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This article was downloaded by: [Nova Southeastern University]On: 08 October 2014, At: 06:25Publisher: Taylor & FrancisInforma Ltd Registered in England and Wales Registered Number: 1072954 Registered office: MortimerHouse, 37-41 Mortimer Street, London W1T 3JH, UK
Road Materials and Pavement DesignPublication details, including instructions for authors and subscription information:http://www.tandfonline.com/loi/trmp20
Evaluation of Rut Resistant Asphalt Mixtures forIntersectionElie Y. Hajj a , George Tannoury b & Peter E. Sebaaly aa Pavements/Materials Program, Dept of Civ. & Env. Engineering MS257 , University ofNevada , Reno, NV, 89557, United States E-mail:b Terracon Consulting Engineers and Scientists , Roseville, Kansas, 67209, United StatesE-mail:Published online: 17 Oct 2011.
To cite this article: Elie Y. Hajj , George Tannoury & Peter E. Sebaaly (2011) Evaluation of Rut Resistant Asphalt Mixturesfor Intersection, Road Materials and Pavement Design, 12:2, 263-292
To link to this article: http://dx.doi.org/10.1080/14680629.2011.9695246
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Road Materials and Pavement Design. Volume 12 – No. 2/2011, pages 263 to 292
Evaluation of Rut Resistant Asphalt
Mixtures for Intersection
Elie Y. Hajj*— George Tannoury**— Peter E. Sebaaly*
* Pavements/Materials Program, Dept of Civ. & Env. Engineering MS257
University of Nevada
Reno, NV 89557, United States
** Terracon Consulting Engineers and Scientists
Roseville, Kansas 67209, United States
ABSTRACT. The Nevada Department of Transportation (NDOT) sponsored a two-phase
research study to develop specific requirements to be used for HMA mixes at intersection. The
phase I of the study evaluated the impact of different aggregate gradations on the mixtures’
resistance to rutting. The rutting resistance of a HMA mix was found to be highly dependent
upon the aggregate gradation. The phase II consisted of a laboratory evaluation of the mixes
with the most promising gradations identified in phase I for fatigue cracking resistance.
Additionally, a full mechanistic analysis is conducted to effectively evaluate the relative
fatigue and rutting performances of the evaluated HMA mixes under heavy braking 18-wheel
truck. Based on the data generated in this study a new aggregate specification limit was
recommended for asphalt mixtures at intersections. The recommended gradation is intended
to improve the asphalt mixture’s resistance to rutting without jeopardizing its resistance to
fatigue cracking.
KEYWORDS: Intersection, Rutting, Fatigue, 18-Wheel Truck, Mechanistic Design, 3D-Move.
DOI:10.3166/RMPD.12.263-292 © 2011 Lavoisier, Paris
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264 Road Materials and Pavement Design. Volume 12 – No. 2/2011
1. Introduction
During the last decades there have been dramatic changes in traffic volumes,
traffic weights, and tire pressures, resulting in a significant increase in permanent
deformation of the Hot Mix Asphalt (HMA) pavements. Permanent deformation is a
major mode of failure in flexible pavements consisting of both rutting and shoving.
Typically, a rutting failure alone occurs under traffic loads moving at highway
speed, while both rutting and shoving failure may occur under traffic loads at
intersections. In many instances, the same HMA mixtures that have a history of
good performance in rutting did not perform well at intersections. Permanent
deformation of HMA is a common problem at intersections where the HMA mixture
exhibits lower stiffness when subjected to slow moving or stopped vehicle loads.
This problem is more common in hot climates weather where the stiffness of the
HMA is further decreased with the increase of the pavement temperature.
Additionally, the different behaviour of HMA pavement at intersection is related to
the more complex stresses imposed at the pavement surface layer by the braking,
accelerating and turning movements of heavy loaded trucks. Therefore, different
type of HMA mixtures may be required at intersections from the one used on the
main lane.
Permanent deformation is the largest and the most frequently occurring problem
when dealing with HMA at intersections. Rutting in the HMA layers develops
gradually as the number of load application increases, usually appearing as
longitudinal depressions in the wheel paths accompanied by small upheavals to the
sides. There are three general types of HMA pavement rutting, which are described
below, that can result from different mechanism.
Consolidation can occur when there is insufficient compaction during the
construction of the pavement. An HMA mix with insufficient density is prone to
further compaction under traffic, especially in hot weather and at intersections where
the loads are slow moving or static. With consolidation, a depression occurs in the
wheel path with no humps on either side of that depression. Furthermore, surface
wear takes place because of the surface abrasion under chains and studded tires used
in the winter season (Marker, 1981; Sousa and Weissman, 1994).
Instability of the HMA mixture at intersection is a significant performance
problem that leads to plastic flow at the surface of the pavement. Some of the more
common reasons for mixture instability are: excessive amount of asphalt binder and
insufficient air voids, too much rounded aggregate, or too high of the minus 0.075-
mm material. Plastic flow will normally appear as longitudinal ruts in the pavement
near the centre of the applied load with humps of material on either side of the rut
(Marker, 1981; Sousa and Weissman, 1994).
Lastly, structural rutting results from insufficient structural capacity in the
pavement system and can occur when the strength and/or thickness of the pavement
layers are insufficient to support the design traffic on the existing subgrade. The
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Evaluation of Rut Resistant Asphalt Mixtures for Intersection 265
compaction of the supporting layers results in the development of ruts in the
pavement surface. A rut resulting from this type of action will generally be
accompanied by longitudinal and/or alligator cracking ((Marker, 1981, Sousa and
Weissman, 1994; Rosenberg and Buncher, 1999).
The rutting resistance of an HMA mix is highly dependent upon the integrity of
the aggregate structure. Mr. Robert D. Bailey of the Illinois Department of
Transportation (retired 1997) developed a specific procedure termed “Bailey
method” to select aggregate gradation for asphalt mixtures. This method focused on
creating aggregate structure which facilitates interlock in the coarse aggregate,
resulting in a strong “aggregate skeleton”, and thus providing high shear strength
and rutting resistance in the HMA pavement. Additional information on the Bailey
method can be found in Vavrik et al. (2001 and 2002).
