friction Confinement on Dynamic Compres-sive Strength The macroscopic nominal compressive stress-strain curves of the concrete specimen under different strainrates and end friction coefficients are plotted and compared inFigure 11 Moreover the corresponding peak stresses that isthe nominal dynamic compressive strengths of concrete arereported in Table 2 Obviously both the stress-strain curvesof concrete in Figure 11 and the axial dynamic compressivestrengths in Table 2 demonstrate the effects of strain rates andend friction coefficients
It can be noted obviously from Figure 11 and Table 2 thatthe dynamic uniaxial compressive strength of concrete isimproved due to the end friction confinement effect Further-more under the same strain rates the ascending curves of theconcrete sample with various friction coefficients are almostoverlapped indicating that the elastic modulus of concreteis almost not influenced by the end friction confinementeffect The obtained compressive strengths and the softening
curves are distinct significantly because the stresses andstrains status as well as the fracture paths within the concretespecimen for different friction coefficients vary
For various strain rates the quantitative relationshipsbetween the obtained dynamic compressive strengths of theconcrete specimen and end friction coefficient are presentedin Figures 12(a) and 12(b) It can be seen clearly fromFigure 12 that the concrete dynamic compressive strengthincreases with the increase of end friction coefficient Whenthe end friction coefficient 120583 grows from 0 to 03 the uniaxialcompressive strength increases rapidly while the uniaxialdynamic compressive strength increases slightly and thengets to be stable when the end friction coefficient exceeds 03This is to say when the end friction coefficient exceeds 03 theend confinement effect on the dynamic compressivemechan-ical behavior of concrete can be ignored This can also beconcluded from the analysis resultsmentioned previously forexample the damage factor distribution of concrete pre-sented in Figure 10
Furthermore the results about the effect of end frictionconfinement on concrete dynamic compressive strength atmedium and low strain rates are similar to those at high strainrate For more information about the end confinement effectfor high strain rate refer to Li et al [40]
Figure 13 presents the damage distribution within theconcrete specimens at their corresponding peak stressesunder different end friction confinement conditions at thesame loading velocities Figure 13(a) shows the results for theloading condition of a relative lower strain rate that is 120576 = 1 times10minus2 sminus1 One can note that for ldquopurerdquo uniaxial compressivebehavior of concrete (ie the end friction 120583 between theconcrete specimen and the rigid block is zero 120583 = 0) thenumber of cracks generated or the damage degree withinthe specimen is very limited when reaching the compressivestrength of the concrete sample With the increase of endfriction coefficient for example 120583 = 01 and 02 the totalnumber of cracks ascends gradually but the number of cracksnear the top and bottom regions of the specimen descendsWhen the end friction coefficient becomes larger than 03(eg 120583 = 03 06 08 and infin) the number of cracks turnsto be stable but the width of the cracks broadens as can beseen in Figure 13(a)
Figure 13(b) shows the simulation results for the loadingcondition of a relative higher strain rate that is 120576 = 1 times10minus05 sminus1 For ldquopurerdquo uniaxial compression (ie the end
14 Shock and Vibration
7252015
9
Quasistatic loading
8
95
85
752515
Dynamic loading
20
Dynamic loading
20
10
9
8
25 30 35302520
11
10
9
8
Dynamic loading
Dynamic loading Dynamic loading= 1 times 10minus1 sminus1
= 1 times 10minus3 sminus1
= 1 times 10minus2 sminus1
= 1 times 10minus5 sminus1
times10minus3
0
3
6
9
12
15
18C
ompr
essiv
e st
ress
(MPa
)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
= 1 times 10minus15 sminus1
= 1 times 10minus05 sminus1
120576
120576
120576
120576
120576
120576
Figure 11 Continued
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
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Shock and Vibration
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International Journal of
Shock and Vibration 5
the compressive strength in (10a) and (10b) was oftenadopted for example in the publications [10 11]
The CEB also gives empirical formulae to estimate theDIF for concrete tensile strength However comparisonbetween the available experimental results in the literaturewith the CEB empirical equations indicates that the CEBtensile DIF substantially underestimates the tensile DIF ofconcrete [24 25] In Malvar and Rossrsquos [24] work an empiri-cal formula was proposed and the formula for the tensile DIFcan be written as
TDIF =119891td119891ts
= (120576119889
120576ts)
120575
for 120576119889le 1 sminus1 (11a)
TDIF =119891td119891ts
= 120573(120576119889
120576ts)
13
for 120576119889gt 1 sminus1 (11b)
where 119891td and 119891ts are respectively the dynamic uniaxial ten-sile strength at the strain rate 120576
119889and the quasistatic uniaxial
tensile strength 120576ts = 10minus6 sminus1 (static strain rate) log120573 = 6120575minus2
120575 = 1(1 + 81198911015840
1198881198911015840
1198880) 11989110158401198880= 10MPa and 119891
1015840
119888is the quasistatic
uniaxial compressive strength of concrete (in MPa)
3 Mesoscale ComputationalModel for Concrete
Theoretical experimental and numerical studies indicatethat the failure pattern crack mode and even the velocity ofthe crack propagation are influenced by loading rate [11 26ndash28] The mechanical behaviors of concrete including themacroscopic mechanical properties and the failure patternsare associated with the micro-mesostructure of concreteDue to the complexity of concrete the failure behavior can bestudied numerically In the numerical simulations concreteheterogeneity should be accounted for and thus it requiresthe adoption of a mesoscale mechanical model in which theheterogeneity can be explicitly described
At themesoscale concretewas often assumed to be amul-tiphase composite composed of aggregate mortar matrix theinterfacial transition zones [ITZs] voids and so forth A lot ofwork [9 10 19 29] has demonstrated that the ITZs have a dra-matic influence on the failure pattern and the macromechan-ical properties of concrete However the mechanical proper-ties especially the dynamic mechanical behavior of the ITZsare not well understood yet [13 19 30ndash32] Moreover thereal typical thickness of ITZ is about 10ndash50120583m [9 10] whichlimits the minimum size of the finite element mesh In mostsimulation efforts the ITZ thickness is set as 02ndash08mm[9 10] 05mm [8] 04mm [19] and 1mm [12] for the sake ofsimplicity
31 Mesostructure and Mechanical Model of Concrete Con-crete exhibits heterogeneity in material and mechanicalproperties onmany length scales [29] At the mesoscale con-sidering the effect of heterogeneities of concrete the concretein the present work was regarded as a three-phase compositecomposed of coarse aggregate particles mortar matrix andthe ITZs between the former two phases Random aggregatemodels have long been demonstrated to be an effective
mesomechanical approach to simulating the failure processand the deformation of concrete and they have been widelyutilized in fracturemechanics of concrete for example in [11ndash13 33] Based on the concrete random aggregate model inwhich the shape size and distribution of the coarse aggregateparticles closely resemble real concrete in the statistical senselots of efforts have been carried out to investigate the macro-scopic mechanical behavior and failure mechanism of con-crete [10ndash12 29] In this work the concrete random aggregatemodel was therefore also employed
Due to great computational expense and memorydemand of mesoscale simulations it is in general notpossible to model the full structure at the mesoscale with thecomputational power available nowadays Herein the presentstudy only two-dimensional simulations were thus con-ducted Similar to the work [9ndash12 33] the aggregate particlesare modeled as circles with random spatial distributionenfolded by a thin interface layer of ITZ Similar to those in[11 12] the ldquotake-and-placerdquo method was utilized to generatethe coarse aggregate particles The fine ones and othercomponents (eg air voids) were assumed to be mixed upwith the cement paste establishing the mortar matrix phaseThis matrix phase can thus be regarded as a homogeneouscomponent at the mesoscale The material properties of thepaste phase are thus strongly dependent on the type of cementused amount of pores water to cement ratio and otheradditives present in the concrete which can be determinedby microscale simulation efforts Furthermore the Fullercurve widely utilized for example in [11 12] was selected todetermine the distribution of aggregate with different sizesemployed in the concrete specimen The aggregate particleswere then placed into the matrix one by one at randomlydetermined positions and in such a way that no overlappingwith particles already placed Finally at the mesoscale aggre-gate particles (typically sand or gravel) and the surroundingITZ layers behave as inclusions in the matrix phase of mortarmatrix
Figure 4 presents a typical schematic diagram of concretemesostructure generated by employing the above approachThe size of the heterogeneous concrete specimen is 150mm times
150mm Note that aggregate particles in real concrete arenot perfectly circular However the efforts in [10 11] haveindicated that the effect of aggregate shape on macroscopicstress-strain curve of concrete seems to be very smallSimilar to that in [11 34] the concrete sample contains 6medium stones with a diameter of 30mm and 56 small stoneswith a diameter of 12mm The concrete specimens involveabout 469 of aggregate per volume In Figure 4 the greenareas mean the aggregate phase the red thin-layer zonessurrounding the aggregate particles are the ITZs and the greyzones denote the mortar matrix Herein the interfacial zonesare viewed as uniform thickness shells placed concentricallyaround each aggregate Similar to the work [34] the thicknessof the ITZ was set as 1mm
To describe the influence of end friction confinement onthe dynamic compressive mechanical properties of concretetwo rigid blocks (see the two blue blocks in Figure 4) wereplaced respectively at the top and the bottom of the con-crete specimen The interactions between the heterogeneous
6 Shock and Vibration
y
x
AggregateITZ
Mortar matrixRigid block
Uniaxial compression
Unit mm End
fric
tion
25 25150
2525
150
Figure 4 Mesoscale mechanical model of concrete under dynamic uniaxial compression considering the influence of end frictionconfinement The specimen has 22346 elements [For interpretation of the references to color in this figure legend the reader is referredto the web version of this paper]
concrete specimen and the two rigid blocks that is the twored-line regions are implemented by the classic coulombfriction behavior The friction coefficients considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces ofthe specimen were fixed in the horizontal direction) fora quantitative assessment of the end friction confinementeffect As known the DIF difference obtained from thesimulation results with different friction coefficients canthen be attributed purely to the influence of end frictionconfinement effects
Themeshing of these concrete specimens were conductedwith four node solid elements with a linear strain field Tohave a better understanding of concrete fracture the averagemesh size was l mm which is consistent with that in the workfrom Hentz et al [23] and Du et al [11 12]
32 Mechanical Parameters for the Three MesocomponentsIn Zhou and Haorsquos [11 13] and Snozzi et alrsquos [35] workthe uniaxial tensile and compressive mechanical behaviorof concrete at high strain rate were studied From theirsimulation observations it can be noticed that no damagegenerates in the aggregate phaseMoreover in Pedersen et alrsquos[8] simulation of the dynamic tensile behavior of concretethe aggregate grains were assumed to follow a linear elasticmaterial behaviorThis is because the tensile and compressivestrengths of the aggregate are much larger than those of mor-tar matrix and the ITZs Similar to the work [8 11] the aggre-gate was assumed as elastic in the following simulationsThistreatment should work for the concrete subjected to mediumand low strain rates as discussed in the present study
To the mortar matrix and the ITZs the continuumdamage mechanics theories mentioned previously wereemployed to describe their mechanical properties In contin-uum mechanics the constitutive model is often expressed in
terms of stress-strain relations When the material exhibitsstrain-softening behavior leading to the strain localizationbehavior this formulation leads to a strongmesh dependencyof the finite element results in which the energy dissipateddecreases upon mesh refinement [11 19] Similar to the workin [10 11 19] to avoid or release unreasonable mesh sensitiveresults the tensile postfailure behavior was given in terms ofa fracture energy cracking criterion by specifying a stress-displacement curve instead of a stress-strain curve In addi-tion unlike discrete crack models [36 37] the continuumdamaged plasticity model based on continuum mechanicsuses damage factors such asDAMAGEC for compression andDAMAGET for tension to describe the fracture behavior andit is not capable of providing accurate crack geometry such ascrack width
The main mechanical parameters including the elasticmodulus Poissonrsquos ratio and uniaxial tensilecompressivestrengths of the three mesoconstituents used in this study forthe following numerical analysis were listed in Table 1
It is to be noted that the DIFs given in Section 22 are builtbased on the test results on concrete material The strain rateeffects for the aggregate phase mortar matrix and the ITZare essentially distinct as illustrated in [38 39] NeverthelessGrote et alrsquos [21] experimental observations indicate that thedynamic mechanical behavior of mortar matrix is closelysimilar to that of concrete In addition the ITZ layer can betreated as a kind of mortar matrix with a high(er) porosity[34] and thus its dynamic mechanical behavior can also beregarded as similar to those of mortar matrix and concreteIn summary it is assumed that the ITZ and the mortarmatrix have the same DIFs mentioned previously The treat-ments are consistent with the ones in [9 10] The strainrate effect for both the mortar matrix and the ITZs ontheir tensilecompressive strengths was incorporated intothe plasticity damaged model which was represented by
Shock and Vibration 7
Table 1 Mechanical parameters of the concrete mesocomponentsused in the study
Mortar matrix ITZ AggregateMass density 120588 [kgm3] 275 times 103 275 times 103 288 times 103
Elastic modulus [GPa] 30lowast
25lowast
70lowast
Poissonrsquos ratio 02lowast
022lowast
016lowast
Dilation angle 120595 [∘] 30 30Eccentricity 120578 01 01Shape factor 119870
1198880667 0667
Stress ratio 120590119888119888120590119888
116 116Tensile yield stress 120590
119905[MPa] 143
lowast12lowast
Compressive yield stress 1205901198880
[MPa] 143lowast
12lowast
Ultimate compressive yieldstress 120590cu [MPa] 143 12
Note data with ldquolowastrdquo are quoted from Du et al [12]
a dynamic increase factor (ie the DIF) with respect to strainrate
33 BoundaryLoading Conditions and FE Simulations Toexamine the effects of end friction confinement on themacromechanical behavior of concrete subjected to dynamiccompressive loadings the failure behavior of the concretespecimen was explored The corresponding loading andboundary conditions for the interaction system were illus-trated as follows (1) constant vertical velocity V was appliedon the top surface of the rigid block and the left and rightsides of the specimen are free of stress (2) the movementat the bottom rigid block was fixed at both the vertical andhorizontal directions (3) friction behavior between the twoblocks and the concrete sample was set The nominal strainrate 120576 is defined as the applied velocity divided by the heightof the specimen that is 120576 = Vℎ where ℎ is the height of thespecimen
In the following simulations ABAQUS increased auto-matically the size of step time going from smaller one to themaximumauthorized defined by the user For all the concretespecimens the numerical simulations were performed in aplane strain condition
34 Verification of the Mesoscale Approach In reality theavailable tests on loading rate effect of concrete are not veryrich and the test data is also not complete Comparativelyspeaking Dilger et alrsquos [14] test data is the most completeone and it is often used to verify the reliability of the analysismethod or model such as in [26]
To illustrate the reliability and accuracy of the presentmesoscale simulation method Dilger et alrsquos [14] test on thedynamic uniaxial compressive behavior of concrete was alsoselected for the comparison in this section In Dilger et alrsquos[14] experiment the macroscopic mechanical behavior ofconcrete under different nominal strain rates (ie the strainrates of 333 times 10minus5 sminus1 333 times 10minus3 sminus1 and 02 sminus1) was
explored and the complete compressive stress-strain curvesof concrete were obtained
In the previouswork [33] a series of dynamic compressivetest of concrete under different strain rates were conductedbased on the present mesoscale mechanical method includ-ing 120576 = 333 times 10minus5 sminus1 1 times 10minus4 sminus1 333 times 10minus3 sminus1 1 times 10minus2 sminus15 times 10minus2 sminus1 02 sminus1 1 sminus1 100 sminus1 and 200 sminus1 It is to benoted that in the simulations the concrete specimens werefixed at one end and loaded longitudinally through an appliedconstant velocity at the other end The detailed mechanicalparameters and analysis method can refer to [33]
Figure 5 presents the failure patterns of the concretespecimen subjected to different nominal strain rates Onecan notice that with the increase of strain rate the numberof cracks (ie the red damaged region) increases obviouslyand the crack branching behavior occurs Therefore withthe increase of strain rate the fracture of concrete requiresmore energy demand to reach failure which should be themain reason for the improvement of the dynamic strength ofconcrete
Figure 6(a) reports the comparison between the sim-ulations results (solid curves) and the experimental data(symbols) in terms of nominal stress (applied forces dividedby the specimen cross sectional area) versus nominal strain(the displacement generated at the applied-load end dividedby the length of the specimen) curves and the agreementis very good It should be noted herein that as mentionedpreviously the relatedmechanical and physical parameters ofthe concrete mixture used in the test are not full especiallythe mechanical parameters of the ITZ Accordingly in thepreviouswork [33] themechanical parameters (especially theelasticmodulus and the strength) of the ITZwere determinedby the inversion method on the basis of only two strainrates (333 times 10minus5 sminus1 and 333 times 10minus3 sminus1) The simulationof the third available strain (ie 02 sminus1) can be regarded asa validation of the ability of the model to predict concretestrength outside the range of strain rates used for calibrationThis treatment is similar to that in [26]
Furthermore the compressive DIFs were evaluatedaccording to the simulation results and the comparison of thepresent simulation results and some available experimentalobservations is plotted in Figure 6(b) It can be observedthat the present simulation results agree very well with thecollective experimental data This indicates that the presentanalysis method can well simulate the dynamic compressivebehavior of concrete The validated mesoscale mechanicalapproach would be employed in the following simulations tostudy the effect of end friction confinement on the dynamiccompressive behavior of concrete