Williams (2003) explored the relationships between HMA mixture properties
and rutting susceptibility as measured under wheel-tracking devices. As a result, an
increase in rut depth was observed with the decrease in VMA. On the other hand, a
decrease in rut depth was observed with the increase in the PG high temperature
binder grade. Additionally, an increase in the asphalt binder content and film
thickness resulted in a reduction in the mixtures’ resistance to rutting. Therefore, it
was concluded that a change in the binder content, binder properties, and/or
aggregates gradation can improve the mixtures’ resistance to rutting while it may
greatly jeopardize its resistance to fatigue and thermal cracking.
In 2003, a study performed by the US Army Corps of Engineers (Partl and
Newman, 2003) pointed out the need for selecting an asphalt modifier that can resist
multiple distresses such as rutting, fatigue, thermal cracking, and moisture damage.
Given the good resistance of polymer-modified binders against rutting, it was found
that the type of polymer might have a significant impact on fatigue properties.
Mixtures contained reactive styrene–butadiene cross-linked polymer exhibited the
highest fatigue life.
In 1996, Harvey and Tsai evaluated the effects of a broad range of asphalt
contents and air-void contents on fatigue life and stiffness for a typical California
mix. It was found that the fatigue life was significantly affected by the strain level,
air-void content, and asphalt content. A higher laboratory fatigue life (i.e. better
fatigue resistance) was observed for lower air-void content and higher asphalt
content. Additionally, a decrease in air-void content and asphalt content resulted in a
significant increase in initial stiffness.
Historical field measurements in Nevada show that a significant number of HMA
pavements carrying very heavy and channelized traffic in southern Nevada are
experiencing severe permanent deformation near signalized intersections. Realizing
the need for different asphalt mixes at or near intersections, the Nevada Department
of Transportation (NDOT) sponsored a two-phase research study at the University
of Nevada to develop specific requirements for HMA mixes at intersections. Phase I
of the study consisted of a post-mortem evaluation of in-service intersections and a
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266 Road Materials and Pavement Design. Volume 12 – No. 2/2011
laboratory evaluation of mixtures with different aggregate gradations in terms of
their resistance to rutting. Phase II of this study consisted of a laboratory evaluation
of the rut resistant HMA mixes identified in phase I for fatigue cracking resistance.
This phase is essential as an improved resistance to rutting of a mixture may
partially jeopardize its resistance to fatigue cracking. In addition, the phase II of the
study included a re-evaluation of the rutting characteristics of the rut resistant mixes
using laboratory techniques proposed by the new AASHTO mechanistic-empirical
pavement design guide (MEPDG) (NCHRP, 2004). Additionally, a full mechanistic
analysis was conducted to effectively evaluate the relative performance of the
evaluated HMA mixes under moving and braking heavy loads.
This paper presents in details the research effort that was conducted under phase
II of the overall research effort with a brief summary of the findings from phase I
that was completed in 2006. More information on phase I can be found in Hajj
(2005) and Sebaaly et al. (2005).
2. Research objective
The overall objective of this research study was to identify an HMA mix with
good resistance to rutting and shoving at intersections. Phase I of this study
evaluated the impact of aggregate gradation on the mixtures resistance to permanent
deformation. The objective of phase II of this study was to evaluate the fatigue
resistance of the rut resistant mixtures identified in phase I. Additionally, the rutting
resistance of the mixes wasre-evaluated according to the test methods referred to in
the new AASHTO Mechanistic Empirical Pavement Design Guide (MEPDG).
3. Findings of phase I
Two laboratory evaluations were conducted: I. Postmortem evaluation of in-
service intersections and II. Laboratory evaluation of mixes with different aggregate
gradations. The full documentation and findings of Phase I are available in
published reports and papers (Sebaaly et al., 2005; Hajj, 2005; Hajj et al., 2007).
The first part of phase I evaluated and compared the volumetric properties of
field cores from rutted and non-rutted intersections in southern Nevada. Several in-
service HMA intersections were identified, some with severe rutting and some
without any rutting failures. Core samples from between the wheel path and
150 meters away from the intersection were obtained from thirteen different projects
in southern Nevada.
The idea behind the sampling plan was that cores from between the wheel path
and away from intersection provide HMA mixes that have not been damaged due to
the traffic loading while the wheel path cores at the intersection represent the
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Evaluation of Rut Resistant Asphalt Mixtures for Intersection 267
damaged mixes. The cores taken were tested for bulk specific gravity and aggregate
gradations. For the projects experiencing severe rutting, the Air Voids (AV) and
voids in the Mineral Aggregate (VMA) were lower at intersection when compared to
the ones at 150meters away from the intersection. The AVs at the intersection were
less than 2.5%, indicating excessive densification of the HMA mixes under heavy
slow/stopped traffic.
Two gradation zones were identified by grouping the extracted aggregate
gradations of the mixes that experienced rutting and mixes that experienced no
rutting. Figure 1 shows that the no rut mixes zones covered denser and coarser
gradations than the rut mixes zones.
Figure 1. Aggregate gradation limits for rut and no rut mixtures from 13 different
projects
Additionally, the field performance of HMA intersections was used in an attempt
to identify a laboratory test that identifies HMA mixes that are prone to permanent
deformation at intersections. To this end, the sampled cores from the various
intersections were tested under the Asphalt Pavement Analyzer (APA) and the
Repeated Shear at Constant Height (RSCH) tests. The analysis of the generated data
led to the conclusion that neither the APA nor the RSCH can be effectively used as a
post-mortem device to explain the performance of HMA mixes at intersections.
In the second part of phase I, five aggregate gradations were used with a PG76-
22 polymer-modified asphalt binder and were evaluated in the laboratory for rutting
resistance.