4 Dynamic Compressive FailureBehavior of Concrete
On the basis of the mesoscale mechanical model describedin Section 3 the simulations of the dynamic axial com-pression of the concrete specimen with various end fric-tion coefficients were implemented The loading velocitiesadopted on the upper rigid block in the simulations are
8 Shock and Vibration
10Damage
120576 = 333 times 10minus5 120576 = 1 times 10minus4 120576 = 333 times 10minus3 120576 = 1 times 10minus2 120576 = 5 times 10minus2
120576 = 2 times 10minus1 120576 = 1 120576 = 100 120576 = 200
Figure 5 Compressive failure patterns of the concrete specimen under different strain rates ranging from 1 times 10minus5 sminus1 to 200 sminus1
Compression test(Dilger et al 1984) and present model
Nom
inal
com
pres
sive
stre
ss (M
Pa)
0002 00030001 0004 0005 00060Compressive strain
0
10
20
30
40
120576 = 333 times 10minus5 sminus1
120576 = 333 times 10minus3 sminus1
120576 = 02 sminus1
(a)
001 1 100
09
12
15
18
21
24
Com
pres
sive D
IF
Test data Present method
1E minus 6 1E minus 4
Strain rate (sminus1)
(b)
Figure 6 (a) Comparison of the present simulation results and Dilger et alrsquos [14] test data and (b) compressive DIFs for the simulation resultsand some available test data
Shock and Vibration 9
Dynamic loading
0
2
4
6
8
10
12
14
Com
pres
sive
stre
ss (M
Pa)
120576 = 1 times 10minus1 sminus1
times10minus3
Mesh size 15mmMesh size 10mmMesh size 05mm
End friction coefficient 120583 = 06
1 432 5 6 70Strain 120576
(a)
Mesh size 15mmMesh size 10mmMesh size 05mm
Damage factor0 1
(b)
Figure 7 (a) The simulation results of three concrete specimens with the same distribution of aggregates and different mesh sizes and(b) damage distribution of the concrete specimens with different mesh sizes under the same strain rate and friction coefficients at theirpeak stresses
V = 15 times 10minus6ms 15 times 10minus4ms 15 times 10minus3ms 15 times
10minus25ms 15 times 10minus2ms 15 times 10minus15ms and 15 times 10minus1msin an ascending sequence and in every loading cycle the con-stant velocity was utilized The corresponding macroscopicnominal strain rates are 120576 = 1 times 10minus5 sminus1 (quasistatic) 1 times10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1and 1 times 100 sminus1 respectively Moreover as mentioned previ-ously the seven end friction coefficients 120583 considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces of thespecimenwere fixed in the horizontal direction) respectively
To check the mesh sensitivity in the simulations threedifferentmesh sizeswere utilized that is 05mm 10mm and
15mm Figure 7(a) presents the nominal compressive stress-strain curves of the concrete specimen subjected to a nominalstrain rate of 01 sminus1 with the same end friction coefficientand the three different mesh sizes It can be found clearlyfrom Figure 7(a) that the mesh sizes (ie 05mm 10mmand 15mm) have less influence on the stress-strain curvesThe three curves are also overlapped Figure 7(b) shows thedamage distribution of the three concrete specimens men-tioned above with the same distribution of aggregates Onecannotice that the failure patterns of the three specimenswithdifferent mesh sizes are closely similar to each other Conse-quently the mesh size of 15mm was used in the followingsimulations
10 Shock and Vibration
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
Equivalent plastic strain times10minus300 56
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
120576
120576
120576
120576
120576
Figure 8 Equivalent plastic strain distribution within the concrete specimen under different strain rates and end friction coefficients at theirpeak compressive stresses
41 Effects of Strain Rate and End Friction Confinement onFailure Patterns of Concrete Figure 8 presents the equivalentplastic strain distribution within the concrete specimensunder five groups of different strain rates ( 120576 = 1 times 10minus5 sminus11 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus1 sminus1 and 1 times 100 sminus1) and fourgroups of different friction coefficients (120583 = 0 03 08 andinfin) at their peak compressive stresses (ie the compressivestrength) One can note from Figures 8(a)ndash8(d) that for thespecimen with the same friction coefficient with the increase
of nominal strain rate the equivalent plastic strain withinconcrete increases obviously In addition as the frictioncoefficient 120583 increases from 0 to infin the equivalent plasticstrain within concrete at reaching the peak stress varies
For the specimenwith the friction coefficient of 0 and 03the obtained plastic strain distributions within the concretespecimens are obviously different For the one with the fric-tion coefficient of 03 and 08 the obtained plastic strain dis-tributions are slightly different And for that with the friction
Shock and Vibration 11
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
000 49
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Maximum principal stress (MPa)
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 9 Maximum principal stress distribution within the concrete specimen under different strain rates and end friction coefficients attheir peak compressive stresses
coefficient of 08 andinfin the obtained plastic strain distribu-tions are almost totally consistent That is to say when thefriction coefficient becomes larger than 08 the effect of endfriction confinement on the failure patterns of concrete canbe ignored
The maximum principal stress distributions within theconcrete specimens under the five groups of different strainrates and the four different friction coefficients at the peakcompressive stresses are presented in Figure 9 It can be
noted intuitively from Figure 9 that the changes of nominalstrain rate and friction coefficient have a significant influenceon the maximum principal stress distribution of the speci-menWith the increase of end friction coefficient the value ofmaximum principal stress gets large and the distribution areadraws close to central section from the top and bottom of theconcrete specimen respectively at same loading velocity
The damage (ie the cracks) distributions within theconcrete specimens corresponding to Figures 8 and 9 are
12 Shock and Vibration
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
0 1
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Damage factor
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 10 Damage distribution within the concrete specimens under different strain rates and friction coefficients at their peak stresses
presented in Figure 10 for different loading velocities anddifferent end friction coefficients In Figure 10 differentcolors represent different damage indexes The red colordenotes the most serious damage while the blue color meansthat no damage generates The white rounded areas whichare regarded as aggregates in these models have no damage
It can be noticed clearly from Figure 10 that the damagedareas increase with the growth of nominal strain rate Whenthe nominal strain rate is relatively low(er) (eg 1 times 10minus5 sminus1)the damaged area of the specimens is small when reaching
their peak stress Accordingly the damage regions (iecracks) are narrow and short and the number of cracks islimited As the nominal strain rate rises from 1times 10minus5 sminus1 to 1times100 sminus1 the damaged area and the number of cracks increasegradually When the nominal strain rate is relatively high(er)(eg 1 times 100 sminus1) a lot of areas are damaged in different levelsThe cracks widen and link together forming a crack networksimultaneously
Therefore it can be concluded that with the increase ofloading velocity the nominal strain rate increases gradually
Shock and Vibration 13
Table 2 Dynamic compressive strength of concrete under different end friction coefficients
120583Dynamic compressive strength [MPa]
1 times 10minus5 sminus1 1 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1 1 times 100 sminus1
0 793 806 858 919 1042 1197 153901 829 838 906 977 1113 1297 161202 846 857 926 1007 1137 1349 168203 849 864 939 1016 1167 1355 169606 857 877 955 1036 1175 1382 173608 860 881 962 1042 1185 1391 1745infin 875 892 980 1067 1212 1406 1749
and the number of cracks or damaged zones increases whenthe apparent compressive strength of concrete is reachedTheenergy consumption of the loading process increases corre-spondinglyThis should be the major reason for the improve-ment of dynamic compressive strength of concrete materials
It can be found obviously from the comparison amongFigures 10(a)ndash10(d) that the damage states of concrete spec-imens are diverse at their peak stresses for different endfriction conditions
Compared with the concrete specimen without end fric-tion confinement (ie 120583 = 0) the deformation at the end ofthe specimen considering the effect of end friction (ie120583 gt 0)was obviously hindered In addition with the increase of endfriction coefficient the obstruction degree of deformationraises For the specimen with the two ends completely fixed(ie 120583 = infin) there is no horizontal deformation at the endsmaking the confinement effect very strong
From Figure 10 one can note that a larger end frictioncoefficient leads to a lower damage level in the top and bottomof the specimen with a constant nominal strain rate Forlarger end friction coefficient the damaged areas draw closeto the central section from the top and bottom of the concretespecimenThese phenomena should generate due to the effectof the end friction confinement which changes the uniaxialloading state in the local regions of concrete These can alsobe illustrated from the simulation results in Figures 8 and 9
42 Effect of End Friction Confinement on Dynamic Compres-sive Strength The macroscopic nominal compressive stress-strain curves of the concrete specimen under different strainrates and end friction coefficients are plotted and compared inFigure 11 Moreover the corresponding peak stresses that isthe nominal dynamic compressive strengths of concrete arereported in Table 2 Obviously both the stress-strain curvesof concrete in Figure 11 and the axial dynamic compressivestrengths in Table 2 demonstrate the effects of strain rates andend friction coefficients
It can be noted obviously from Figure 11 and Table 2 thatthe dynamic uniaxial compressive strength of concrete isimproved due to the end friction confinement effect Further-more under the same strain rates the ascending curves of theconcrete sample with various friction coefficients are almostoverlapped indicating that the elastic modulus of concreteis almost not influenced by the end friction confinementeffect The obtained compressive strengths and the softening
curves are distinct significantly because the stresses andstrains status as well as the fracture paths within the concretespecimen for different friction coefficients vary
For various strain rates the quantitative relationshipsbetween the obtained dynamic compressive strengths of theconcrete specimen and end friction coefficient are presentedin Figures 12(a) and 12(b) It can be seen clearly fromFigure 12 that the concrete dynamic compressive strengthincreases with the increase of end friction coefficient Whenthe end friction coefficient 120583 grows from 0 to 03 the uniaxialcompressive strength increases rapidly while the uniaxialdynamic compressive strength increases slightly and thengets to be stable when the end friction coefficient exceeds 03This is to say when the end friction coefficient exceeds 03 theend confinement effect on the dynamic compressivemechan-ical behavior of concrete can be ignored This can also beconcluded from the analysis resultsmentioned previously forexample the damage factor distribution of concrete pre-sented in Figure 10
Furthermore the results about the effect of end frictionconfinement on concrete dynamic compressive strength atmedium and low strain rates are similar to those at high strainrate For more information about the end confinement effectfor high strain rate refer to Li et al [40]
Figure 13 presents the damage distribution within theconcrete specimens at their corresponding peak stressesunder different end friction confinement conditions at thesame loading velocities Figure 13(a) shows the results for theloading condition of a relative lower strain rate that is 120576 = 1 times10minus2 sminus1 One can note that for ldquopurerdquo uniaxial compressivebehavior of concrete (ie the end friction 120583 between theconcrete specimen and the rigid block is zero 120583 = 0) thenumber of cracks generated or the damage degree withinthe specimen is very limited when reaching the compressivestrength of the concrete sample With the increase of endfriction coefficient for example 120583 = 01 and 02 the totalnumber of cracks ascends gradually but the number of cracksnear the top and bottom regions of the specimen descendsWhen the end friction coefficient becomes larger than 03(eg 120583 = 03 06 08 and infin) the number of cracks turnsto be stable but the width of the cracks broadens as can beseen in Figure 13(a)
Figure 13(b) shows the simulation results for the loadingcondition of a relative higher strain rate that is 120576 = 1 times10minus05 sminus1 For ldquopurerdquo uniaxial compression (ie the end
14 Shock and Vibration
7252015
9
Quasistatic loading
8
95
85
752515
Dynamic loading
20
Dynamic loading
20
10
9
8
25 30 35302520
11
10
9
8
Dynamic loading
Dynamic loading Dynamic loading= 1 times 10minus1 sminus1
= 1 times 10minus3 sminus1
= 1 times 10minus2 sminus1
= 1 times 10minus5 sminus1
times10minus3
0
3
6
9
12
15
18C
ompr
essiv
e st
ress
(MPa
)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
= 1 times 10minus15 sminus1
= 1 times 10minus05 sminus1
120576
120576
120576
120576
120576
120576
Figure 11 Continued
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
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International Journal of
6 Shock and Vibration
y
x
AggregateITZ
Mortar matrixRigid block
Uniaxial compression
Unit mm End
fric
tion
25 25150
2525
150
Figure 4 Mesoscale mechanical model of concrete under dynamic uniaxial compression considering the influence of end frictionconfinement The specimen has 22346 elements [For interpretation of the references to color in this figure legend the reader is referredto the web version of this paper]
concrete specimen and the two rigid blocks that is the twored-line regions are implemented by the classic coulombfriction behavior The friction coefficients considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces ofthe specimen were fixed in the horizontal direction) fora quantitative assessment of the end friction confinementeffect As known the DIF difference obtained from thesimulation results with different friction coefficients canthen be attributed purely to the influence of end frictionconfinement effects
Themeshing of these concrete specimens were conductedwith four node solid elements with a linear strain field Tohave a better understanding of concrete fracture the averagemesh size was l mm which is consistent with that in the workfrom Hentz et al [23] and Du et al [11 12]
32 Mechanical Parameters for the Three MesocomponentsIn Zhou and Haorsquos [11 13] and Snozzi et alrsquos [35] workthe uniaxial tensile and compressive mechanical behaviorof concrete at high strain rate were studied From theirsimulation observations it can be noticed that no damagegenerates in the aggregate phaseMoreover in Pedersen et alrsquos[8] simulation of the dynamic tensile behavior of concretethe aggregate grains were assumed to follow a linear elasticmaterial behaviorThis is because the tensile and compressivestrengths of the aggregate are much larger than those of mor-tar matrix and the ITZs Similar to the work [8 11] the aggre-gate was assumed as elastic in the following simulationsThistreatment should work for the concrete subjected to mediumand low strain rates as discussed in the present study
To the mortar matrix and the ITZs the continuumdamage mechanics theories mentioned previously wereemployed to describe their mechanical properties In contin-uum mechanics the constitutive model is often expressed in
terms of stress-strain relations When the material exhibitsstrain-softening behavior leading to the strain localizationbehavior this formulation leads to a strongmesh dependencyof the finite element results in which the energy dissipateddecreases upon mesh refinement [11 19] Similar to the workin [10 11 19] to avoid or release unreasonable mesh sensitiveresults the tensile postfailure behavior was given in terms ofa fracture energy cracking criterion by specifying a stress-displacement curve instead of a stress-strain curve In addi-tion unlike discrete crack models [36 37] the continuumdamaged plasticity model based on continuum mechanicsuses damage factors such asDAMAGEC for compression andDAMAGET for tension to describe the fracture behavior andit is not capable of providing accurate crack geometry such ascrack width
The main mechanical parameters including the elasticmodulus Poissonrsquos ratio and uniaxial tensilecompressivestrengths of the three mesoconstituents used in this study forthe following numerical analysis were listed in Table 1
It is to be noted that the DIFs given in Section 22 are builtbased on the test results on concrete material The strain rateeffects for the aggregate phase mortar matrix and the ITZare essentially distinct as illustrated in [38 39] NeverthelessGrote et alrsquos [21] experimental observations indicate that thedynamic mechanical behavior of mortar matrix is closelysimilar to that of concrete In addition the ITZ layer can betreated as a kind of mortar matrix with a high(er) porosity[34] and thus its dynamic mechanical behavior can also beregarded as similar to those of mortar matrix and concreteIn summary it is assumed that the ITZ and the mortarmatrix have the same DIFs mentioned previously The treat-ments are consistent with the ones in [9 10] The strainrate effect for both the mortar matrix and the ITZs ontheir tensilecompressive strengths was incorporated intothe plasticity damaged model which was represented by
Shock and Vibration 7
Table 1 Mechanical parameters of the concrete mesocomponentsused in the study
Mortar matrix ITZ AggregateMass density 120588 [kgm3] 275 times 103 275 times 103 288 times 103
Elastic modulus [GPa] 30lowast
25lowast
70lowast
Poissonrsquos ratio 02lowast
022lowast
016lowast
Dilation angle 120595 [∘] 30 30Eccentricity 120578 01 01Shape factor 119870
1198880667 0667
Stress ratio 120590119888119888120590119888
116 116Tensile yield stress 120590
119905[MPa] 143
lowast12lowast
Compressive yield stress 1205901198880
[MPa] 143lowast
12lowast
Ultimate compressive yieldstress 120590cu [MPa] 143 12
Note data with ldquolowastrdquo are quoted from Du et al [12]
a dynamic increase factor (ie the DIF) with respect to strainrate
33 BoundaryLoading Conditions and FE Simulations Toexamine the effects of end friction confinement on themacromechanical behavior of concrete subjected to dynamiccompressive loadings the failure behavior of the concretespecimen was explored The corresponding loading andboundary conditions for the interaction system were illus-trated as follows (1) constant vertical velocity V was appliedon the top surface of the rigid block and the left and rightsides of the specimen are free of stress (2) the movementat the bottom rigid block was fixed at both the vertical andhorizontal directions (3) friction behavior between the twoblocks and the concrete sample was set The nominal strainrate 120576 is defined as the applied velocity divided by the heightof the specimen that is 120576 = Vℎ where ℎ is the height of thespecimen
In the following simulations ABAQUS increased auto-matically the size of step time going from smaller one to themaximumauthorized defined by the user For all the concretespecimens the numerical simulations were performed in aplane strain condition