– No Rut Mixture gradation, designated as NRM,
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268 Road Materials and Pavement Design. Volume 12 – No. 2/2011
– Caltrans gradation used for intersections, designated as CT,
– NDOT Type 2C gradation, designated as T2C,
– NDOT Type 2 gradation, designated as T2,
– Rut Mixture gradation, designated as RM.
The RM and the NRM gradations belong to the rut mixtures and no rut mixtures
zones, respectively, as identified in Figure 1. The NDOT Type 2C gradation is used
by NDOT very successfully to resist rutting under highway traffic load throughout
the entire state of Nevada but its performance has not been as good at intersections
in the southern part of the state. The T2C gradation belongs to the no rut mixtures
zone for sieve sizes larger than 4.75 mm and for the rut mixtures zone for sieve sizes
smaller than 4.75 mm. The NDOT Type 2 gradation is a finer gradation than the
NDOT Type 2C gradation and belongs to the rut mixtures zone. On the other hand,
the CT gradation belongs to the rut mixtures zone for sieve sizes larger than 9.5 mm
and for the no rut mixtures zone for sieve sizes smaller than 9.5 mm. It should be
noted that both NDOT gradations meet the Superpave specification for a nominal
maximum aggregate size of 19 mm. Figure 2 shows all five aggregate gradations
evaluated in the laboratory.
Figure 2. Laboratory produced aggregate gradations – phase I
The laboratory evaluation assessed the resistance of the mixes to permanent
deformation using the triaxial compressive strength test, the Repeated Shear
Constant Height (RSCH) test, the repeated Load Triaxial Test (RLT), and the
Asphalt Pavement Analyzer (APA) test. All laboratory performance test results
yielded a ranking of mixtures from best to worst rutting resistance as follows: NRM,
CT, T2C, T2, and RM.
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Evaluation of Rut Resistant Asphalt Mixtures for Intersection 269
The mixes with the aggregate gradation identified from the intersections that
experienced no rutting (NRM) showed the best performance in all the permanent
deformation tests conducted in this phase of the study. However, this gradation was
the coarsest one among all the evaluated five gradations. Therefore, it was
recommended that fatigue resistance of this mix should be evaluated prior to its
implementation at intersections in southern Nevada. On the other hand, the NDOT
Type 2C gradation showed, in the laboratory, a significant improvement in rutting
resistance when compared to the mixes that experienced rutting at intersections in
southern Nevada. However, NDOT started recently specifying the PG76-22 binder
for the southern part of the state after using the AC-30 asphalt binder for the past 15
years. Therefore, it was also recommended to continue monitoring the performance
of the Type 2C mixes with the PG76-22 binder at intersections in southern Nevada.
In summary, phase I of the study led to the conclusion that permanent
deformation at intersections in southern Nevada may be resisted by certain
aggregate gradations and mixtures that meet specific permanent deformation testing
requirements. However, the fatigue characteristics of the identified rut resistant
mixtures, i.e., T2C, CT, and NRM, were unknown which led to phase II of the
research.
4. Materials and mixtures characteristics
In phase II of the research study, an experimental program was carried out to
evaluate the rutting and fatigue behaviors of the mixes with the NRM, CT, and
NDOT type 2C gradations (Figure 2). All three mixes were designed with a
polymer-modified PG76-22 asphalt binder and limestone aggregates sampled from
atypical quarry located south of Las Vegas, Nevada.
All mixes were designed using the Hveem Mix Design Method as specified by
NDOT. Additionally, all mixes were treated with 1.5% hydrated lime by dry weight
of aggregate following NDOT’s specifications. NDOT mandates the use of lime in
all mixes to improve the mixtures’ resistance to moisture damage. The mixes were
designed for heavy traffic which corresponds to a minimum Hveem stability of 37.
5. Laboratory evaluation
The laboratory-produced mixes were evaluated in terms of the following
properties: stiffness, resistance to rutting, and resistance to fatigue cracking. The
laboratory evaluation will provide mixtures properties that are used in the following
two analyses: a) comparison of the relative performance of the various mixes, and b)
mechanistic analysis of HMA pavements under moving and braking heavy loaded
trucks.
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270 Road Materials and Pavement Design. Volume 12 – No. 2/2011
5.1. Stiffness of the mixtures
The Dynamic Modulus (|E*|) is the primary material property of HMA mixes
that is used in structural pavement design. Due to the viscoelastic behavior of the
HMA pavement, this property varies with temperature and time of loading. The
dynamic modulus test (AASHTO TP62-07, 2008) was used to develop the dynamic
modulus master curve of the three HMA mixes. For linear viscoelastic materials
such as HMA mixes, the stress-strain relationship under a continuous sinusoidal
loading is defined by its complex dynamic modulus (|E*|). Mathematically, the
“dynamic modulus” is defined as the absolute value of the complex modulus, i.e.,
|E*| = 10/00, where 10 and 00are peak (amplitude) stress and strain, respectively.
The dynamic modulus master curve is represented by the sigmoidal function
described by Equation [1a]. The general form of the shift factors is provided in
Equation [1b].
�[1a]
[1b]
where, tr is the time of loading at the reference temperature, D andGare fitting
parameters; for a given set of data, G represents the minimum value of log(|E*|), D+
G represents the maximum value of log(|E*|), E + J = parameters describing the
shape of the sigmoidal function, a(T)is the shift factor as a function of temperature,
T is the temperature of interest and tis the time of loading at a given temperature of
interest.
According to the new AASHTO MEPDG (NCHRP, 2004), a(T) can be
expressed in terms of asphalt binder viscosity and time of loading at a given
temperature of interest as shown in Equation [2]. The parameter c is one of the
values returned by the numerical optimization. The optimization was performed
using the “Solver” function in Microsoft Excel®. This calculation is performed by a
spreadsheet to compute the sum of the squared errors between the logarithm of the
average measured dynamic moduli at each temperature/frequency combination and
the values predicted by Equation [1a] (AASHTO PP62-09, 2010). The shift factor
depends only on the binder viscosity for the age and temperature of interest (K), and
the Rolling Thin Film Oven (RTFO) aged viscosity at the reference temperature
(KTR)
� [2]
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Evaluation of Rut Resistant Asphalt Mixtures for Intersection 271
For the RTFO-agedPG76-22 asphalt binder, the viscosity was measured at
multiple temperatures and the viscosity-temperature (in Rankine) relationship was
developed:
loglog(K) = 4.704 – 2.481 x log( TR ) [3]
Figure 3 shows the dynamic modulus master curves |E*| for all the three
evaluated mixes at the reference temperature of 21ºC. Figure 3 shows that the |E*| of
the NRM mix is higher than the CT and the T2C mixes for a reduced frequency
above 0.0004 Hz. However, the dynamic modulus property of the CT mix is higher
than the T2C mix only at a reduced frequency between 0.1 and 3500 Hz. At a
reduced frequency below 0.0003 Hz the dynamic modulus of the T2C exceeded the
ones of the CT and NRM mixes.
Figure 3. Dynamic modulus master curves at 21°C
Additionally, the storage (E’) and loss (E”) moduli master curves of the various
mixes at 21°C are shown in Figure 4. The data show that E’ of the NRM mix is
higher than the CT and T2C mixes at all frequency above 0.0001 Hz. However, the
E’ property of the CT mix is higher than the T2C mix only at a frequency of 0.1 to
4000 Hz. At a frequency below 0.0001 Hz the E’ of the T2C exceeded the ones of
the CT and NRM mixes. On the other hand, the E” of the NRM mix is higher than
the CT and T2C mixes at a frequency above 0.001 Hz. However, the E” property of
the CT mix is higher than the T2C mix only at a frequency of 0.1 to 450 Hz.
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272 Road Materials and Pavement Design. Volume 12 – No. 2/2011
Figure 4. Storage and loss modulus master curves at 21°C
5.2. Resistance of the mixtures to rutting
The resistance of the HMA mixes to rutting can be evaluated under two types of
testing: empirical and fundamental. In the category of the empirical tests, this study
used the Asphalt Pavement Analyzer (APA) to evaluate the relative performance of
the various mixtures. However, in the category of fundamental tests, this study used
the repeated load triaxial test (RLT) to evaluate the fundamental behavior of the
various mixtures.
5.2.1. Rutting behavior in the asphalt pavement analyzer test
The APA test is standardized under AASHTO TP63-03 (2008), where a loaded
concave steel wheel travels along a pressurized rubber hose that rests upon the HMA
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Evaluation of Rut Resistant Asphalt Mixtures for Intersection 273
sample. Four 152-mm diameter cylindrical samples were compacted from each mix
using the Superpave Gyratory Compactor (SGC) to a height of 76 mm and air voids
of 7±0.5%. Samples are secured within form-fitting acrylic blocks during testing.
The APA wheel load is 445-N and the hose pressure is 689kPa. A data acquisition
program records rut depths during testing at 2 points within each sample and their
average is reported.
Figure 5 summarizes the rut depth data from the APA test at 60°C. The data
indicate that all mixes meet and are far below the NDOT APA criterion of 8mm rut
depth after 8,000 cycles at 60°C for highway speed. No significant difference was
observed between the various mixes at 60°Cthus indicating similar resistance to
rutting. These results could be an indication that the APA test is not sensitive
enough to test for any significant difference in the rutting resistance of the mixtures
when tested at a temperature lower than the high performance temperature of the
binder (i.e. PG76-22).
Following the above observation, the various mixes were tested under the APA
at 76°C. Figure 5 shows that all three mixtures exhibited a rut depth at 76°C that is
less than 8mm with the NRM having the lowest (2.0 mm) followed by the CT mix
(2.8 mm) and the NDOT T2C mix (3.6 mm). The various APA rut depths after 8000
cycles were compared using the least square mean (LS mean) statistical technique.
The LS mean results show that the three mixes were significantly different at
76°C,with the NRM having the best rutting resistance followed by the CT and the
NDOT T2C.
Figure 5. APA rut depths at 60 and 76°C (numbers above bars represent mean
values for 4 replicates and whiskers represent mean +/- one standard deviation)
5.2.2. Rutting behaviour in the repeated load triaxial test
HMA samples of 100 mm diameter by 152 mm height specimens were
compacted in the SGC to 7r0.5%air voids. All mixes were evaluated at 30, 50 and
70ºC. Compressed air was used to apply a constant confining pressure of 207kPa.
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274 Road Materials and Pavement Design. Volume 12 – No. 2/2011
Adeviator vertical stress of 307kPa was cycled by applying a haversine load pulse of
0.1 second duration followed by a 0.6 second rest period (i.e., unload). The 0.1
second load duration was selected in order to simulate the loading of a truck moving
at highway speed. This complete cycle was repeated 12,000 times. Axial
deformations were continuously measured over the middle 100mm of the sample.
The RLT test results were used to develop the rutting performance models for
the three evaluated mixes. The performance model suggested in the MEPDG
(Equation [4]) to assess rutting in the HMA layer relates the ratio of axial permanent
strain (0p)over the resilient axial strain (0r), to the number of loading cycles (N) and
temperature (T). The a, b, and c in Equation [4] are experimentally determined
regression coefficients. It is clearly shown from the generalized rutting model that
the lower the 0p/0r the higher the rutting resistance of the mix.
[4]
The data from the RLT test were plotted in the form of the ratio of permanent
strain over the resilient strain (0p/0r) versus loading cycles (N) as shown in Figure 6.
Each curve represents the average response of three replicate samples tested at each
of the specified temperatures (i.e. 30, 50 and 70ºC). In general, the lower the RLT
curve (i.e. lower intercept and slope of the RLT curve) the higher the resistance of
the mixture to permanent deformation. The data in Figure 6 show that the resistance
of the mixtures to permanent deformation increase as the temperature of the test
decreases. Additionally, the data show that 0p/0r of the T2C mix increased at higher
rate than the 0p/0r of the NRM and CT mixes at all three temperatures. Consequently,
the T2C mix will exhibit a faster build-up of the permanent strain under multiple
loading indicating a lower resistance to rutting than the NRM and CT mixes.