34 Verification of the Mesoscale Approach In reality theavailable tests on loading rate effect of concrete are not veryrich and the test data is also not complete Comparativelyspeaking Dilger et alrsquos [14] test data is the most completeone and it is often used to verify the reliability of the analysismethod or model such as in [26]
To illustrate the reliability and accuracy of the presentmesoscale simulation method Dilger et alrsquos [14] test on thedynamic uniaxial compressive behavior of concrete was alsoselected for the comparison in this section In Dilger et alrsquos[14] experiment the macroscopic mechanical behavior ofconcrete under different nominal strain rates (ie the strainrates of 333 times 10minus5 sminus1 333 times 10minus3 sminus1 and 02 sminus1) was
explored and the complete compressive stress-strain curvesof concrete were obtained
In the previouswork [33] a series of dynamic compressivetest of concrete under different strain rates were conductedbased on the present mesoscale mechanical method includ-ing 120576 = 333 times 10minus5 sminus1 1 times 10minus4 sminus1 333 times 10minus3 sminus1 1 times 10minus2 sminus15 times 10minus2 sminus1 02 sminus1 1 sminus1 100 sminus1 and 200 sminus1 It is to benoted that in the simulations the concrete specimens werefixed at one end and loaded longitudinally through an appliedconstant velocity at the other end The detailed mechanicalparameters and analysis method can refer to [33]
Figure 5 presents the failure patterns of the concretespecimen subjected to different nominal strain rates Onecan notice that with the increase of strain rate the numberof cracks (ie the red damaged region) increases obviouslyand the crack branching behavior occurs Therefore withthe increase of strain rate the fracture of concrete requiresmore energy demand to reach failure which should be themain reason for the improvement of the dynamic strength ofconcrete
Figure 6(a) reports the comparison between the sim-ulations results (solid curves) and the experimental data(symbols) in terms of nominal stress (applied forces dividedby the specimen cross sectional area) versus nominal strain(the displacement generated at the applied-load end dividedby the length of the specimen) curves and the agreementis very good It should be noted herein that as mentionedpreviously the relatedmechanical and physical parameters ofthe concrete mixture used in the test are not full especiallythe mechanical parameters of the ITZ Accordingly in thepreviouswork [33] themechanical parameters (especially theelasticmodulus and the strength) of the ITZwere determinedby the inversion method on the basis of only two strainrates (333 times 10minus5 sminus1 and 333 times 10minus3 sminus1) The simulationof the third available strain (ie 02 sminus1) can be regarded asa validation of the ability of the model to predict concretestrength outside the range of strain rates used for calibrationThis treatment is similar to that in [26]
Furthermore the compressive DIFs were evaluatedaccording to the simulation results and the comparison of thepresent simulation results and some available experimentalobservations is plotted in Figure 6(b) It can be observedthat the present simulation results agree very well with thecollective experimental data This indicates that the presentanalysis method can well simulate the dynamic compressivebehavior of concrete The validated mesoscale mechanicalapproach would be employed in the following simulations tostudy the effect of end friction confinement on the dynamiccompressive behavior of concrete
4 Dynamic Compressive FailureBehavior of Concrete
On the basis of the mesoscale mechanical model describedin Section 3 the simulations of the dynamic axial com-pression of the concrete specimen with various end fric-tion coefficients were implemented The loading velocitiesadopted on the upper rigid block in the simulations are
8 Shock and Vibration
10Damage
120576 = 333 times 10minus5 120576 = 1 times 10minus4 120576 = 333 times 10minus3 120576 = 1 times 10minus2 120576 = 5 times 10minus2
120576 = 2 times 10minus1 120576 = 1 120576 = 100 120576 = 200
Figure 5 Compressive failure patterns of the concrete specimen under different strain rates ranging from 1 times 10minus5 sminus1 to 200 sminus1
Compression test(Dilger et al 1984) and present model
Nom
inal
com
pres
sive
stre
ss (M
Pa)
0002 00030001 0004 0005 00060Compressive strain
0
10
20
30
40
120576 = 333 times 10minus5 sminus1
120576 = 333 times 10minus3 sminus1
120576 = 02 sminus1
(a)
001 1 100
09
12
15
18
21
24
Com
pres
sive D
IF
Test data Present method
1E minus 6 1E minus 4
Strain rate (sminus1)
(b)
Figure 6 (a) Comparison of the present simulation results and Dilger et alrsquos [14] test data and (b) compressive DIFs for the simulation resultsand some available test data
Shock and Vibration 9
Dynamic loading
0
2
4
6
8
10
12
14
Com
pres
sive
stre
ss (M
Pa)
120576 = 1 times 10minus1 sminus1
times10minus3
Mesh size 15mmMesh size 10mmMesh size 05mm
End friction coefficient 120583 = 06
1 432 5 6 70Strain 120576
(a)
Mesh size 15mmMesh size 10mmMesh size 05mm
Damage factor0 1
(b)
Figure 7 (a) The simulation results of three concrete specimens with the same distribution of aggregates and different mesh sizes and(b) damage distribution of the concrete specimens with different mesh sizes under the same strain rate and friction coefficients at theirpeak stresses
V = 15 times 10minus6ms 15 times 10minus4ms 15 times 10minus3ms 15 times
10minus25ms 15 times 10minus2ms 15 times 10minus15ms and 15 times 10minus1msin an ascending sequence and in every loading cycle the con-stant velocity was utilized The corresponding macroscopicnominal strain rates are 120576 = 1 times 10minus5 sminus1 (quasistatic) 1 times10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1and 1 times 100 sminus1 respectively Moreover as mentioned previ-ously the seven end friction coefficients 120583 considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces of thespecimenwere fixed in the horizontal direction) respectively
To check the mesh sensitivity in the simulations threedifferentmesh sizeswere utilized that is 05mm 10mm and
15mm Figure 7(a) presents the nominal compressive stress-strain curves of the concrete specimen subjected to a nominalstrain rate of 01 sminus1 with the same end friction coefficientand the three different mesh sizes It can be found clearlyfrom Figure 7(a) that the mesh sizes (ie 05mm 10mmand 15mm) have less influence on the stress-strain curvesThe three curves are also overlapped Figure 7(b) shows thedamage distribution of the three concrete specimens men-tioned above with the same distribution of aggregates Onecannotice that the failure patterns of the three specimenswithdifferent mesh sizes are closely similar to each other Conse-quently the mesh size of 15mm was used in the followingsimulations
10 Shock and Vibration
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
Equivalent plastic strain times10minus300 56
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
120576
120576
120576
120576
120576
Figure 8 Equivalent plastic strain distribution within the concrete specimen under different strain rates and end friction coefficients at theirpeak compressive stresses
41 Effects of Strain Rate and End Friction Confinement onFailure Patterns of Concrete Figure 8 presents the equivalentplastic strain distribution within the concrete specimensunder five groups of different strain rates ( 120576 = 1 times 10minus5 sminus11 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus1 sminus1 and 1 times 100 sminus1) and fourgroups of different friction coefficients (120583 = 0 03 08 andinfin) at their peak compressive stresses (ie the compressivestrength) One can note from Figures 8(a)ndash8(d) that for thespecimen with the same friction coefficient with the increase
of nominal strain rate the equivalent plastic strain withinconcrete increases obviously In addition as the frictioncoefficient 120583 increases from 0 to infin the equivalent plasticstrain within concrete at reaching the peak stress varies
For the specimenwith the friction coefficient of 0 and 03the obtained plastic strain distributions within the concretespecimens are obviously different For the one with the fric-tion coefficient of 03 and 08 the obtained plastic strain dis-tributions are slightly different And for that with the friction
Shock and Vibration 11
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
000 49
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Maximum principal stress (MPa)
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 9 Maximum principal stress distribution within the concrete specimen under different strain rates and end friction coefficients attheir peak compressive stresses
coefficient of 08 andinfin the obtained plastic strain distribu-tions are almost totally consistent That is to say when thefriction coefficient becomes larger than 08 the effect of endfriction confinement on the failure patterns of concrete canbe ignored
The maximum principal stress distributions within theconcrete specimens under the five groups of different strainrates and the four different friction coefficients at the peakcompressive stresses are presented in Figure 9 It can be
noted intuitively from Figure 9 that the changes of nominalstrain rate and friction coefficient have a significant influenceon the maximum principal stress distribution of the speci-menWith the increase of end friction coefficient the value ofmaximum principal stress gets large and the distribution areadraws close to central section from the top and bottom of theconcrete specimen respectively at same loading velocity
The damage (ie the cracks) distributions within theconcrete specimens corresponding to Figures 8 and 9 are
12 Shock and Vibration
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
0 1
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Damage factor
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 10 Damage distribution within the concrete specimens under different strain rates and friction coefficients at their peak stresses
presented in Figure 10 for different loading velocities anddifferent end friction coefficients In Figure 10 differentcolors represent different damage indexes The red colordenotes the most serious damage while the blue color meansthat no damage generates The white rounded areas whichare regarded as aggregates in these models have no damage
It can be noticed clearly from Figure 10 that the damagedareas increase with the growth of nominal strain rate Whenthe nominal strain rate is relatively low(er) (eg 1 times 10minus5 sminus1)the damaged area of the specimens is small when reaching
their peak stress Accordingly the damage regions (iecracks) are narrow and short and the number of cracks islimited As the nominal strain rate rises from 1times 10minus5 sminus1 to 1times100 sminus1 the damaged area and the number of cracks increasegradually When the nominal strain rate is relatively high(er)(eg 1 times 100 sminus1) a lot of areas are damaged in different levelsThe cracks widen and link together forming a crack networksimultaneously
Therefore it can be concluded that with the increase ofloading velocity the nominal strain rate increases gradually
Shock and Vibration 13
Table 2 Dynamic compressive strength of concrete under different end friction coefficients
120583Dynamic compressive strength [MPa]
1 times 10minus5 sminus1 1 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1 1 times 100 sminus1
0 793 806 858 919 1042 1197 153901 829 838 906 977 1113 1297 161202 846 857 926 1007 1137 1349 168203 849 864 939 1016 1167 1355 169606 857 877 955 1036 1175 1382 173608 860 881 962 1042 1185 1391 1745infin 875 892 980 1067 1212 1406 1749
and the number of cracks or damaged zones increases whenthe apparent compressive strength of concrete is reachedTheenergy consumption of the loading process increases corre-spondinglyThis should be the major reason for the improve-ment of dynamic compressive strength of concrete materials
It can be found obviously from the comparison amongFigures 10(a)ndash10(d) that the damage states of concrete spec-imens are diverse at their peak stresses for different endfriction conditions
Compared with the concrete specimen without end fric-tion confinement (ie 120583 = 0) the deformation at the end ofthe specimen considering the effect of end friction (ie120583 gt 0)was obviously hindered In addition with the increase of endfriction coefficient the obstruction degree of deformationraises For the specimen with the two ends completely fixed(ie 120583 = infin) there is no horizontal deformation at the endsmaking the confinement effect very strong
From Figure 10 one can note that a larger end frictioncoefficient leads to a lower damage level in the top and bottomof the specimen with a constant nominal strain rate Forlarger end friction coefficient the damaged areas draw closeto the central section from the top and bottom of the concretespecimenThese phenomena should generate due to the effectof the end friction confinement which changes the uniaxialloading state in the local regions of concrete These can alsobe illustrated from the simulation results in Figures 8 and 9
42 Effect of End Friction Confinement on Dynamic Compres-sive Strength The macroscopic nominal compressive stress-strain curves of the concrete specimen under different strainrates and end friction coefficients are plotted and compared inFigure 11 Moreover the corresponding peak stresses that isthe nominal dynamic compressive strengths of concrete arereported in Table 2 Obviously both the stress-strain curvesof concrete in Figure 11 and the axial dynamic compressivestrengths in Table 2 demonstrate the effects of strain rates andend friction coefficients
It can be noted obviously from Figure 11 and Table 2 thatthe dynamic uniaxial compressive strength of concrete isimproved due to the end friction confinement effect Further-more under the same strain rates the ascending curves of theconcrete sample with various friction coefficients are almostoverlapped indicating that the elastic modulus of concreteis almost not influenced by the end friction confinementeffect The obtained compressive strengths and the softening
curves are distinct significantly because the stresses andstrains status as well as the fracture paths within the concretespecimen for different friction coefficients vary
For various strain rates the quantitative relationshipsbetween the obtained dynamic compressive strengths of theconcrete specimen and end friction coefficient are presentedin Figures 12(a) and 12(b) It can be seen clearly fromFigure 12 that the concrete dynamic compressive strengthincreases with the increase of end friction coefficient Whenthe end friction coefficient 120583 grows from 0 to 03 the uniaxialcompressive strength increases rapidly while the uniaxialdynamic compressive strength increases slightly and thengets to be stable when the end friction coefficient exceeds 03This is to say when the end friction coefficient exceeds 03 theend confinement effect on the dynamic compressivemechan-ical behavior of concrete can be ignored This can also beconcluded from the analysis resultsmentioned previously forexample the damage factor distribution of concrete pre-sented in Figure 10
Furthermore the results about the effect of end frictionconfinement on concrete dynamic compressive strength atmedium and low strain rates are similar to those at high strainrate For more information about the end confinement effectfor high strain rate refer to Li et al [40]
Figure 13 presents the damage distribution within theconcrete specimens at their corresponding peak stressesunder different end friction confinement conditions at thesame loading velocities Figure 13(a) shows the results for theloading condition of a relative lower strain rate that is 120576 = 1 times10minus2 sminus1 One can note that for ldquopurerdquo uniaxial compressivebehavior of concrete (ie the end friction 120583 between theconcrete specimen and the rigid block is zero 120583 = 0) thenumber of cracks generated or the damage degree withinthe specimen is very limited when reaching the compressivestrength of the concrete sample With the increase of endfriction coefficient for example 120583 = 01 and 02 the totalnumber of cracks ascends gradually but the number of cracksnear the top and bottom regions of the specimen descendsWhen the end friction coefficient becomes larger than 03(eg 120583 = 03 06 08 and infin) the number of cracks turnsto be stable but the width of the cracks broadens as can beseen in Figure 13(a)
Figure 13(b) shows the simulation results for the loadingcondition of a relative higher strain rate that is 120576 = 1 times10minus05 sminus1 For ldquopurerdquo uniaxial compression (ie the end
14 Shock and Vibration
7252015
9
Quasistatic loading
8
95
85
752515
Dynamic loading
20
Dynamic loading
20
10
9
8
25 30 35302520
11
10
9
8
Dynamic loading
Dynamic loading Dynamic loading= 1 times 10minus1 sminus1
= 1 times 10minus3 sminus1
= 1 times 10minus2 sminus1
= 1 times 10minus5 sminus1
times10minus3
0
3
6
9
12
15
18C
ompr
essiv
e st
ress
(MPa
)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
= 1 times 10minus15 sminus1
= 1 times 10minus05 sminus1
120576
120576
120576
120576
120576
120576
Figure 11 Continued
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
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Shock and Vibration 7
Table 1 Mechanical parameters of the concrete mesocomponentsused in the study
Mortar matrix ITZ AggregateMass density 120588 [kgm3] 275 times 103 275 times 103 288 times 103
Elastic modulus [GPa] 30lowast
25lowast
70lowast
Poissonrsquos ratio 02lowast
022lowast
016lowast
Dilation angle 120595 [∘] 30 30Eccentricity 120578 01 01Shape factor 119870
1198880667 0667
Stress ratio 120590119888119888120590119888
116 116Tensile yield stress 120590
119905[MPa] 143
lowast12lowast
Compressive yield stress 1205901198880
[MPa] 143lowast
12lowast
Ultimate compressive yieldstress 120590cu [MPa] 143 12
Note data with ldquolowastrdquo are quoted from Du et al [12]
a dynamic increase factor (ie the DIF) with respect to strainrate
33 BoundaryLoading Conditions and FE Simulations Toexamine the effects of end friction confinement on themacromechanical behavior of concrete subjected to dynamiccompressive loadings the failure behavior of the concretespecimen was explored The corresponding loading andboundary conditions for the interaction system were illus-trated as follows (1) constant vertical velocity V was appliedon the top surface of the rigid block and the left and rightsides of the specimen are free of stress (2) the movementat the bottom rigid block was fixed at both the vertical andhorizontal directions (3) friction behavior between the twoblocks and the concrete sample was set The nominal strainrate 120576 is defined as the applied velocity divided by the heightof the specimen that is 120576 = Vℎ where ℎ is the height of thespecimen
In the following simulations ABAQUS increased auto-matically the size of step time going from smaller one to themaximumauthorized defined by the user For all the concretespecimens the numerical simulations were performed in aplane strain condition
34 Verification of the Mesoscale Approach In reality theavailable tests on loading rate effect of concrete are not veryrich and the test data is also not complete Comparativelyspeaking Dilger et alrsquos [14] test data is the most completeone and it is often used to verify the reliability of the analysismethod or model such as in [26]
To illustrate the reliability and accuracy of the presentmesoscale simulation method Dilger et alrsquos [14] test on thedynamic uniaxial compressive behavior of concrete was alsoselected for the comparison in this section In Dilger et alrsquos[14] experiment the macroscopic mechanical behavior ofconcrete under different nominal strain rates (ie the strainrates of 333 times 10minus5 sminus1 333 times 10minus3 sminus1 and 02 sminus1) was