The RLT data at the three testing temperatures were used to develop the
generalized rutting model for each mixture as presented in Equation [4]. Table 1
summarizes the regression coefficients for the generalized rutting models of each
mix.
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Evaluation of Rut Resistant Asphalt Mixtures for Intersection 275
Figure 6. RLT test results at 30, 50, and 70°C
Table 1. Rutting regression parameters of the various mixtures
Mix a* b* c* R2
NRM 3.0047×10-4 0.35443 1.9155 0.986
CT 3.9653×10-5 0.34572 2.5212 0.992
T2C 7.1050×10-6 0.41377 2.7634 0.999
* , T in qC
The ratio of the permanent axial strain over the resilient axial strain (0p/0r) after
12,000 loading cycles were compared for any statistically significant differences
using the LS mean technique. Figure 7 summarizes the 0p/0r values along with the
significance difference after 12,000 loading cycles. The statistical analysis shows
that, at the 30°C, the NRM mix exhibits the highest 0p/0r, followed by the NDOT
T2C mix, and the CT mix. At 50°C, the NDOT T2C mix exhibits the highest 0p/0r,
followed by the NRM mix and the CT mix. Consequently the CT mix will have a
better resistance to rutting than the other two mixes at 30°C and 50°C. On the other
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276 Road Materials and Pavement Design. Volume 12 – No. 2/2011
hand, at 70qC the NRM mix exhibited the lowest 0p/0r, followed by the CT mix, and
the NDOT T2C mix. Therefore, the NRM mix will have a better rutting resistance
with the NDOT T2C mix having the least resistance to rutting.
Figure 7. Statistical comparison of Hp/Hr from RLT test results after 12,000
cycles(SH and SL denotes, respectively, “significantly higher” and “significantly
lower” 0p/0r of the NRM or CT mix than the 0p/0r of the NDOT T2C mix)
5.3. Resistance of the mixtures to fatigue cracking
The resistance of the three HMA mixes to fatigue cracking was evaluated at
4.4°C, 21°C and 43°C using the flexural beam fatigue test (AASHTO T321-07, 2008)
under the strain controlled mode of testing. Fatigue life (Nf) or failure was defined as
the number of cycles corresponding to a 50% reduction in the initial stiffness. The
initial flexural stiffness of the mix was measured at the 50th load cycle. The model
shown in Equation [5] was used to characterize the fatigue behavior of the HMA
mixes at each of the tested temperatures:
[5]
Where 0t is the applied tensile strain, and k1 and k2 are experimentally determined
coefficients. The beam fatigue samples were compacted using the kneading
compactor to 7±0.5 percent air voids. It is clearly shown from the beam fatigue
relationship that the higher the k1 and k2 values, the more fatigue resistant the mix is.
Figure 8 shows the fatigue relationships of the three mixes at each of the testing
temperatures. The data show a better fatigue resistance for the CT and NDOT T2C
mixes at 4.4°C when compared to the NRM mix. On the other hand, a better fatigue
resistance for the CT mix at 21°C was observed when compared to the other two
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Evaluation of Rut Resistant Asphalt Mixtures for Intersection 277
mixes which exhibited similar fatigue characteristics. Additionally, a better fatigue
resistance was observed for the CT mix at 43°C when compared to the other two
mixes with a slightly better resistance for the NDOT T2C mix over the NRM mix.
Figure 9 summarizes the fatigue data of the various mixes in terms of the number
of cycles to failure and ratios under tensile strains of 500 microns at a temperature of
4.4°C, and 800 microns at a temperature of 21°C, representing medium and high
levels of tensile strains at the bottom of the HMA layer of a flexible pavement. The
selection of the strain levels was based on the typical stains encountered in
pavements and the availability of data for the statistical comparison of the Nf values
of the various mixes. No statistical analyses were conducted at 43°C because two
out of the three mixes were not actually tested at 800 microns. The statistical
analyses show that at 4.4°C, the CT mix has significantly higher number of cycles to
failure than the NRM and NDOT T2C mixes. Additionally the NDOT T2C mix has
significantly higher fatigue life than the NRM mix. At 21°C, the CT mix has
significantly higher number of cycles to failure than the NRM and the NDOT T2C
mixes.
The recommended MEPDG generalized model that correlates the number of
cycles to failure (Nf) to the tensile strain (0t) and mixture’s stiffness (E) was
developed for each of the mixes evaluated in this study (Equation [6]) by fitting a
multiple linear regression for the test data at the various temperatures. The k1, k2 and
k3 are experimentally determined coefficients (Table 2). The short-term aged
dynamic moduli of the various mixes at 10 Hz and at the various temperatures
(4.4°C, 21°C, and 43qC) were determined using the dynamic modulus master curves
and their corresponding shift factors at the specified temperature. The developed
mix specific generalized models will be used in the mechanistic analysis described
later to evaluate the impact of mixture type on the fatigue performance of an HMA
pavement.
[6]
Table 2. Fatigue generalized models of the various HMA mixes
Mix K1 K2 K3 R2
NRM 0.62908 4.2395 2.1470 0.916
CT 0.26784 4.3172 2.0598 0.860
T2C 0.03493 4.4143 2.0374 0.926
* , Ht in mm/mm and E in MPa
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Figure 8. Fatigue characteristics of the various mixes
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Figure 9. Laboratory measured fatigue life of the various mixes and ratio of fatigue
life with respect to T2C mix
6. Mechanistic analysis
A better laboratory performance of an HMA mix in rutting or fatigue may not
necessarily translate into a better performance in the field as the performance life of
an asphalt pavement is highly dependent on both the stiffness and the characteristics
of the HMA mix (e.g. rutting and fatigue resistance) and their interactions. For
example, in a mechanistic pavement analysis, an HMA layer with a higher stiffness
will produce under field loading a lower tensile strain at the bottom of the HMA
layer. But on the other hand, the same mix will show a lower laboratory fatigue life
(lower resistance to fatigue cracking) under strain controlled mode of testing when
compared to mixes with lower stiffness. Therefore, depending on the magnitude of
the reduction in the calculated strain at the bottom of the HMA layer, the HMA layer
with the higher stiffness may result in a longer fatigue life in the field even though it
exhibited a lower laboratory fatigue life. Therefore, a full mechanistic analysis needs
to be conducted to effectively evaluate the performance of an HMA pavement.
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A mechanistic-empirical design method represents the most advanced method
for designing HMA pavements. The mechanistic portion is based on the mechanics
of materials that relates an input, such as a wheel load, to an output or pavement
response, such as stress or strain. The empirical portion is when the response values
are used to predict distresses based on laboratory relationships calibrated with field
performance data. Consequently, predicting the rutting and fatigue life of HMA
pavements necessitates the development of permanent deformation and fatigue
models in the laboratory followed by a mechanistic analysis to determine the
pavement responses in the HMA layer, which in turn are used as input to the
permanent deformation and fatigue models.
The permanent deformation and fatigue models for the three mixes (i.e. NRM,
CT, and T2C) developed in this study are used in the mechanistic analysis. It should
be mentioned that the developed performance models are statistical relationships
based on the laboratory analysis of the asphalt mixes and therefore field
shift/adjustment factors are required to provide reasonable estimates of the actual
performance in the field. The field shift factors are outside the scope of this research
and the laboratory-based performance models were only used for a relative
comparison.
Pavement responses were determined under the loading of an 18-wheel truck at
normal highway speed (without braking) and at intersection (with braking). In this
study the computer code 3D-Moving Load Analysis (3D-MOVE) developed by
Siddharthan et al. (1998) was used to estimate the pavement dynamic responses.
6.1. Description of the computer code 3D-MOVE load analysis
The computer code 3D-MOVE incorporates the approach of the formulation of a
continuum-based “finite-layer” model to evaluate the response of a layered medium
subjected to a moving surface load (Siddharthan et al., 1998). The pavement system
is characterized through a combination of viscoelastic and elastic horizontal layers
with each layer characterized using a set of uniform properties that rest on a rigid
impermeable layer. The 3D-MOVE model can handle multiple moving loads, non-
uniform tire-pavement normal contact stress distribution, and non-uniform interface
shear stresses caused by braking and turning forces.
Since the 3D-MOVE program can only simulate moving loads at a constant
speed, the response of the asphalt pavement to the decelerated truck during the
braking period was estimated at two different speeds: 64 and 3.2 km per hour, before
it starts braking and as it approaches the intersection, respectively. The braking
forces as a result of deceleration were incorporated in the analysis to simulate the
braking effect.
The mechanistic-empirical analysis is used in conjunction with the dynamic
modulus, fatigue characteristics data, and rutting characteristic data that were
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measured in the laboratory on all three mixes to assess the fatigue and rutting
performance of HMA pavements. The analysis considered a three layers pavement
consisting of an HMA layer on top of a crushed aggregate base on top of the
subgrade. A total of six pavement structures were analyzed in this study (Table 3).
Table 3. Analyzed pavement structures
Thickness [mm]
Structure No.Pavement layers
1 2 3 4 5 6
NRM 100 200 -- -- -- --
CT -- -- 100 200 -- --
T2C -- -- -- -- 100 200
Crushed aggregate base
(CAB)200 200 200 200 200 200
Subgrade Infinite
The first step of the above mechanistic analysis is to estimate the load
distributions on various tires of the 18-wheel tractor-semitrailer during normal
highway traffic and at intersections. Braking at intersections causes the vehicle to
decelerate and the loads to transfer to the front of the vehicle. The resulting axle load
can be higher or lower than the initial static load, depending on the axle location.
Figure 10 shows the major forces acting on an 18-wheel tractor-semitrailer during
braking on a downward sloping pavement. The axles include: the tractor steering
axle, the tractor tandem axle (i.e., driving axle), and the semitrailer tandem axle (i.e.,
trailer axle). Since an intersection located on a downward sloped pavement
represents the worst case scenario, the tire loads distributions were determined for
an 18-wheel truck braking on a 6% downward sloping pavement (Hajj, 2005; Hajj et
al., 2006).
In order to calculate the normal load on each axle, the tractor and the semitrailer
are considered as free bodies separately and combined. The vertical, horizontal, and
moment equilibrium equations for the tractor, semitrailer unit, and tractor-
semitrailer combination were derived as a function of truck loads and geometry. By
solving the system of equilibrium equations, the normal loads on the various axles
during braking on a downward slope can be expressed as a function of the linear
deceleration of the truck along the longitudinal axis, the angle of the slope with the
horizontal, the tractor and semitrailer total weights and the truck geometry. The full
formulation and solutions are presented by Hajj (2005). Table 4 summarizes the load
distributions on the various axles of the 18-wheel tractor-trailer combination under
the normal highway traffic (without braking) and at intersections (with braking).
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282 Road Materials and Pavement Design. Volume 12 – No. 2/2011
Figure 10. Forces acting on a tractor-semitrailer during braking on a downward
slope
Table 4. Axle load distributions of a fully loaded 18-wheel tractor-trailer
Speed – Braking
Action AxleVertical load per tire
[kN]
Horizontal load per tire
[kN]
Steering 26.7 0
Front driving
Rear driving
18.9
18.9
0
064km/h –
no braking
Front trailer
Rear trailer
18.9
18.9
0
0
Steering 37.7 9.6
Front driving
Rear driving
22.8
14.9
13.2
13.23.2km/h –
braking
Front trailer
Rear trailer
19.5
12.7
11.4
11.4
The stress distribution at the tire-pavement interface is significantly affected by
tire type, inflation pressure, and load. Previous studies showed that the stress
distribution at the tire-pavement interface is not uniform, and influences the HMA
pavement resistance to rutting and fatigue failures (Sebaaly, 1992; De Beer and
Fisher, 1997; Myers et al., 1999; Weissman, 1999). This study used the non-uniform
stress distributions under the Goodyear G159A 295/75R22.5 tire measured by the
Kistler device, for an inflation pressure of 827kPa. The Kistler MODULAS Quartz
Sensor Array device measures the vertical stress as the tire moves over a measuring
pad. The loading of the MODULAS sensors was accomplished by driving a truck
with a single trailer at a preset speed. Vertical stress distributions are available for a
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wide range of tire loads and vehicle speeds. Braking forces at each tire were
included as interface shear stresses with their distribution estimated by multiplying
the vertical stress distribution by the calculated coefficient of friction between the
tire and the pavement surface. The coefficient of friction at each tire was determined
by dividing the longitudinal load at the tire by the associated vertical load.