explored and the complete compressive stress-strain curvesof concrete were obtained
In the previouswork [33] a series of dynamic compressivetest of concrete under different strain rates were conductedbased on the present mesoscale mechanical method includ-ing 120576 = 333 times 10minus5 sminus1 1 times 10minus4 sminus1 333 times 10minus3 sminus1 1 times 10minus2 sminus15 times 10minus2 sminus1 02 sminus1 1 sminus1 100 sminus1 and 200 sminus1 It is to benoted that in the simulations the concrete specimens werefixed at one end and loaded longitudinally through an appliedconstant velocity at the other end The detailed mechanicalparameters and analysis method can refer to [33]
Figure 5 presents the failure patterns of the concretespecimen subjected to different nominal strain rates Onecan notice that with the increase of strain rate the numberof cracks (ie the red damaged region) increases obviouslyand the crack branching behavior occurs Therefore withthe increase of strain rate the fracture of concrete requiresmore energy demand to reach failure which should be themain reason for the improvement of the dynamic strength ofconcrete
Figure 6(a) reports the comparison between the sim-ulations results (solid curves) and the experimental data(symbols) in terms of nominal stress (applied forces dividedby the specimen cross sectional area) versus nominal strain(the displacement generated at the applied-load end dividedby the length of the specimen) curves and the agreementis very good It should be noted herein that as mentionedpreviously the relatedmechanical and physical parameters ofthe concrete mixture used in the test are not full especiallythe mechanical parameters of the ITZ Accordingly in thepreviouswork [33] themechanical parameters (especially theelasticmodulus and the strength) of the ITZwere determinedby the inversion method on the basis of only two strainrates (333 times 10minus5 sminus1 and 333 times 10minus3 sminus1) The simulationof the third available strain (ie 02 sminus1) can be regarded asa validation of the ability of the model to predict concretestrength outside the range of strain rates used for calibrationThis treatment is similar to that in [26]
Furthermore the compressive DIFs were evaluatedaccording to the simulation results and the comparison of thepresent simulation results and some available experimentalobservations is plotted in Figure 6(b) It can be observedthat the present simulation results agree very well with thecollective experimental data This indicates that the presentanalysis method can well simulate the dynamic compressivebehavior of concrete The validated mesoscale mechanicalapproach would be employed in the following simulations tostudy the effect of end friction confinement on the dynamiccompressive behavior of concrete
4 Dynamic Compressive FailureBehavior of Concrete
On the basis of the mesoscale mechanical model describedin Section 3 the simulations of the dynamic axial com-pression of the concrete specimen with various end fric-tion coefficients were implemented The loading velocitiesadopted on the upper rigid block in the simulations are
8 Shock and Vibration
10Damage
120576 = 333 times 10minus5 120576 = 1 times 10minus4 120576 = 333 times 10minus3 120576 = 1 times 10minus2 120576 = 5 times 10minus2
120576 = 2 times 10minus1 120576 = 1 120576 = 100 120576 = 200
Figure 5 Compressive failure patterns of the concrete specimen under different strain rates ranging from 1 times 10minus5 sminus1 to 200 sminus1
Compression test(Dilger et al 1984) and present model
Nom
inal
com
pres
sive
stre
ss (M
Pa)
0002 00030001 0004 0005 00060Compressive strain
0
10
20
30
40
120576 = 333 times 10minus5 sminus1
120576 = 333 times 10minus3 sminus1
120576 = 02 sminus1
(a)
001 1 100
09
12
15
18
21
24
Com
pres
sive D
IF
Test data Present method
1E minus 6 1E minus 4
Strain rate (sminus1)
(b)
Figure 6 (a) Comparison of the present simulation results and Dilger et alrsquos [14] test data and (b) compressive DIFs for the simulation resultsand some available test data
Shock and Vibration 9
Dynamic loading
0
2
4
6
8
10
12
14
Com
pres
sive
stre
ss (M
Pa)
120576 = 1 times 10minus1 sminus1
times10minus3
Mesh size 15mmMesh size 10mmMesh size 05mm
End friction coefficient 120583 = 06
1 432 5 6 70Strain 120576
(a)
Mesh size 15mmMesh size 10mmMesh size 05mm
Damage factor0 1
(b)
Figure 7 (a) The simulation results of three concrete specimens with the same distribution of aggregates and different mesh sizes and(b) damage distribution of the concrete specimens with different mesh sizes under the same strain rate and friction coefficients at theirpeak stresses
V = 15 times 10minus6ms 15 times 10minus4ms 15 times 10minus3ms 15 times
10minus25ms 15 times 10minus2ms 15 times 10minus15ms and 15 times 10minus1msin an ascending sequence and in every loading cycle the con-stant velocity was utilized The corresponding macroscopicnominal strain rates are 120576 = 1 times 10minus5 sminus1 (quasistatic) 1 times10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1and 1 times 100 sminus1 respectively Moreover as mentioned previ-ously the seven end friction coefficients 120583 considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces of thespecimenwere fixed in the horizontal direction) respectively
To check the mesh sensitivity in the simulations threedifferentmesh sizeswere utilized that is 05mm 10mm and
15mm Figure 7(a) presents the nominal compressive stress-strain curves of the concrete specimen subjected to a nominalstrain rate of 01 sminus1 with the same end friction coefficientand the three different mesh sizes It can be found clearlyfrom Figure 7(a) that the mesh sizes (ie 05mm 10mmand 15mm) have less influence on the stress-strain curvesThe three curves are also overlapped Figure 7(b) shows thedamage distribution of the three concrete specimens men-tioned above with the same distribution of aggregates Onecannotice that the failure patterns of the three specimenswithdifferent mesh sizes are closely similar to each other Conse-quently the mesh size of 15mm was used in the followingsimulations
10 Shock and Vibration
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
Equivalent plastic strain times10minus300 56
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
120576
120576
120576
120576
120576
Figure 8 Equivalent plastic strain distribution within the concrete specimen under different strain rates and end friction coefficients at theirpeak compressive stresses
41 Effects of Strain Rate and End Friction Confinement onFailure Patterns of Concrete Figure 8 presents the equivalentplastic strain distribution within the concrete specimensunder five groups of different strain rates ( 120576 = 1 times 10minus5 sminus11 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus1 sminus1 and 1 times 100 sminus1) and fourgroups of different friction coefficients (120583 = 0 03 08 andinfin) at their peak compressive stresses (ie the compressivestrength) One can note from Figures 8(a)ndash8(d) that for thespecimen with the same friction coefficient with the increase
of nominal strain rate the equivalent plastic strain withinconcrete increases obviously In addition as the frictioncoefficient 120583 increases from 0 to infin the equivalent plasticstrain within concrete at reaching the peak stress varies
For the specimenwith the friction coefficient of 0 and 03the obtained plastic strain distributions within the concretespecimens are obviously different For the one with the fric-tion coefficient of 03 and 08 the obtained plastic strain dis-tributions are slightly different And for that with the friction
Shock and Vibration 11
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
000 49
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Maximum principal stress (MPa)
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 9 Maximum principal stress distribution within the concrete specimen under different strain rates and end friction coefficients attheir peak compressive stresses
coefficient of 08 andinfin the obtained plastic strain distribu-tions are almost totally consistent That is to say when thefriction coefficient becomes larger than 08 the effect of endfriction confinement on the failure patterns of concrete canbe ignored
The maximum principal stress distributions within theconcrete specimens under the five groups of different strainrates and the four different friction coefficients at the peakcompressive stresses are presented in Figure 9 It can be
noted intuitively from Figure 9 that the changes of nominalstrain rate and friction coefficient have a significant influenceon the maximum principal stress distribution of the speci-menWith the increase of end friction coefficient the value ofmaximum principal stress gets large and the distribution areadraws close to central section from the top and bottom of theconcrete specimen respectively at same loading velocity
The damage (ie the cracks) distributions within theconcrete specimens corresponding to Figures 8 and 9 are
12 Shock and Vibration
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
0 1
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Damage factor
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 10 Damage distribution within the concrete specimens under different strain rates and friction coefficients at their peak stresses
presented in Figure 10 for different loading velocities anddifferent end friction coefficients In Figure 10 differentcolors represent different damage indexes The red colordenotes the most serious damage while the blue color meansthat no damage generates The white rounded areas whichare regarded as aggregates in these models have no damage
It can be noticed clearly from Figure 10 that the damagedareas increase with the growth of nominal strain rate Whenthe nominal strain rate is relatively low(er) (eg 1 times 10minus5 sminus1)the damaged area of the specimens is small when reaching
their peak stress Accordingly the damage regions (iecracks) are narrow and short and the number of cracks islimited As the nominal strain rate rises from 1times 10minus5 sminus1 to 1times100 sminus1 the damaged area and the number of cracks increasegradually When the nominal strain rate is relatively high(er)(eg 1 times 100 sminus1) a lot of areas are damaged in different levelsThe cracks widen and link together forming a crack networksimultaneously
Therefore it can be concluded that with the increase ofloading velocity the nominal strain rate increases gradually
Shock and Vibration 13
Table 2 Dynamic compressive strength of concrete under different end friction coefficients
120583Dynamic compressive strength [MPa]
1 times 10minus5 sminus1 1 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1 1 times 100 sminus1
0 793 806 858 919 1042 1197 153901 829 838 906 977 1113 1297 161202 846 857 926 1007 1137 1349 168203 849 864 939 1016 1167 1355 169606 857 877 955 1036 1175 1382 173608 860 881 962 1042 1185 1391 1745infin 875 892 980 1067 1212 1406 1749
and the number of cracks or damaged zones increases whenthe apparent compressive strength of concrete is reachedTheenergy consumption of the loading process increases corre-spondinglyThis should be the major reason for the improve-ment of dynamic compressive strength of concrete materials
It can be found obviously from the comparison amongFigures 10(a)ndash10(d) that the damage states of concrete spec-imens are diverse at their peak stresses for different endfriction conditions
Compared with the concrete specimen without end fric-tion confinement (ie 120583 = 0) the deformation at the end ofthe specimen considering the effect of end friction (ie120583 gt 0)was obviously hindered In addition with the increase of endfriction coefficient the obstruction degree of deformationraises For the specimen with the two ends completely fixed(ie 120583 = infin) there is no horizontal deformation at the endsmaking the confinement effect very strong
From Figure 10 one can note that a larger end frictioncoefficient leads to a lower damage level in the top and bottomof the specimen with a constant nominal strain rate Forlarger end friction coefficient the damaged areas draw closeto the central section from the top and bottom of the concretespecimenThese phenomena should generate due to the effectof the end friction confinement which changes the uniaxialloading state in the local regions of concrete These can alsobe illustrated from the simulation results in Figures 8 and 9
42 Effect of End Friction Confinement on Dynamic Compres-sive Strength The macroscopic nominal compressive stress-strain curves of the concrete specimen under different strainrates and end friction coefficients are plotted and compared inFigure 11 Moreover the corresponding peak stresses that isthe nominal dynamic compressive strengths of concrete arereported in Table 2 Obviously both the stress-strain curvesof concrete in Figure 11 and the axial dynamic compressivestrengths in Table 2 demonstrate the effects of strain rates andend friction coefficients
It can be noted obviously from Figure 11 and Table 2 thatthe dynamic uniaxial compressive strength of concrete isimproved due to the end friction confinement effect Further-more under the same strain rates the ascending curves of theconcrete sample with various friction coefficients are almostoverlapped indicating that the elastic modulus of concreteis almost not influenced by the end friction confinementeffect The obtained compressive strengths and the softening
curves are distinct significantly because the stresses andstrains status as well as the fracture paths within the concretespecimen for different friction coefficients vary
For various strain rates the quantitative relationshipsbetween the obtained dynamic compressive strengths of theconcrete specimen and end friction coefficient are presentedin Figures 12(a) and 12(b) It can be seen clearly fromFigure 12 that the concrete dynamic compressive strengthincreases with the increase of end friction coefficient Whenthe end friction coefficient 120583 grows from 0 to 03 the uniaxialcompressive strength increases rapidly while the uniaxialdynamic compressive strength increases slightly and thengets to be stable when the end friction coefficient exceeds 03This is to say when the end friction coefficient exceeds 03 theend confinement effect on the dynamic compressivemechan-ical behavior of concrete can be ignored This can also beconcluded from the analysis resultsmentioned previously forexample the damage factor distribution of concrete pre-sented in Figure 10
Furthermore the results about the effect of end frictionconfinement on concrete dynamic compressive strength atmedium and low strain rates are similar to those at high strainrate For more information about the end confinement effectfor high strain rate refer to Li et al [40]
Figure 13 presents the damage distribution within theconcrete specimens at their corresponding peak stressesunder different end friction confinement conditions at thesame loading velocities Figure 13(a) shows the results for theloading condition of a relative lower strain rate that is 120576 = 1 times10minus2 sminus1 One can note that for ldquopurerdquo uniaxial compressivebehavior of concrete (ie the end friction 120583 between theconcrete specimen and the rigid block is zero 120583 = 0) thenumber of cracks generated or the damage degree withinthe specimen is very limited when reaching the compressivestrength of the concrete sample With the increase of endfriction coefficient for example 120583 = 01 and 02 the totalnumber of cracks ascends gradually but the number of cracksnear the top and bottom regions of the specimen descendsWhen the end friction coefficient becomes larger than 03(eg 120583 = 03 06 08 and infin) the number of cracks turnsto be stable but the width of the cracks broadens as can beseen in Figure 13(a)
Figure 13(b) shows the simulation results for the loadingcondition of a relative higher strain rate that is 120576 = 1 times10minus05 sminus1 For ldquopurerdquo uniaxial compression (ie the end
14 Shock and Vibration
7252015
9
Quasistatic loading
8
95
85
752515
Dynamic loading
20
Dynamic loading
20
10
9
8
25 30 35302520
11
10
9
8
Dynamic loading
Dynamic loading Dynamic loading= 1 times 10minus1 sminus1
= 1 times 10minus3 sminus1
= 1 times 10minus2 sminus1
= 1 times 10minus5 sminus1
times10minus3
0
3
6
9
12
15
18C
ompr
essiv
e st
ress
(MPa
)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
= 1 times 10minus15 sminus1
= 1 times 10minus05 sminus1
120576
120576
120576
120576
120576
120576
Figure 11 Continued
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
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International Journal of
8 Shock and Vibration
10Damage
120576 = 333 times 10minus5 120576 = 1 times 10minus4 120576 = 333 times 10minus3 120576 = 1 times 10minus2 120576 = 5 times 10minus2
120576 = 2 times 10minus1 120576 = 1 120576 = 100 120576 = 200
Figure 5 Compressive failure patterns of the concrete specimen under different strain rates ranging from 1 times 10minus5 sminus1 to 200 sminus1
Compression test(Dilger et al 1984) and present model
Nom
inal
com
pres
sive
stre
ss (M
Pa)
0002 00030001 0004 0005 00060Compressive strain
0
10
20
30
40
120576 = 333 times 10minus5 sminus1
120576 = 333 times 10minus3 sminus1
120576 = 02 sminus1
(a)
001 1 100
09
12
15
18
21
24
Com
pres
sive D
IF
Test data Present method
1E minus 6 1E minus 4
Strain rate (sminus1)
(b)
Figure 6 (a) Comparison of the present simulation results and Dilger et alrsquos [14] test data and (b) compressive DIFs for the simulation resultsand some available test data
Shock and Vibration 9
Dynamic loading
0
2
4
6
8
10
12
14
Com
pres
sive
stre
ss (M
Pa)
120576 = 1 times 10minus1 sminus1
times10minus3
Mesh size 15mmMesh size 10mmMesh size 05mm
End friction coefficient 120583 = 06
1 432 5 6 70Strain 120576
(a)
Mesh size 15mmMesh size 10mmMesh size 05mm
Damage factor0 1
(b)
Figure 7 (a) The simulation results of three concrete specimens with the same distribution of aggregates and different mesh sizes and(b) damage distribution of the concrete specimens with different mesh sizes under the same strain rate and friction coefficients at theirpeak stresses
V = 15 times 10minus6ms 15 times 10minus4ms 15 times 10minus3ms 15 times
10minus25ms 15 times 10minus2ms 15 times 10minus15ms and 15 times 10minus1msin an ascending sequence and in every loading cycle the con-stant velocity was utilized The corresponding macroscopicnominal strain rates are 120576 = 1 times 10minus5 sminus1 (quasistatic) 1 times10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1and 1 times 100 sminus1 respectively Moreover as mentioned previ-ously the seven end friction coefficients 120583 considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces of thespecimenwere fixed in the horizontal direction) respectively
To check the mesh sensitivity in the simulations threedifferentmesh sizeswere utilized that is 05mm 10mm and
15mm Figure 7(a) presents the nominal compressive stress-strain curves of the concrete specimen subjected to a nominalstrain rate of 01 sminus1 with the same end friction coefficientand the three different mesh sizes It can be found clearlyfrom Figure 7(a) that the mesh sizes (ie 05mm 10mmand 15mm) have less influence on the stress-strain curvesThe three curves are also overlapped Figure 7(b) shows thedamage distribution of the three concrete specimens men-tioned above with the same distribution of aggregates Onecannotice that the failure patterns of the three specimenswithdifferent mesh sizes are closely similar to each other Conse-quently the mesh size of 15mm was used in the followingsimulations
10 Shock and Vibration
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
Equivalent plastic strain times10minus300 56
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
120576
120576
120576
120576
120576