Two vehicle speeds were considered: 64 km per hour (away from intersection)
and 3.2 km per hour (at intersection). Rutting and fatigue analyses were conducted
at two different pavement temperatures of 64°C and 21°C, respectively. The
laboratory developed dynamic modulus master curves of the three mixes for the
analyses temperatures (i.e. 64°C and 21°C) are used to characterize the HMA mixes.
The internal damping for the HMA layer is estimated as a function of the loading
frequency and is included in the analysis by writing the dynamic modulus (|E*|) in
its complex form as follows (Rosset, 1980):
[7]
In which ]AC is the internal damping of the HMA, and E’ and E” are the real and
imaginary modulus components, respectively. The poisson’s ratio (X) for the HMA
layer is assumed to be constant of value 0.4 for the temperature range used in this
analysis.
The base course and subgrade layers are treated in this study as linear elastic
materials with anelastic modulus of 240MPa and 69MPa, respectively. The internal
damping of the unbound layers was assumed to be 5%. The poisson’s ratio was
assumed to be 0.4 for both layers.
Pavement responses such as stresses, strains, and displacements were computed
as a function of time using the 3D-MOVE computer code. Responses at the middle
of the HMA layer were considered for rutting analysis; whereas the responses at the
bottom of HMA layer were considered for fatigue analysis.
6.2. Rutting analysis
The latest development in predicting rutting within the HMA layer calls for the
determination of plastic vertical compressive strain within the HMA layer. The total
rutting within the HMA layer is then calculated by multiplying the permanent strain
times the thickness of the HMA layer.
[8]
Where, RDHMA is the rutting generated in the HMA layer,Hp is the permanent
strain within the HMA layer, and hAC is the thickness of the HMA layer.
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284 Road Materials and Pavement Design. Volume 12 – No. 2/2011
The developed laboratory rutting models for the three mixtures (Table 1) along
with the calculated dynamic resilient axial strain from the mechanistic analysis were
used to predict the permanent strain (Hp) within the HMA layer of the various
pavement structures. It should be noted that the predicted permanent strains were
multiplied by the depth correction function (k1) recommended by the new AASHTO
MEPDG. The depth correction function (k1) is an empirical attempt based on
engineering judgment and very limited field data to adjust the computed plastic
strains for the influence of lateral confining pressure at different depths. Equation
[9] shows k1 as a function of hAC (mm) and the depth (depth, mm) to the
computational point. A k1 value of 3.49 and 0.633 was computed at the mid depths
of the 100 and 200 mm HMA layers, respectively.
[9a]
[9b]
[9c]
The rutting resistance of the various mixes was evaluated with the calculated
permanent axial strain (Hp) in the HMA layer for a fixed number of load repetitions.
Table 5 summarizes the maximum permanent strains and rut depths within the 100-
mm and 200-mm HMA layers under 12,000 loading cycles at normal highway speed
and at intersection. The highest permanent strain and rut depth were found to be
under the steering axle which makes it the most damaging axle in the 18-wheel truck
to the pavement at normal highway speed and at intersection.
The data in Table 5 show that the permanent strains at intersection for 12,000
loading cycles are higher than the one at normal highway speed by a ratio of about
2.0 for both the NDOT T2C and CT mixes and a ratio of 2.5 for the NRM mix.
Additionally, the NRM mix exhibited significantly lower rut depth at normal
highway speed when compared to the NDOT T2C and CT mixes. However, at
intersection all three mixes exhibited similar rut depths after 12,000 loading cycles
with a slightly lower rut depth for the NRM mix. Therefore, it can be concluded that
all mixes exhibited similar rutting resistance under a braking 18-wheel truck with a
slight better resistance for the NRM mix.
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Table 5. Maximum permanent strains and rut depths under 18-wheel truck at 64qCand after 12,000 loading repetitions
Maximum permanent axial strains and rut depths under 12,000 loading repetitions
100-mm HMA layer 200-mm HMA layer
MixesNormal
highway
speed
(64km/h,
no braking)
Intersect-
ion
(3.2km/h,
braking)
Ratio of
Hp-max at
intersection
over Hp-max at
normal
highway
speed
Normal
highway
speed
(64km/h,
no
braking)
Intersect-
ion
(3.2km/h,
braking)
Ratio of
Hp-max at
intersection
over Hp-max at
normal
highway
speed
NRM9.3%
(9.4mm)
22.8%
(23.1mm)2.4
1.6%
(3.3mm)
4.0%
(8.1mm)2.5
CT13.0%
(13.2mm)
25.3%
(25.4mm)1.9
2.1%
(4.3mm)
4.3%
(8.6mm)2.0
NDOT
T2C
14.4%*
(14.7mm)
25.7%
(25.4mm)1.8
2.3%
(4.6mm)
4.4%
(8.9mm)1.9
Ratio of
NRM
over
NDOT
T2C
0.65 0.89
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0.70 0.91
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Ratio of
CT over
NDOT
T2C
0.90 0.98
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0.91 0.98
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Ratio of
CT over
NRM1.40 1.11
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1.31 1.08
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* Rut depth in “mm” is shown in parenthesis.