Figure 8 Equivalent plastic strain distribution within the concrete specimen under different strain rates and end friction coefficients at theirpeak compressive stresses
41 Effects of Strain Rate and End Friction Confinement onFailure Patterns of Concrete Figure 8 presents the equivalentplastic strain distribution within the concrete specimensunder five groups of different strain rates ( 120576 = 1 times 10minus5 sminus11 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus1 sminus1 and 1 times 100 sminus1) and fourgroups of different friction coefficients (120583 = 0 03 08 andinfin) at their peak compressive stresses (ie the compressivestrength) One can note from Figures 8(a)ndash8(d) that for thespecimen with the same friction coefficient with the increase
of nominal strain rate the equivalent plastic strain withinconcrete increases obviously In addition as the frictioncoefficient 120583 increases from 0 to infin the equivalent plasticstrain within concrete at reaching the peak stress varies
For the specimenwith the friction coefficient of 0 and 03the obtained plastic strain distributions within the concretespecimens are obviously different For the one with the fric-tion coefficient of 03 and 08 the obtained plastic strain dis-tributions are slightly different And for that with the friction
Shock and Vibration 11
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
000 49
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Maximum principal stress (MPa)
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 9 Maximum principal stress distribution within the concrete specimen under different strain rates and end friction coefficients attheir peak compressive stresses
coefficient of 08 andinfin the obtained plastic strain distribu-tions are almost totally consistent That is to say when thefriction coefficient becomes larger than 08 the effect of endfriction confinement on the failure patterns of concrete canbe ignored
The maximum principal stress distributions within theconcrete specimens under the five groups of different strainrates and the four different friction coefficients at the peakcompressive stresses are presented in Figure 9 It can be
noted intuitively from Figure 9 that the changes of nominalstrain rate and friction coefficient have a significant influenceon the maximum principal stress distribution of the speci-menWith the increase of end friction coefficient the value ofmaximum principal stress gets large and the distribution areadraws close to central section from the top and bottom of theconcrete specimen respectively at same loading velocity
The damage (ie the cracks) distributions within theconcrete specimens corresponding to Figures 8 and 9 are
12 Shock and Vibration
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
0 1
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Damage factor
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 10 Damage distribution within the concrete specimens under different strain rates and friction coefficients at their peak stresses
presented in Figure 10 for different loading velocities anddifferent end friction coefficients In Figure 10 differentcolors represent different damage indexes The red colordenotes the most serious damage while the blue color meansthat no damage generates The white rounded areas whichare regarded as aggregates in these models have no damage
It can be noticed clearly from Figure 10 that the damagedareas increase with the growth of nominal strain rate Whenthe nominal strain rate is relatively low(er) (eg 1 times 10minus5 sminus1)the damaged area of the specimens is small when reaching
their peak stress Accordingly the damage regions (iecracks) are narrow and short and the number of cracks islimited As the nominal strain rate rises from 1times 10minus5 sminus1 to 1times100 sminus1 the damaged area and the number of cracks increasegradually When the nominal strain rate is relatively high(er)(eg 1 times 100 sminus1) a lot of areas are damaged in different levelsThe cracks widen and link together forming a crack networksimultaneously
Therefore it can be concluded that with the increase ofloading velocity the nominal strain rate increases gradually
Shock and Vibration 13
Table 2 Dynamic compressive strength of concrete under different end friction coefficients
120583Dynamic compressive strength [MPa]
1 times 10minus5 sminus1 1 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1 1 times 100 sminus1
0 793 806 858 919 1042 1197 153901 829 838 906 977 1113 1297 161202 846 857 926 1007 1137 1349 168203 849 864 939 1016 1167 1355 169606 857 877 955 1036 1175 1382 173608 860 881 962 1042 1185 1391 1745infin 875 892 980 1067 1212 1406 1749
and the number of cracks or damaged zones increases whenthe apparent compressive strength of concrete is reachedTheenergy consumption of the loading process increases corre-spondinglyThis should be the major reason for the improve-ment of dynamic compressive strength of concrete materials
It can be found obviously from the comparison amongFigures 10(a)ndash10(d) that the damage states of concrete spec-imens are diverse at their peak stresses for different endfriction conditions
Compared with the concrete specimen without end fric-tion confinement (ie 120583 = 0) the deformation at the end ofthe specimen considering the effect of end friction (ie120583 gt 0)was obviously hindered In addition with the increase of endfriction coefficient the obstruction degree of deformationraises For the specimen with the two ends completely fixed(ie 120583 = infin) there is no horizontal deformation at the endsmaking the confinement effect very strong
From Figure 10 one can note that a larger end frictioncoefficient leads to a lower damage level in the top and bottomof the specimen with a constant nominal strain rate Forlarger end friction coefficient the damaged areas draw closeto the central section from the top and bottom of the concretespecimenThese phenomena should generate due to the effectof the end friction confinement which changes the uniaxialloading state in the local regions of concrete These can alsobe illustrated from the simulation results in Figures 8 and 9
42 Effect of End Friction Confinement on Dynamic Compres-sive Strength The macroscopic nominal compressive stress-strain curves of the concrete specimen under different strainrates and end friction coefficients are plotted and compared inFigure 11 Moreover the corresponding peak stresses that isthe nominal dynamic compressive strengths of concrete arereported in Table 2 Obviously both the stress-strain curvesof concrete in Figure 11 and the axial dynamic compressivestrengths in Table 2 demonstrate the effects of strain rates andend friction coefficients
It can be noted obviously from Figure 11 and Table 2 thatthe dynamic uniaxial compressive strength of concrete isimproved due to the end friction confinement effect Further-more under the same strain rates the ascending curves of theconcrete sample with various friction coefficients are almostoverlapped indicating that the elastic modulus of concreteis almost not influenced by the end friction confinementeffect The obtained compressive strengths and the softening
curves are distinct significantly because the stresses andstrains status as well as the fracture paths within the concretespecimen for different friction coefficients vary
For various strain rates the quantitative relationshipsbetween the obtained dynamic compressive strengths of theconcrete specimen and end friction coefficient are presentedin Figures 12(a) and 12(b) It can be seen clearly fromFigure 12 that the concrete dynamic compressive strengthincreases with the increase of end friction coefficient Whenthe end friction coefficient 120583 grows from 0 to 03 the uniaxialcompressive strength increases rapidly while the uniaxialdynamic compressive strength increases slightly and thengets to be stable when the end friction coefficient exceeds 03This is to say when the end friction coefficient exceeds 03 theend confinement effect on the dynamic compressivemechan-ical behavior of concrete can be ignored This can also beconcluded from the analysis resultsmentioned previously forexample the damage factor distribution of concrete pre-sented in Figure 10
Furthermore the results about the effect of end frictionconfinement on concrete dynamic compressive strength atmedium and low strain rates are similar to those at high strainrate For more information about the end confinement effectfor high strain rate refer to Li et al [40]
Figure 13 presents the damage distribution within theconcrete specimens at their corresponding peak stressesunder different end friction confinement conditions at thesame loading velocities Figure 13(a) shows the results for theloading condition of a relative lower strain rate that is 120576 = 1 times10minus2 sminus1 One can note that for ldquopurerdquo uniaxial compressivebehavior of concrete (ie the end friction 120583 between theconcrete specimen and the rigid block is zero 120583 = 0) thenumber of cracks generated or the damage degree withinthe specimen is very limited when reaching the compressivestrength of the concrete sample With the increase of endfriction coefficient for example 120583 = 01 and 02 the totalnumber of cracks ascends gradually but the number of cracksnear the top and bottom regions of the specimen descendsWhen the end friction coefficient becomes larger than 03(eg 120583 = 03 06 08 and infin) the number of cracks turnsto be stable but the width of the cracks broadens as can beseen in Figure 13(a)
Figure 13(b) shows the simulation results for the loadingcondition of a relative higher strain rate that is 120576 = 1 times10minus05 sminus1 For ldquopurerdquo uniaxial compression (ie the end
14 Shock and Vibration
7252015
9
Quasistatic loading
8
95
85
752515
Dynamic loading
20
Dynamic loading
20
10
9
8
25 30 35302520
11
10
9
8
Dynamic loading
Dynamic loading Dynamic loading= 1 times 10minus1 sminus1
= 1 times 10minus3 sminus1
= 1 times 10minus2 sminus1
= 1 times 10minus5 sminus1
times10minus3
0
3
6
9
12
15
18C
ompr
essiv
e st
ress
(MPa
)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
= 1 times 10minus15 sminus1
= 1 times 10minus05 sminus1
120576
120576
120576
120576
120576
120576
Figure 11 Continued
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
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International Journal of
Shock and Vibration 9
Dynamic loading
0
2
4
6
8
10
12
14
Com
pres
sive
stre
ss (M
Pa)
120576 = 1 times 10minus1 sminus1
times10minus3
Mesh size 15mmMesh size 10mmMesh size 05mm
End friction coefficient 120583 = 06
1 432 5 6 70Strain 120576
(a)
Mesh size 15mmMesh size 10mmMesh size 05mm
Damage factor0 1
(b)
Figure 7 (a) The simulation results of three concrete specimens with the same distribution of aggregates and different mesh sizes and(b) damage distribution of the concrete specimens with different mesh sizes under the same strain rate and friction coefficients at theirpeak stresses
V = 15 times 10minus6ms 15 times 10minus4ms 15 times 10minus3ms 15 times
10minus25ms 15 times 10minus2ms 15 times 10minus15ms and 15 times 10minus1msin an ascending sequence and in every loading cycle the con-stant velocity was utilized The corresponding macroscopicnominal strain rates are 120576 = 1 times 10minus5 sminus1 (quasistatic) 1 times10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1and 1 times 100 sminus1 respectively Moreover as mentioned previ-ously the seven end friction coefficients 120583 considered in thefollowing simulations are 00 (completely smooth) 01 0203 06 08 and infin (ie the top and bottom surfaces of thespecimenwere fixed in the horizontal direction) respectively
To check the mesh sensitivity in the simulations threedifferentmesh sizeswere utilized that is 05mm 10mm and
15mm Figure 7(a) presents the nominal compressive stress-strain curves of the concrete specimen subjected to a nominalstrain rate of 01 sminus1 with the same end friction coefficientand the three different mesh sizes It can be found clearlyfrom Figure 7(a) that the mesh sizes (ie 05mm 10mmand 15mm) have less influence on the stress-strain curvesThe three curves are also overlapped Figure 7(b) shows thedamage distribution of the three concrete specimens men-tioned above with the same distribution of aggregates Onecannotice that the failure patterns of the three specimenswithdifferent mesh sizes are closely similar to each other Conse-quently the mesh size of 15mm was used in the followingsimulations
10 Shock and Vibration
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
Equivalent plastic strain times10minus300 56
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
120576
120576
120576
120576
120576
Figure 8 Equivalent plastic strain distribution within the concrete specimen under different strain rates and end friction coefficients at theirpeak compressive stresses
41 Effects of Strain Rate and End Friction Confinement onFailure Patterns of Concrete Figure 8 presents the equivalentplastic strain distribution within the concrete specimensunder five groups of different strain rates ( 120576 = 1 times 10minus5 sminus11 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus1 sminus1 and 1 times 100 sminus1) and fourgroups of different friction coefficients (120583 = 0 03 08 andinfin) at their peak compressive stresses (ie the compressivestrength) One can note from Figures 8(a)ndash8(d) that for thespecimen with the same friction coefficient with the increase
of nominal strain rate the equivalent plastic strain withinconcrete increases obviously In addition as the frictioncoefficient 120583 increases from 0 to infin the equivalent plasticstrain within concrete at reaching the peak stress varies
For the specimenwith the friction coefficient of 0 and 03the obtained plastic strain distributions within the concretespecimens are obviously different For the one with the fric-tion coefficient of 03 and 08 the obtained plastic strain dis-tributions are slightly different And for that with the friction
Shock and Vibration 11
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
000 49
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Maximum principal stress (MPa)
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 9 Maximum principal stress distribution within the concrete specimen under different strain rates and end friction coefficients attheir peak compressive stresses
coefficient of 08 andinfin the obtained plastic strain distribu-tions are almost totally consistent That is to say when thefriction coefficient becomes larger than 08 the effect of endfriction confinement on the failure patterns of concrete canbe ignored
The maximum principal stress distributions within theconcrete specimens under the five groups of different strainrates and the four different friction coefficients at the peakcompressive stresses are presented in Figure 9 It can be
noted intuitively from Figure 9 that the changes of nominalstrain rate and friction coefficient have a significant influenceon the maximum principal stress distribution of the speci-menWith the increase of end friction coefficient the value ofmaximum principal stress gets large and the distribution areadraws close to central section from the top and bottom of theconcrete specimen respectively at same loading velocity
The damage (ie the cracks) distributions within theconcrete specimens corresponding to Figures 8 and 9 are
12 Shock and Vibration
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
0 1
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Damage factor
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 10 Damage distribution within the concrete specimens under different strain rates and friction coefficients at their peak stresses
presented in Figure 10 for different loading velocities anddifferent end friction coefficients In Figure 10 differentcolors represent different damage indexes The red colordenotes the most serious damage while the blue color meansthat no damage generates The white rounded areas whichare regarded as aggregates in these models have no damage
It can be noticed clearly from Figure 10 that the damagedareas increase with the growth of nominal strain rate Whenthe nominal strain rate is relatively low(er) (eg 1 times 10minus5 sminus1)the damaged area of the specimens is small when reaching
their peak stress Accordingly the damage regions (iecracks) are narrow and short and the number of cracks islimited As the nominal strain rate rises from 1times 10minus5 sminus1 to 1times100 sminus1 the damaged area and the number of cracks increasegradually When the nominal strain rate is relatively high(er)(eg 1 times 100 sminus1) a lot of areas are damaged in different levelsThe cracks widen and link together forming a crack networksimultaneously
Therefore it can be concluded that with the increase ofloading velocity the nominal strain rate increases gradually
Shock and Vibration 13
Table 2 Dynamic compressive strength of concrete under different end friction coefficients
120583Dynamic compressive strength [MPa]
1 times 10minus5 sminus1 1 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1 1 times 100 sminus1
0 793 806 858 919 1042 1197 153901 829 838 906 977 1113 1297 161202 846 857 926 1007 1137 1349 168203 849 864 939 1016 1167 1355 169606 857 877 955 1036 1175 1382 173608 860 881 962 1042 1185 1391 1745infin 875 892 980 1067 1212 1406 1749
and the number of cracks or damaged zones increases whenthe apparent compressive strength of concrete is reachedTheenergy consumption of the loading process increases corre-spondinglyThis should be the major reason for the improve-ment of dynamic compressive strength of concrete materials
It can be found obviously from the comparison amongFigures 10(a)ndash10(d) that the damage states of concrete spec-imens are diverse at their peak stresses for different endfriction conditions
Compared with the concrete specimen without end fric-tion confinement (ie 120583 = 0) the deformation at the end ofthe specimen considering the effect of end friction (ie120583 gt 0)was obviously hindered In addition with the increase of endfriction coefficient the obstruction degree of deformationraises For the specimen with the two ends completely fixed(ie 120583 = infin) there is no horizontal deformation at the endsmaking the confinement effect very strong
From Figure 10 one can note that a larger end frictioncoefficient leads to a lower damage level in the top and bottomof the specimen with a constant nominal strain rate Forlarger end friction coefficient the damaged areas draw closeto the central section from the top and bottom of the concretespecimenThese phenomena should generate due to the effectof the end friction confinement which changes the uniaxialloading state in the local regions of concrete These can alsobe illustrated from the simulation results in Figures 8 and 9
42 Effect of End Friction Confinement on Dynamic Compres-sive Strength The macroscopic nominal compressive stress-strain curves of the concrete specimen under different strainrates and end friction coefficients are plotted and compared inFigure 11 Moreover the corresponding peak stresses that isthe nominal dynamic compressive strengths of concrete arereported in Table 2 Obviously both the stress-strain curvesof concrete in Figure 11 and the axial dynamic compressivestrengths in Table 2 demonstrate the effects of strain rates andend friction coefficients
It can be noted obviously from Figure 11 and Table 2 thatthe dynamic uniaxial compressive strength of concrete isimproved due to the end friction confinement effect Further-more under the same strain rates the ascending curves of theconcrete sample with various friction coefficients are almostoverlapped indicating that the elastic modulus of concreteis almost not influenced by the end friction confinementeffect The obtained compressive strengths and the softening
curves are distinct significantly because the stresses andstrains status as well as the fracture paths within the concretespecimen for different friction coefficients vary
For various strain rates the quantitative relationshipsbetween the obtained dynamic compressive strengths of theconcrete specimen and end friction coefficient are presentedin Figures 12(a) and 12(b) It can be seen clearly fromFigure 12 that the concrete dynamic compressive strengthincreases with the increase of end friction coefficient Whenthe end friction coefficient 120583 grows from 0 to 03 the uniaxialcompressive strength increases rapidly while the uniaxialdynamic compressive strength increases slightly and thengets to be stable when the end friction coefficient exceeds 03This is to say when the end friction coefficient exceeds 03 theend confinement effect on the dynamic compressivemechan-ical behavior of concrete can be ignored This can also beconcluded from the analysis resultsmentioned previously forexample the damage factor distribution of concrete pre-sented in Figure 10
Furthermore the results about the effect of end frictionconfinement on concrete dynamic compressive strength atmedium and low strain rates are similar to those at high strainrate For more information about the end confinement effectfor high strain rate refer to Li et al [40]
Figure 13 presents the damage distribution within theconcrete specimens at their corresponding peak stressesunder different end friction confinement conditions at thesame loading velocities Figure 13(a) shows the results for theloading condition of a relative lower strain rate that is 120576 = 1 times10minus2 sminus1 One can note that for ldquopurerdquo uniaxial compressivebehavior of concrete (ie the end friction 120583 between theconcrete specimen and the rigid block is zero 120583 = 0) thenumber of cracks generated or the damage degree withinthe specimen is very limited when reaching the compressivestrength of the concrete sample With the increase of endfriction coefficient for example 120583 = 01 and 02 the totalnumber of cracks ascends gradually but the number of cracksnear the top and bottom regions of the specimen descendsWhen the end friction coefficient becomes larger than 03(eg 120583 = 03 06 08 and infin) the number of cracks turnsto be stable but the width of the cracks broadens as can beseen in Figure 13(a)
Figure 13(b) shows the simulation results for the loadingcondition of a relative higher strain rate that is 120576 = 1 times10minus05 sminus1 For ldquopurerdquo uniaxial compression (ie the end
14 Shock and Vibration
7252015
9
Quasistatic loading
8
95
85
752515
Dynamic loading
20
Dynamic loading
20
10
9
8
25 30 35302520
11
10
9
8
Dynamic loading
Dynamic loading Dynamic loading= 1 times 10minus1 sminus1
= 1 times 10minus3 sminus1
= 1 times 10minus2 sminus1
= 1 times 10minus5 sminus1
times10minus3
0
3
6
9
12
15
18C
ompr
essiv
e st
ress
(MPa
)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
= 1 times 10minus15 sminus1
= 1 times 10minus05 sminus1
120576
120576
120576
120576
120576
120576
Figure 11 Continued
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
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Shock and Vibration
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International Journal of
10 Shock and Vibration
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
Equivalent plastic strain times10minus300 56
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
120576
120576
120576
120576
120576
Figure 8 Equivalent plastic strain distribution within the concrete specimen under different strain rates and end friction coefficients at theirpeak compressive stresses
41 Effects of Strain Rate and End Friction Confinement onFailure Patterns of Concrete Figure 8 presents the equivalentplastic strain distribution within the concrete specimensunder five groups of different strain rates ( 120576 = 1 times 10minus5 sminus11 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus1 sminus1 and 1 times 100 sminus1) and fourgroups of different friction coefficients (120583 = 0 03 08 andinfin) at their peak compressive stresses (ie the compressivestrength) One can note from Figures 8(a)ndash8(d) that for thespecimen with the same friction coefficient with the increase
of nominal strain rate the equivalent plastic strain withinconcrete increases obviously In addition as the frictioncoefficient 120583 increases from 0 to infin the equivalent plasticstrain within concrete at reaching the peak stress varies
For the specimenwith the friction coefficient of 0 and 03the obtained plastic strain distributions within the concretespecimens are obviously different For the one with the fric-tion coefficient of 03 and 08 the obtained plastic strain dis-tributions are slightly different And for that with the friction
Shock and Vibration 11
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
000 49
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Maximum principal stress (MPa)
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 9 Maximum principal stress distribution within the concrete specimen under different strain rates and end friction coefficients attheir peak compressive stresses
coefficient of 08 andinfin the obtained plastic strain distribu-tions are almost totally consistent That is to say when thefriction coefficient becomes larger than 08 the effect of endfriction confinement on the failure patterns of concrete canbe ignored
The maximum principal stress distributions within theconcrete specimens under the five groups of different strainrates and the four different friction coefficients at the peakcompressive stresses are presented in Figure 9 It can be
noted intuitively from Figure 9 that the changes of nominalstrain rate and friction coefficient have a significant influenceon the maximum principal stress distribution of the speci-menWith the increase of end friction coefficient the value ofmaximum principal stress gets large and the distribution areadraws close to central section from the top and bottom of theconcrete specimen respectively at same loading velocity
The damage (ie the cracks) distributions within theconcrete specimens corresponding to Figures 8 and 9 are
12 Shock and Vibration
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
0 1
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Damage factor
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 10 Damage distribution within the concrete specimens under different strain rates and friction coefficients at their peak stresses
presented in Figure 10 for different loading velocities anddifferent end friction coefficients In Figure 10 differentcolors represent different damage indexes The red colordenotes the most serious damage while the blue color meansthat no damage generates The white rounded areas whichare regarded as aggregates in these models have no damage
It can be noticed clearly from Figure 10 that the damagedareas increase with the growth of nominal strain rate Whenthe nominal strain rate is relatively low(er) (eg 1 times 10minus5 sminus1)the damaged area of the specimens is small when reaching
their peak stress Accordingly the damage regions (iecracks) are narrow and short and the number of cracks islimited As the nominal strain rate rises from 1times 10minus5 sminus1 to 1times100 sminus1 the damaged area and the number of cracks increasegradually When the nominal strain rate is relatively high(er)(eg 1 times 100 sminus1) a lot of areas are damaged in different levelsThe cracks widen and link together forming a crack networksimultaneously
Therefore it can be concluded that with the increase ofloading velocity the nominal strain rate increases gradually
Shock and Vibration 13
Table 2 Dynamic compressive strength of concrete under different end friction coefficients
120583Dynamic compressive strength [MPa]
1 times 10minus5 sminus1 1 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1 1 times 100 sminus1
0 793 806 858 919 1042 1197 153901 829 838 906 977 1113 1297 161202 846 857 926 1007 1137 1349 168203 849 864 939 1016 1167 1355 169606 857 877 955 1036 1175 1382 173608 860 881 962 1042 1185 1391 1745infin 875 892 980 1067 1212 1406 1749
and the number of cracks or damaged zones increases whenthe apparent compressive strength of concrete is reachedTheenergy consumption of the loading process increases corre-spondinglyThis should be the major reason for the improve-ment of dynamic compressive strength of concrete materials
It can be found obviously from the comparison amongFigures 10(a)ndash10(d) that the damage states of concrete spec-imens are diverse at their peak stresses for different endfriction conditions
Compared with the concrete specimen without end fric-tion confinement (ie 120583 = 0) the deformation at the end ofthe specimen considering the effect of end friction (ie120583 gt 0)was obviously hindered In addition with the increase of endfriction coefficient the obstruction degree of deformationraises For the specimen with the two ends completely fixed(ie 120583 = infin) there is no horizontal deformation at the endsmaking the confinement effect very strong
From Figure 10 one can note that a larger end frictioncoefficient leads to a lower damage level in the top and bottomof the specimen with a constant nominal strain rate Forlarger end friction coefficient the damaged areas draw closeto the central section from the top and bottom of the concretespecimenThese phenomena should generate due to the effectof the end friction confinement which changes the uniaxialloading state in the local regions of concrete These can alsobe illustrated from the simulation results in Figures 8 and 9
42 Effect of End Friction Confinement on Dynamic Compres-sive Strength The macroscopic nominal compressive stress-strain curves of the concrete specimen under different strainrates and end friction coefficients are plotted and compared inFigure 11 Moreover the corresponding peak stresses that isthe nominal dynamic compressive strengths of concrete arereported in Table 2 Obviously both the stress-strain curvesof concrete in Figure 11 and the axial dynamic compressivestrengths in Table 2 demonstrate the effects of strain rates andend friction coefficients
It can be noted obviously from Figure 11 and Table 2 thatthe dynamic uniaxial compressive strength of concrete isimproved due to the end friction confinement effect Further-more under the same strain rates the ascending curves of theconcrete sample with various friction coefficients are almostoverlapped indicating that the elastic modulus of concreteis almost not influenced by the end friction confinementeffect The obtained compressive strengths and the softening
curves are distinct significantly because the stresses andstrains status as well as the fracture paths within the concretespecimen for different friction coefficients vary
For various strain rates the quantitative relationshipsbetween the obtained dynamic compressive strengths of theconcrete specimen and end friction coefficient are presentedin Figures 12(a) and 12(b) It can be seen clearly fromFigure 12 that the concrete dynamic compressive strengthincreases with the increase of end friction coefficient Whenthe end friction coefficient 120583 grows from 0 to 03 the uniaxialcompressive strength increases rapidly while the uniaxialdynamic compressive strength increases slightly and thengets to be stable when the end friction coefficient exceeds 03This is to say when the end friction coefficient exceeds 03 theend confinement effect on the dynamic compressivemechan-ical behavior of concrete can be ignored This can also beconcluded from the analysis resultsmentioned previously forexample the damage factor distribution of concrete pre-sented in Figure 10
Furthermore the results about the effect of end frictionconfinement on concrete dynamic compressive strength atmedium and low strain rates are similar to those at high strainrate For more information about the end confinement effectfor high strain rate refer to Li et al [40]
Figure 13 presents the damage distribution within theconcrete specimens at their corresponding peak stressesunder different end friction confinement conditions at thesame loading velocities Figure 13(a) shows the results for theloading condition of a relative lower strain rate that is 120576 = 1 times10minus2 sminus1 One can note that for ldquopurerdquo uniaxial compressivebehavior of concrete (ie the end friction 120583 between theconcrete specimen and the rigid block is zero 120583 = 0) thenumber of cracks generated or the damage degree withinthe specimen is very limited when reaching the compressivestrength of the concrete sample With the increase of endfriction coefficient for example 120583 = 01 and 02 the totalnumber of cracks ascends gradually but the number of cracksnear the top and bottom regions of the specimen descendsWhen the end friction coefficient becomes larger than 03(eg 120583 = 03 06 08 and infin) the number of cracks turnsto be stable but the width of the cracks broadens as can beseen in Figure 13(a)
Figure 13(b) shows the simulation results for the loadingcondition of a relative higher strain rate that is 120576 = 1 times10minus05 sminus1 For ldquopurerdquo uniaxial compression (ie the end
14 Shock and Vibration
7252015
9
Quasistatic loading
8
95
85
752515
Dynamic loading
20
Dynamic loading
20
10
9
8
25 30 35302520
11
10
9
8
Dynamic loading
Dynamic loading Dynamic loading= 1 times 10minus1 sminus1
= 1 times 10minus3 sminus1
= 1 times 10minus2 sminus1
= 1 times 10minus5 sminus1
times10minus3
0
3
6
9
12
15
18C
ompr
essiv
e st
ress
(MPa
)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
= 1 times 10minus15 sminus1
= 1 times 10minus05 sminus1
120576
120576
120576
120576
120576
120576
Figure 11 Continued
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
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International Journal of
Shock and Vibration 11
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
000 49
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Maximum principal stress (MPa)
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 9 Maximum principal stress distribution within the concrete specimen under different strain rates and end friction coefficients attheir peak compressive stresses
coefficient of 08 andinfin the obtained plastic strain distribu-tions are almost totally consistent That is to say when thefriction coefficient becomes larger than 08 the effect of endfriction confinement on the failure patterns of concrete canbe ignored
The maximum principal stress distributions within theconcrete specimens under the five groups of different strainrates and the four different friction coefficients at the peakcompressive stresses are presented in Figure 9 It can be
noted intuitively from Figure 9 that the changes of nominalstrain rate and friction coefficient have a significant influenceon the maximum principal stress distribution of the speci-menWith the increase of end friction coefficient the value ofmaximum principal stress gets large and the distribution areadraws close to central section from the top and bottom of theconcrete specimen respectively at same loading velocity
The damage (ie the cracks) distributions within theconcrete specimens corresponding to Figures 8 and 9 are
12 Shock and Vibration
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
0 1
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Damage factor
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 10 Damage distribution within the concrete specimens under different strain rates and friction coefficients at their peak stresses
presented in Figure 10 for different loading velocities anddifferent end friction coefficients In Figure 10 differentcolors represent different damage indexes The red colordenotes the most serious damage while the blue color meansthat no damage generates The white rounded areas whichare regarded as aggregates in these models have no damage
It can be noticed clearly from Figure 10 that the damagedareas increase with the growth of nominal strain rate Whenthe nominal strain rate is relatively low(er) (eg 1 times 10minus5 sminus1)the damaged area of the specimens is small when reaching
their peak stress Accordingly the damage regions (iecracks) are narrow and short and the number of cracks islimited As the nominal strain rate rises from 1times 10minus5 sminus1 to 1times100 sminus1 the damaged area and the number of cracks increasegradually When the nominal strain rate is relatively high(er)(eg 1 times 100 sminus1) a lot of areas are damaged in different levelsThe cracks widen and link together forming a crack networksimultaneously
Therefore it can be concluded that with the increase ofloading velocity the nominal strain rate increases gradually
Shock and Vibration 13
Table 2 Dynamic compressive strength of concrete under different end friction coefficients
120583Dynamic compressive strength [MPa]
1 times 10minus5 sminus1 1 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1 1 times 100 sminus1
0 793 806 858 919 1042 1197 153901 829 838 906 977 1113 1297 161202 846 857 926 1007 1137 1349 168203 849 864 939 1016 1167 1355 169606 857 877 955 1036 1175 1382 173608 860 881 962 1042 1185 1391 1745infin 875 892 980 1067 1212 1406 1749
and the number of cracks or damaged zones increases whenthe apparent compressive strength of concrete is reachedTheenergy consumption of the loading process increases corre-spondinglyThis should be the major reason for the improve-ment of dynamic compressive strength of concrete materials
It can be found obviously from the comparison amongFigures 10(a)ndash10(d) that the damage states of concrete spec-imens are diverse at their peak stresses for different endfriction conditions
Compared with the concrete specimen without end fric-tion confinement (ie 120583 = 0) the deformation at the end ofthe specimen considering the effect of end friction (ie120583 gt 0)was obviously hindered In addition with the increase of endfriction coefficient the obstruction degree of deformationraises For the specimen with the two ends completely fixed(ie 120583 = infin) there is no horizontal deformation at the endsmaking the confinement effect very strong
From Figure 10 one can note that a larger end frictioncoefficient leads to a lower damage level in the top and bottomof the specimen with a constant nominal strain rate Forlarger end friction coefficient the damaged areas draw closeto the central section from the top and bottom of the concretespecimenThese phenomena should generate due to the effectof the end friction confinement which changes the uniaxialloading state in the local regions of concrete These can alsobe illustrated from the simulation results in Figures 8 and 9
42 Effect of End Friction Confinement on Dynamic Compres-sive Strength The macroscopic nominal compressive stress-strain curves of the concrete specimen under different strainrates and end friction coefficients are plotted and compared inFigure 11 Moreover the corresponding peak stresses that isthe nominal dynamic compressive strengths of concrete arereported in Table 2 Obviously both the stress-strain curvesof concrete in Figure 11 and the axial dynamic compressivestrengths in Table 2 demonstrate the effects of strain rates andend friction coefficients
It can be noted obviously from Figure 11 and Table 2 thatthe dynamic uniaxial compressive strength of concrete isimproved due to the end friction confinement effect Further-more under the same strain rates the ascending curves of theconcrete sample with various friction coefficients are almostoverlapped indicating that the elastic modulus of concreteis almost not influenced by the end friction confinementeffect The obtained compressive strengths and the softening
curves are distinct significantly because the stresses andstrains status as well as the fracture paths within the concretespecimen for different friction coefficients vary
For various strain rates the quantitative relationshipsbetween the obtained dynamic compressive strengths of theconcrete specimen and end friction coefficient are presentedin Figures 12(a) and 12(b) It can be seen clearly fromFigure 12 that the concrete dynamic compressive strengthincreases with the increase of end friction coefficient Whenthe end friction coefficient 120583 grows from 0 to 03 the uniaxialcompressive strength increases rapidly while the uniaxialdynamic compressive strength increases slightly and thengets to be stable when the end friction coefficient exceeds 03This is to say when the end friction coefficient exceeds 03 theend confinement effect on the dynamic compressivemechan-ical behavior of concrete can be ignored This can also beconcluded from the analysis resultsmentioned previously forexample the damage factor distribution of concrete pre-sented in Figure 10
Furthermore the results about the effect of end frictionconfinement on concrete dynamic compressive strength atmedium and low strain rates are similar to those at high strainrate For more information about the end confinement effectfor high strain rate refer to Li et al [40]
Figure 13 presents the damage distribution within theconcrete specimens at their corresponding peak stressesunder different end friction confinement conditions at thesame loading velocities Figure 13(a) shows the results for theloading condition of a relative lower strain rate that is 120576 = 1 times10minus2 sminus1 One can note that for ldquopurerdquo uniaxial compressivebehavior of concrete (ie the end friction 120583 between theconcrete specimen and the rigid block is zero 120583 = 0) thenumber of cracks generated or the damage degree withinthe specimen is very limited when reaching the compressivestrength of the concrete sample With the increase of endfriction coefficient for example 120583 = 01 and 02 the totalnumber of cracks ascends gradually but the number of cracksnear the top and bottom regions of the specimen descendsWhen the end friction coefficient becomes larger than 03(eg 120583 = 03 06 08 and infin) the number of cracks turnsto be stable but the width of the cracks broadens as can beseen in Figure 13(a)
Figure 13(b) shows the simulation results for the loadingcondition of a relative higher strain rate that is 120576 = 1 times10minus05 sminus1 For ldquopurerdquo uniaxial compression (ie the end
14 Shock and Vibration
7252015
9
Quasistatic loading
8
95
85
752515
Dynamic loading
20
Dynamic loading
20
10
9
8
25 30 35302520
11
10
9
8
Dynamic loading
Dynamic loading Dynamic loading= 1 times 10minus1 sminus1
= 1 times 10minus3 sminus1
= 1 times 10minus2 sminus1
= 1 times 10minus5 sminus1
times10minus3
0
3
6
9
12
15
18C
ompr
essiv
e st
ress
(MPa
)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
= 1 times 10minus15 sminus1
= 1 times 10minus05 sminus1
120576
120576
120576
120576
120576
120576
Figure 11 Continued
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
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Shock and Vibration
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International Journal of
12 Shock and Vibration
Incr
easin
g fr
ictio
n co
effici
ent
Increasing strain rate
0 1
(a) 120583 = 0
(b) 120583 = 03
(c) 120583 = 08
(d) 120583 = infin
Damage factor
= 1 times 10minus1 sminus1 = 1 times 100 sminus1= 1 times 10minus3 sminus1 = 1 times 10minus2 sminus1= 1 times 10minus5 sminus1120576
120576
120576
120576
120576
Figure 10 Damage distribution within the concrete specimens under different strain rates and friction coefficients at their peak stresses
presented in Figure 10 for different loading velocities anddifferent end friction coefficients In Figure 10 differentcolors represent different damage indexes The red colordenotes the most serious damage while the blue color meansthat no damage generates The white rounded areas whichare regarded as aggregates in these models have no damage
It can be noticed clearly from Figure 10 that the damagedareas increase with the growth of nominal strain rate Whenthe nominal strain rate is relatively low(er) (eg 1 times 10minus5 sminus1)the damaged area of the specimens is small when reaching
their peak stress Accordingly the damage regions (iecracks) are narrow and short and the number of cracks islimited As the nominal strain rate rises from 1times 10minus5 sminus1 to 1times100 sminus1 the damaged area and the number of cracks increasegradually When the nominal strain rate is relatively high(er)(eg 1 times 100 sminus1) a lot of areas are damaged in different levelsThe cracks widen and link together forming a crack networksimultaneously
Therefore it can be concluded that with the increase ofloading velocity the nominal strain rate increases gradually
Shock and Vibration 13
Table 2 Dynamic compressive strength of concrete under different end friction coefficients
120583Dynamic compressive strength [MPa]
1 times 10minus5 sminus1 1 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1 1 times 100 sminus1
0 793 806 858 919 1042 1197 153901 829 838 906 977 1113 1297 161202 846 857 926 1007 1137 1349 168203 849 864 939 1016 1167 1355 169606 857 877 955 1036 1175 1382 173608 860 881 962 1042 1185 1391 1745infin 875 892 980 1067 1212 1406 1749
and the number of cracks or damaged zones increases whenthe apparent compressive strength of concrete is reachedTheenergy consumption of the loading process increases corre-spondinglyThis should be the major reason for the improve-ment of dynamic compressive strength of concrete materials
It can be found obviously from the comparison amongFigures 10(a)ndash10(d) that the damage states of concrete spec-imens are diverse at their peak stresses for different endfriction conditions
Compared with the concrete specimen without end fric-tion confinement (ie 120583 = 0) the deformation at the end ofthe specimen considering the effect of end friction (ie120583 gt 0)was obviously hindered In addition with the increase of endfriction coefficient the obstruction degree of deformationraises For the specimen with the two ends completely fixed(ie 120583 = infin) there is no horizontal deformation at the endsmaking the confinement effect very strong
From Figure 10 one can note that a larger end frictioncoefficient leads to a lower damage level in the top and bottomof the specimen with a constant nominal strain rate Forlarger end friction coefficient the damaged areas draw closeto the central section from the top and bottom of the concretespecimenThese phenomena should generate due to the effectof the end friction confinement which changes the uniaxialloading state in the local regions of concrete These can alsobe illustrated from the simulation results in Figures 8 and 9
42 Effect of End Friction Confinement on Dynamic Compres-sive Strength The macroscopic nominal compressive stress-strain curves of the concrete specimen under different strainrates and end friction coefficients are plotted and compared inFigure 11 Moreover the corresponding peak stresses that isthe nominal dynamic compressive strengths of concrete arereported in Table 2 Obviously both the stress-strain curvesof concrete in Figure 11 and the axial dynamic compressivestrengths in Table 2 demonstrate the effects of strain rates andend friction coefficients
It can be noted obviously from Figure 11 and Table 2 thatthe dynamic uniaxial compressive strength of concrete isimproved due to the end friction confinement effect Further-more under the same strain rates the ascending curves of theconcrete sample with various friction coefficients are almostoverlapped indicating that the elastic modulus of concreteis almost not influenced by the end friction confinementeffect The obtained compressive strengths and the softening
curves are distinct significantly because the stresses andstrains status as well as the fracture paths within the concretespecimen for different friction coefficients vary
For various strain rates the quantitative relationshipsbetween the obtained dynamic compressive strengths of theconcrete specimen and end friction coefficient are presentedin Figures 12(a) and 12(b) It can be seen clearly fromFigure 12 that the concrete dynamic compressive strengthincreases with the increase of end friction coefficient Whenthe end friction coefficient 120583 grows from 0 to 03 the uniaxialcompressive strength increases rapidly while the uniaxialdynamic compressive strength increases slightly and thengets to be stable when the end friction coefficient exceeds 03This is to say when the end friction coefficient exceeds 03 theend confinement effect on the dynamic compressivemechan-ical behavior of concrete can be ignored This can also beconcluded from the analysis resultsmentioned previously forexample the damage factor distribution of concrete pre-sented in Figure 10
Furthermore the results about the effect of end frictionconfinement on concrete dynamic compressive strength atmedium and low strain rates are similar to those at high strainrate For more information about the end confinement effectfor high strain rate refer to Li et al [40]
Figure 13 presents the damage distribution within theconcrete specimens at their corresponding peak stressesunder different end friction confinement conditions at thesame loading velocities Figure 13(a) shows the results for theloading condition of a relative lower strain rate that is 120576 = 1 times10minus2 sminus1 One can note that for ldquopurerdquo uniaxial compressivebehavior of concrete (ie the end friction 120583 between theconcrete specimen and the rigid block is zero 120583 = 0) thenumber of cracks generated or the damage degree withinthe specimen is very limited when reaching the compressivestrength of the concrete sample With the increase of endfriction coefficient for example 120583 = 01 and 02 the totalnumber of cracks ascends gradually but the number of cracksnear the top and bottom regions of the specimen descendsWhen the end friction coefficient becomes larger than 03(eg 120583 = 03 06 08 and infin) the number of cracks turnsto be stable but the width of the cracks broadens as can beseen in Figure 13(a)
Figure 13(b) shows the simulation results for the loadingcondition of a relative higher strain rate that is 120576 = 1 times10minus05 sminus1 For ldquopurerdquo uniaxial compression (ie the end
14 Shock and Vibration
7252015
9
Quasistatic loading
8
95
85
752515
Dynamic loading
20
Dynamic loading
20
10
9
8
25 30 35302520
11
10
9
8
Dynamic loading
Dynamic loading Dynamic loading= 1 times 10minus1 sminus1
= 1 times 10minus3 sminus1
= 1 times 10minus2 sminus1
= 1 times 10minus5 sminus1
times10minus3
0
3
6
9
12
15
18C
ompr
essiv
e st
ress
(MPa
)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
= 1 times 10minus15 sminus1
= 1 times 10minus05 sminus1
120576
120576
120576
120576
120576
120576
Figure 11 Continued
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
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International Journal of
Shock and Vibration 13
Table 2 Dynamic compressive strength of concrete under different end friction coefficients
120583Dynamic compressive strength [MPa]
1 times 10minus5 sminus1 1 times 10minus3 sminus1 1 times 10minus2 sminus1 1 times 10minus15 sminus1 1 times 10minus1 sminus1 1 times 10minus05 sminus1 1 times 100 sminus1
0 793 806 858 919 1042 1197 153901 829 838 906 977 1113 1297 161202 846 857 926 1007 1137 1349 168203 849 864 939 1016 1167 1355 169606 857 877 955 1036 1175 1382 173608 860 881 962 1042 1185 1391 1745infin 875 892 980 1067 1212 1406 1749
and the number of cracks or damaged zones increases whenthe apparent compressive strength of concrete is reachedTheenergy consumption of the loading process increases corre-spondinglyThis should be the major reason for the improve-ment of dynamic compressive strength of concrete materials
It can be found obviously from the comparison amongFigures 10(a)ndash10(d) that the damage states of concrete spec-imens are diverse at their peak stresses for different endfriction conditions
Compared with the concrete specimen without end fric-tion confinement (ie 120583 = 0) the deformation at the end ofthe specimen considering the effect of end friction (ie120583 gt 0)was obviously hindered In addition with the increase of endfriction coefficient the obstruction degree of deformationraises For the specimen with the two ends completely fixed(ie 120583 = infin) there is no horizontal deformation at the endsmaking the confinement effect very strong
From Figure 10 one can note that a larger end frictioncoefficient leads to a lower damage level in the top and bottomof the specimen with a constant nominal strain rate Forlarger end friction coefficient the damaged areas draw closeto the central section from the top and bottom of the concretespecimenThese phenomena should generate due to the effectof the end friction confinement which changes the uniaxialloading state in the local regions of concrete These can alsobe illustrated from the simulation results in Figures 8 and 9
42 Effect of End Friction Confinement on Dynamic Compres-sive Strength The macroscopic nominal compressive stress-strain curves of the concrete specimen under different strainrates and end friction coefficients are plotted and compared inFigure 11 Moreover the corresponding peak stresses that isthe nominal dynamic compressive strengths of concrete arereported in Table 2 Obviously both the stress-strain curvesof concrete in Figure 11 and the axial dynamic compressivestrengths in Table 2 demonstrate the effects of strain rates andend friction coefficients
It can be noted obviously from Figure 11 and Table 2 thatthe dynamic uniaxial compressive strength of concrete isimproved due to the end friction confinement effect Further-more under the same strain rates the ascending curves of theconcrete sample with various friction coefficients are almostoverlapped indicating that the elastic modulus of concreteis almost not influenced by the end friction confinementeffect The obtained compressive strengths and the softening
curves are distinct significantly because the stresses andstrains status as well as the fracture paths within the concretespecimen for different friction coefficients vary
For various strain rates the quantitative relationshipsbetween the obtained dynamic compressive strengths of theconcrete specimen and end friction coefficient are presentedin Figures 12(a) and 12(b) It can be seen clearly fromFigure 12 that the concrete dynamic compressive strengthincreases with the increase of end friction coefficient Whenthe end friction coefficient 120583 grows from 0 to 03 the uniaxialcompressive strength increases rapidly while the uniaxialdynamic compressive strength increases slightly and thengets to be stable when the end friction coefficient exceeds 03This is to say when the end friction coefficient exceeds 03 theend confinement effect on the dynamic compressivemechan-ical behavior of concrete can be ignored This can also beconcluded from the analysis resultsmentioned previously forexample the damage factor distribution of concrete pre-sented in Figure 10
Furthermore the results about the effect of end frictionconfinement on concrete dynamic compressive strength atmedium and low strain rates are similar to those at high strainrate For more information about the end confinement effectfor high strain rate refer to Li et al [40]
Figure 13 presents the damage distribution within theconcrete specimens at their corresponding peak stressesunder different end friction confinement conditions at thesame loading velocities Figure 13(a) shows the results for theloading condition of a relative lower strain rate that is 120576 = 1 times10minus2 sminus1 One can note that for ldquopurerdquo uniaxial compressivebehavior of concrete (ie the end friction 120583 between theconcrete specimen and the rigid block is zero 120583 = 0) thenumber of cracks generated or the damage degree withinthe specimen is very limited when reaching the compressivestrength of the concrete sample With the increase of endfriction coefficient for example 120583 = 01 and 02 the totalnumber of cracks ascends gradually but the number of cracksnear the top and bottom regions of the specimen descendsWhen the end friction coefficient becomes larger than 03(eg 120583 = 03 06 08 and infin) the number of cracks turnsto be stable but the width of the cracks broadens as can beseen in Figure 13(a)
Figure 13(b) shows the simulation results for the loadingcondition of a relative higher strain rate that is 120576 = 1 times10minus05 sminus1 For ldquopurerdquo uniaxial compression (ie the end
14 Shock and Vibration
7252015
9
Quasistatic loading
8
95
85
752515
Dynamic loading
20
Dynamic loading
20
10
9
8
25 30 35302520
11
10
9
8
Dynamic loading
Dynamic loading Dynamic loading= 1 times 10minus1 sminus1
= 1 times 10minus3 sminus1
= 1 times 10minus2 sminus1
= 1 times 10minus5 sminus1
times10minus3
0
3
6
9
12
15
18C
ompr
essiv
e st
ress
(MPa
)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
= 1 times 10minus15 sminus1
= 1 times 10minus05 sminus1
120576
120576
120576
120576
120576
120576
Figure 11 Continued
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
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Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
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Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
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Chemical EngineeringInternational Journal of Antennas and
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Navigation and Observation
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DistributedSensor Networks
International Journal of
14 Shock and Vibration
7252015
9
Quasistatic loading
8
95
85
752515
Dynamic loading
20
Dynamic loading
20
10
9
8
25 30 35302520
11
10
9
8
Dynamic loading
Dynamic loading Dynamic loading= 1 times 10minus1 sminus1
= 1 times 10minus3 sminus1
= 1 times 10minus2 sminus1
= 1 times 10minus5 sminus1
times10minus3
0
3
6
9
12
15
18C
ompr
essiv
e st
ress
(MPa
)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
times10minus3
3 6 90Strain 120576 times10minus3
3 6 90Strain 120576
= 1 times 10minus15 sminus1
= 1 times 10minus05 sminus1
120576
120576
120576
120576
120576
120576
Figure 11 Continued
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
Shock and Vibration 15
Dynamic loading
Friction coefficient
= 1 times 100 sminus1
120583 = 01
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = 0
120583 = infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3
3 6 90Strain 120576
120576
Figure 11 Dynamic compressive stress-strain curves of concrete under different strain rates and end friction coefficients
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus3 sminus1
1 times 10minus2 sminus1 1 times 10minus5 sminus11 times 10minus15 sminus1
02 04 06 08 1000Friction coefficient 120583
6
7
8
9
10
11
12
(a)
Com
pres
sive s
treng
th (M
Pa)
Strain rate1 times 10minus1 sminus11 times 100 sminus1
1 times 10minus05 sminus1
6
8
10
12
14
16
18
20
02 04 06 08 1000Friction coefficient 120583
(b)
Figure 12 The relationship between the obtained dynamic compressive strengths of concrete and end friction coefficient
friction coefficient 120583 = 0) the cracks generated within thespecimen exhibit a network distribution With the increaseof the end friction coefficient (eg 120583 = 01 and 02) thedamage distribution concentrates on the central section from
the top and bottom of the specimen When the end frictioncoefficient becomes larger than 03 (eg 120583 = 03 06 08 andinfin) the damage distributions within the specimen becomestable For the five end friction coefficients that is 120583 = 03
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
16 Shock and Vibration
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
0 1
Damage factor
(a)
0 1
Damage factor
120583 = 01 120583 = 02 120583 = 03
120583 = 06 120583 = 08
120583 = 00
120583 = infin
(b)
Figure 13 Damage distribution within concretes at their corresponding peak stresses (a) for 120576 = 1 times 10minus2 sminus1 and (b) for 120576 = 1 times 10
minus05 sminus1
06 08 and infin the damage distribution and the damagedegree within the specimen are almost totally the same
According to the above analysis on the simulation resultsit can be concluded that at the medium and low strainrate levels (1 times 10
minus5 sminus1 sim 1 times 100 sminus1) the dynamic axial
compressive strength of concrete increases first (0 le 120583 le 03)and then keeps stable (120583 gt 03) In addition the end frictionconfinement effect changes the local stress distribution withconcrete and the damage pattern
43 Effect of End Friction Confinement on Compressive DIFsLi et al [40] explored the effect of end friction confinementon the dynamic increase factor (DIF) of concrete subjectedto high strain rate ranging from 27 sminus1 to 390 sminus1 and Haoet al [4] explored the one ranging from 10 sminus1 to 590 sminus1Herein the present work concentrates on the one subjected tomedium and low strain rate ranging from 10minus5 sminus1 to 100 sminus1
Seven groups of curves which describe the relationshipof compressive DIFs and nominal strain rate under different
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
International Journal of
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Shock and Vibration
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Civil EngineeringAdvances in
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Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
Shock and Vibration 17
Takeda (1959)Takeda and Tachikawa (1962)Hatano and Tsutsumi (1960)Kvirikadze (1977)
08
10
12
14
16
18
20
22C
ompr
essiv
e D
IF
minus5 minus4 minus3 minus2 minus1 0minus6log( )
Present model (120583 = 0)
120576
(a)
Friction coefficient
Uniaxial compression
Concrete
minus5 minus4 minus3 minus2 minus1 0minus6log( )
120583 = 01
120583 = 0
120583 = 02
120583 = 03
120583 = 06
120583 = 08
120583 = infin
08
10
12
14
16
18
20
22
Com
pres
sive
DIF
120576
(b)
Figure 14 The relationship between the obtained compressive DIFs and strain rate (a) comparison of the present simulation results and theavailable test data and (b) compressive DIFs of concrete under different end friction coefficients
end friction coefficients are obtained as shown in Figure 14It can be found obviously from Figure 14(a) that the presentsimulation results for 120583 = 0 coincide well with the availableexperimental observations The feasibility of the presentmesomechanical method is therefore demonstrated againFigure 14(b) plots the obtained compressive DIFs of concretepossessing various end friction coefficients For the nominalstrain rate 120576 le 1times10
minus3 sminus1 the dynamic compressive strengthof concrete improves slightly While for the nominal strainrate 120576 ge 1 times 10
minus2 sminus1 the dynamic compressive strengthincreases rapidly Exactly for this the effect of end frictionconfinement on the compressive DIFs of concrete with thenominal strain rate of 120576 ge 1 times 10
minus2 sminus1 draws much attentionTo examine the quantitative effect of end friction con-
finement a new factor 120573120583 120576 contribution of end friction
confinement in the improvement of concrete dynamic axialcompressive strength is given in the form of the followingequation
120573120583 120576=
DIF120583 120576minus DIF
0 120576
DIF120583 120576minus 1
(12)
where the subscript 120583 is the end friction coefficient 120576 meansthe nominal strain rate DIF
120583 120576is the dynamic increase factor
for the end friction coefficient 120583 and the nominal strain rate120576 DIF0 120576is the dynamic increase factor when the end friction
coefficient 120583 is equal to zero (ie without considering theeffect of end friction confinement) and the nominal strainrate is 120576
Figure 15(a) shows the quantitative relationships betweenthe friction contribution factor 120573 and end friction coefficient120583 under different nominal strain rates 120576 It can be seen fromFigure 15(a) that when the end friction coefficient 120583 growsfrom01 to 03 the friction contribution factor120573 increases sig-nificantly However as the end friction coefficient grows from03 to infin the friction contribution factor increases slightlyand then gets to be stable In addition one can see fromFigure 15(a) that with the increase of strain rate the frictioncontribution factor decreases especially when the frictioncoefficient exceeds 03
Figure 15(b) plots the relationship between friction con-tribution factor 120573 and nominal strain rate (described bylog( 120576)) under different end friction confinement conditionsWith the increase of nominal strain rate the friction contri-bution factor presents a descending trendMoreover with theincrease of end friction coefficient the descending trend getsto be much more obvious When the strain rate is relativelylower (ie for 120576 = 10minus2 sminus1) the larger the end frictioncoefficient is the larger the friction contribution factor is
For further research considering the extreme situation ofend confinement that is 120583 = infin the ascending parts of theaxial dynamic compressive stress-strain relationship curvesof the concrete specimens are obtained as shown in Figure 16for the relatively low strain rate 120576 = 1 times 10minus2 sminus1 and the rela-tively high strain rate 120576 = 1 times 100 sminus1 In Figure 16 119864
1denotes
the energy consumptionwhen the concrete specimenwithoutconsidering the effect of end friction confinement (ie 120583 = 0)
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
18 Shock and Vibration
Strain rate
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
02 04 06 08 1000Friction coefficient 120583
1 times 10minus2
1 times 10minus11 times 10minus15
1 times 10minus05
1 times 100
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(a)
minus20 minus15 minus10 minus05 00
Friction coefficient
log( 120576)
000
005
010
015
020
025
030
035
Fric
tion
cont
ribut
ion
fact
or 120573
120583 = 01
120583 = 02120583 = 03
120583 = 06
120583 = 08
120583 = infin
120573120583 = (DIF120583 minus DIF0 )(DIF120583 minus 1)120576
120576
120576
120576
(b)
Figure 15 Effects of friction coefficient 120583 and strain rate 120576 on the friction contribution factor 120573 (a) 120573 and 120583 and (b) 120573 and 120576
Friction coefficient
(3)(2)
(3) 120583 (2) 120583(1) 120583
(1)
(1) Quasistatic loading
(2) (3) Dynamic loading= 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
= 1 times 10minus2 sminus1
E1
E2
E3
120576
120576
(a)
(1) Quasistatic loading
(4) (5) Dynamic loading
(5)
(1)
(4)
Friction coefficient(5) 120583 (4) 120583(1) 120583 = 0
= 0
= infin
0
3
6
9
12
15
18
Com
pres
sive
stre
ss (M
Pa)
times10minus3620 4
Strain 120576
= 1 times 10minus5 sminus1
E4
E5
E1
= 1 times 100 sminus1
120576
120576
(b)
Figure 16 The ascending part of concrete dynamic uniaxial compressive stress-strain curves (a) for a lower strain rate of 1 times 10minus2 sminus1 and(b) for a higher strain rate of 1 times 10minus0 sminus1
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
Shock and Vibration 19
reaches its quasistatic nominal compressive strength (thestrain rate 120576 = 1 times 10minus5 sminus1) and its magnitude is equal tothe area occupied by the ascending curve and the horizontalaxial both 119864
2and 119864
4denote the energy consumption for
the strength improvement due to material strain rate effect1198643and 119864
5denote the energy consumption for the strength
improvement due to end friction confinement It can be seenclearly from Figure 16 that
1198643
1198642+ 1198643
gt1198645
1198644+ 1198645
(13)
That is to say when the nominal strain rate is relativelylow(er) (eg 120576 = 1 times 10minus2 sminus1) the contribution of endfriction confinement effect to the enhancement of dynamiccompressive strength is relatively high(er)While the nominalstrain rate is relatively high(er) (eg 120576 = 1 times 100 sminus1) thecontribution of end friction confinement effect to dynamicstrength improvement is relatively low(er) The simulationresults are consistent with those in the work [4]
5 Conclusions
Considering the heterogeneities two-dimensional mesoscalemechanicalmodels of concretewere established to investigatethe quantitative influence of end friction confinement onthe dynamic compressive behavior of concrete specimensunder medium and low strain rates The proposed mesoscaleanalysis method was firstly verified by comparing the presentsimulation results with the available test data In the simula-tions seven groups of friction coefficients namely 00 0102 03 06 08 and infin are taken into account The effectsof end friction confinement on the dynamic failure patternsthe nominal compressive stress-strain relations and the com-pressive DIFs were explored subsequently One can find thatthe friction at the interface of concrete specimen and loadingmeasurement constrains the lateral deformation of the spec-imen and changes the internal stress status and thus it hasa significant influence on the tested DIF Furthermore thefriction contribution factor was proposed and it was used todescribe the quantitatively influence of end friction confine-ment According to the simulations the following conclu-sions can be obtained
(1) At the medium and low strain rate level (1 times
10minus5 sminus1 sim 1times10
0 sminus1) the uniaxial dynamic compres-sive strength increases first (0 le 120583 le 03) and thenkeeps stable (120583 gt 03)
(2) End friction confinement effect changes the uniaxialforce state of local concrete and the failure patternsMeanwhile the concrete uniaxial dynamic compres-sive strength is improved due to the end frictionconfinement effect
(3) For same end friction confinement the friction con-tribution factor decreases with the increase of nomi-nal strain rate (ranging from 1times 10minus2 sminus1 to 1times 100 sminus1)And with the increase of end friction coefficient thedescending trend gets to be obvious
It is to be noted that further studies are still necessary fora fully understanding about the strain-rate effect on the ulti-mate uniaxial compressive strength of concrete and concrete-like materials subjected to dynamic loadings Both tests andsimulations could offermore information to separate pseudo-strain-rate effects from genuine strain-rate effects in dynamicmaterial properties tests which is of significant importancefor material model identification
Conflict of Interests
The authors declare that there is no conflict of interestsregarding the publication of this paper
Acknowledgments
This work was supported by the National Key Basic Researchand Development Program of China (no 2011CB013600)and the Science Fund for Creative Research Groups ofthe National Natural Science Foundation of China (no51421005) The support is gratefully acknowledged
References
[1] H Xu and H M Wen ldquoSemi-empirical equations for thedynamic strength enhancement of concrete-like materialsrdquoInternational Journal of Impact Engineering vol 60 pp 76ndash812013
[2] Q M Li and H Meng ldquoAbout the dynamic strength enhance-ment of concrete-like materials in a split Hopkinson pressurebar testrdquo International Journal of Solids and Structures vol 40no 2 pp 343ndash360 2003
[3] P H Bischoff and S H Perry ldquoCompressive behaviour ofconcrete at high strain ratesrdquo Materials and Structures vol 24no 6 pp 425ndash450 1991
[4] Y Hao H Hao and Z X Li ldquoInfluence of end frictionconfinement on impact tests of concrete material at high strainraterdquo International Journal of Impact Engineering vol 60 pp82ndash106 2013
[5] M J Forrestal T W Wright andW Chen ldquoThe effect of radialinertia on brittle samples during the split Hopkinson pressurebar testrdquo International Journal of Impact Engineering vol 34 no3 pp 405ndash411 2007
[6] Z C Mu A N Dancygier W Zhang and D Z YankelevskyldquoRevisiting the dynamic compressive behavior of concrete-likematerialsrdquo International Journal of Impact Engineering vol 49pp 91ndash102 2012
[7] D J Kim K Sirijaroonchai S E El-Tawil and A NaamanldquoNumerical simulation of the split Hopkinson pressure bartest technique for concrete under compressionrdquo InternationalJournal of Impact Engineering vol 37 no 2 pp 141ndash149 2010
[8] R R Pedersen A Simone and L J Sluys ldquoMesoscopicmodeling and simulation of the dynamic tensile behavior ofconcreterdquo Cement and Concrete Research vol 50 pp 74ndash872013
[9] X Q Zhou and H Hao ldquoMesoscale modelling of concretetensile failure mechanism at high strain ratesrdquo Computers andStructures vol 86 no 21-22 pp 2013ndash2026 2008
[10] XQ Zhou andHHao ldquoModelling of compressive behaviour ofconcrete-likematerials at high strain raterdquo International Journalof Solids and Structures vol 45 no 17 pp 4648ndash4661 2008
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
20 Shock and Vibration
[11] X L Du L Jin and G W Ma ldquoNumerical simulation ofdynamic tensile-failure of concrete at meso-scalerdquo InternationalJournal of Impact Engineering vol 66 pp 5ndash17 2014
[12] X L Du L Jin and R B Zhang ldquoModeling the cracking ofcover concrete due to non-uniform corrosion of reinforcementrdquoCorrosion Science vol 89 pp 189ndash202 2014
[13] S-M Kim and R K Abu Al-Rub ldquoMeso-scale computationalmodeling of the plastic-damage response of cementitious com-positesrdquo Cement and Concrete Research vol 41 no 3 pp 339ndash358 2011
[14] WHDilger R Koch and R Kowalczyk ldquoDuctility of plain andconfined concrete under different strain ratesrdquoACI Journal vol81 no 1 pp 73ndash81 1984
[15] J Lubliner J Oliver S Oller and E Onate ldquoA plastic-damagemodel for concreterdquo International Journal of Solids and Struc-tures vol 25 no 3 pp 299ndash326 1989
[16] J Lee andG L Fenves ldquoPlastic-damagemodel for cyclic loadingof concrete structuresrdquo Journal of Engineering Mechanics vol124 no 8 pp 892ndash900 1998
[17] P Grassl and M Jirasek ldquoDamage-plastic model for concretefailurerdquo International Journal of Solids and Structures vol 43no 22-23 pp 7166ndash7196 2006
[18] P Badel V Godard and J-B Leblond ldquoApplication of someanisotropic damage model to the prediction of the failureof some complex industrial concrete structurerdquo InternationalJournal of Solids and Structures vol 44 no 18-19 pp 5848ndash58742007
[19] Y Huang Z Yang W Ren G Liu and C Zhang ldquo3D meso-scale fracture modelling and validation of concrete based onin-situ X-ray computed tomography images using damageplasticity modelrdquo International Journal of Solids and Structuresvol 67-68 pp 340ndash352 2015
[20] A S Genikomsou and M A Polak ldquoFinite element analysisof punching shear of concrete slabs using damaged plasticitymodel in ABAQUSrdquo Engineering Structures vol 98 pp 38ndash482015
[21] D L Grote S W Park and M Zhou ldquoDynamic behavior ofconcrete at high strain rates and pressures I Experimentalcharacterizationrdquo International Journal of Impact Engineeringvol 25 no 9 pp 869ndash886 2001
[22] SW Park Q Xia andM Zhou ldquoDynamic behavior of concreteat high strain rates and pressures II Numerical simulationrdquoInternational Journal of Impact Engineering vol 25 no 9 pp887ndash910 2001
[23] S Hentz F V Donze and L Daudeville ldquoDiscrete elementmodelling of concrete submitted to dynamic loading at highstrain ratesrdquo Computers amp Structures vol 82 no 29-30 pp2509ndash2524 2004
[24] L J Malvar and C A Ross ldquoReview of strain rate effects forconcrete in tensionrdquo ACI Materials Journal vol 95 no 6 pp735ndash739 1998
[25] X Q Zhou V A Kuznetsov H Hao and JWaschl ldquoNumericalprediction of concrete slab response to blast loadingrdquo Interna-tional Journal of Impact Engineering vol 35 no 10 pp 1186ndash1200 2008
[26] G Cusatis ldquoStrain-rate effects on concrete behaviorrdquo Interna-tional Journal of Impact Engineering vol 38 no 4 pp 162ndash1702011
[27] J Ozbolt A Sharma and H-W Reinhardt ldquoDynamic fractureof concretemdashcompact tension specimenrdquo International Journalof Solids and Structures vol 48 no 10 pp 1534ndash1543 2011
[28] S Pyo and S El-Tawil ldquoCrack velocity-dependent dynamictensile behavior of concreterdquo International Journal of ImpactEngineering vol 55 pp 63ndash70 2013
[29] N Tregger D Corr L Graham-Brady and S Shah ldquoModelingthe effect of mesoscale randomness on concrete fracturerdquoProbabilistic Engineering Mechanics vol 21 no 3 pp 217ndash2252006
[30] W Riedel M Wicklein and K Thoma ldquoShock properties ofconventional and high strength concrete experimental andmesomechanical analysisrdquo International Journal of Impact Engi-neering vol 35 no 3 pp 155ndash171 2008
[31] F Fakhari Tehrani J Absi F Allou and C Petit ldquoHeteroge-neous numerical modeling of asphalt concrete through use ofa biphasic approach porous matrixinclusionsrdquo ComputationalMaterials Science vol 69 pp 186ndash196 2013
[32] F Bernard and S Kamali-Bernard ldquoNumerical study of ITZcontribution on mechanical behavior and diffusivity of mor-tarsrdquo Computational Materials Science vol 102 pp 250ndash2572015
[33] L Jin and X-L Du ldquoEffects of loading rate and its suddenchange on concrete compressive failurerdquo Journal of Vibrationand Shock vol 33 no 19 pp 187ndash193 2014
[34] X L Du L Jin and G W Ma ldquoA meso-scale analysis methodfor the simulation of nonlinear damage and failure behavior ofreinforced concrete membersrdquo International Journal of DamageMechanics vol 22 no 6 pp 878ndash904 2013
[35] L Snozzi A Caballero and J F Molinari ldquoInfluence of themeso-structure in dynamic fracture simulation of concreteunder tensile loadingrdquo Cement and Concrete Research vol 41no 11 pp 1130ndash1142 2011
[36] H-KMan and J GM vanMier ldquoDamage distribution and sizeeffect in numerical concrete from lattice analysesrdquo Cement andConcrete Composites vol 33 no 9 pp 867ndash880 2011
[37] W Y Ren Z J Yang R Sharma C H Zhang and P J WithersldquoTwo-dimensional X-ray CT image based meso-scale fracturemodelling of concreterdquoEngineering FractureMechanics vol 133pp 24ndash39 2015
[38] Y Hao H Hao and X H Zhang ldquoNumerical analysis ofconcrete material properties at high strain rate under directtensionrdquo International Journal of Impact Engineering vol 39 no1 pp 51ndash62 2012
[39] Y Hao and H Hao ldquoNumerical investigation of the dynamiccompressive behaviour of rock materials at high strain raterdquoRock Mechanics and Rock Engineering vol 46 no 2 pp 373ndash388 2013
[40] Q M Li Y B Lu and H Meng ldquoFurther investigation on thedynamic compressive strength enhancement of concrete-likematerials based on split Hopkinson pressure bar tests Part IInumerical simulationsrdquo International Journal of Impact Engi-neering vol 36 no 12 pp 1335ndash1345 2009
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of
International Journal of
AerospaceEngineeringHindawi Publishing Corporationhttpwwwhindawicom Volume 2014
RoboticsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Active and Passive Electronic Components
Control Scienceand Engineering
Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
International Journal of
RotatingMachinery
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporation httpwwwhindawicom
Journal ofEngineeringVolume 2014
Submit your manuscripts athttpwwwhindawicom
VLSI Design
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Shock and Vibration
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Civil EngineeringAdvances in
Acoustics and VibrationAdvances in
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Electrical and Computer Engineering
Journal of
Advances inOptoElectronics
Hindawi Publishing Corporation httpwwwhindawicom
Volume 2014
The Scientific World JournalHindawi Publishing Corporation httpwwwhindawicom Volume 2014
SensorsJournal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Modelling amp Simulation in EngineeringHindawi Publishing Corporation httpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Chemical EngineeringInternational Journal of Antennas and
Propagation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
Navigation and Observation
International Journal of
Hindawi Publishing Corporationhttpwwwhindawicom Volume 2014
DistributedSensor Networks
International Journal of