6.3. Fatigue cracking analysis
The bottom-up fatigue cracking of pavements initiates from the bottom of the
HMA layer and propagates to the pavement surface. The number of load repetitions
is related to the tensile strain at the bottom of the HMA layer and the modulus of the
HMA mix.
The number of load repetitions to fatigue failure of each pavement structure is
estimated using the generalized fatigue model of each mix (Table 2) by applying the
calculated maximum tensile strain at the bottom of the HMA layer (i.e. 3D-MOVE)
and the corresponding stiffness of the mix at 21qC. In order to determine the
mixtures’ stiffness to be used in the fatigue model (Equation [6]), the rate of loading
under normal highway speed and at intersection for each pavement structure is
determined using Barksdale chart (1997). Following Barksdale chart, the loading
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time for both, 100 mm and 200 mm HMA layer, at an operating speed of 3.2km/h
was considered to be 1Hz. At an operating speed of 64km/h the loading time for
both 100 and 200 mm HMA layer was considered to be 10Hz. Following these
steps, the mixtures’ stiffness for the fatigue models were selected from the dynamic
modulus at a loading frequency of 10Hz and 1Hz for the normal highway speed and
intersection, respectively.
The maximum tensile strains at the bottom of the HMA layers were relatively
low and varied between 79 and 238 PH�in the 100-mm HMA layer and between 51
and 127 PH�in the 200-mm HMA layer. The lowest number of cycles to fatigue
failure was under the steering axle which makes it the most damaging axle in the 18-
wheel truck to the pavement at normal highway speed and at intersection.
Table 6. Fatigue lives ratios
100 mm HMA layer 200 mm HMA layer
Fatigue lives ratio Intersection
(3.2km/h,
braking)
Normal
highway speed
(64km/h, no
braking)
Intersection
(3.2km/h,
braking)
Normal highway
speed (64km/h,
no braking)
Nf-NRM/ Nf-NDOT-T2C 1.7 1.4 1.4 1.1
Nf-CT/ Nf-NDOT-T2C 3.2 1.8 3.0 1.4
The critical numbers of load repetitions to fatigue failure in the 100-mm and
200-mm HMA layers under normal highway speed (i.e. 64 km/h no braking) and at
intersection (i.e. 3.2 km/h with braking) were calculated using the appropriate
fatigue model for each of the evaluated mixtures. Since the fatigue models have not
been calibrated against actual field performance data, the ratios of the fatigue lives
were used to evaluate the relative performance of the evaluated mixtures. Table 6
summarizes the ratios of the fatigue lives defined as the ratio of the fatigue life of a
given mix over the fatigue life of the Nevada T2C mix.
Under normal highway speed and in the 100-mm HMA layer, the numbers of
load repetitions to fatigue failure of the CT and NRM mixes were 1.8 and 1.4 times
the number of load repetitions to fatigue failure of the NDOT T2C mix, respectively.
On the other hand, in the 200-mm HMA layer, the numbers of load repetitions to
fatigue failure of the CT and NRM mixes were 1.4 and 1.1 times the number of load
repetitions to fatigue failure of the NDOT T2C mix, respectively.
At intersection and in the 100-mm HMA layer, the numbers of load repetitions to
fatigue failure of the CT and NRM mixes were 3.2 and 1.7 times the number of load
repetitions to fatigue failure of the NDOT T2C mix, respectively. On the other hand,
in the 200-mm HMA layer, the numbers of load repetitions to fatigue failure of the
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CT and NRM mixes were 3.0 and 1.4 times higher than the number of load
repetitions to fatigue failure of the NDOT T2C mix, respectively.
7. Overall summary of findings
The Nevada Department of Transportation (NDOT) is currently specifying the
same type of gradation (i.e. Type 2C) for most of its HMA mixes regardless whether
the mix will be placed on highway or intersection. Although, the NDOT Type 2C
gradation showed excellent rutting resistance under normal highway traffic loading,
its resistance to rutting and shoving at intersections in the hot environment of
southern Nevada was not promising.
The rutting and fatigue resistance of the NRM, CT, and NDOT T2C mixes were
relatively compared and ranked based on the laboratory evaluations and the
mechanistic-empirical analysis. The mix that ranked first was given a score of 1
while the mix that ranked last was given a score of 3. Then, the sums of all scores
were then calculated for each mix and are summarized in Table 7. The mix with the
lowest sum of scores is ranked first overall while the mix with the highest sum of
scores is ranked last.
Based on the data generated from the laboratory experiment and the mechanistic
analyses, the following conclusion can be made.
– When the laboratory rutting resistances of the mixes were compared, the NRM
mix showed higher rutting resistance than the CT mix and the NDOT T2C mix in
the RLT test at 70qC and in the APA test at 76qC. Additionally, the CT mix showed
higher rutting resistance than the NDOT T2C mix in the RLT and in the APA tests.
– When the laboratory fatigue resistances of the mixes were compared, the CT
mix showed higher fatigue resistance than the NRM mix and the NDOT T2C mix.
Also, the NDOT T2C mix showed higher fatigue resistance than the NRM mix.
– The dynamic modulus of the NRM mix is higher than the dynamic modulus of
the CT mix and the NDOT T2C mix at 21°C. The dynamic modulus of the CT mix
was higher than the dynamic modulus of the NDOT T2C mix only at a frequency
higher than 0.1 Hz.
– When combining the laboratory fatigue and rutting characteristics of the mixes
with their mechanical properties (|E*|) into the mechanistic-empirical analysis, the
following observations were obtained:
- Rutting analysis: Under normal highway speed and at intersection, the NRM
mix exhibited a rut depth slightly lower than the CT and the NDOT T2C mixes
which showed similar rut depths regardless of the HMA layer thickness.
- Fatigue analysis: The fatigue life of the CT mix is better than the fatigue life
of the NDOT T2C mix and the NRM mix under both normal highway speed and at
intersection. Additionally, the fatigue life of the NRM mix is better than the fatigue
life of the NDOT T2C mix. However, the polymer-modified PG76-22 mix has
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288 Road Materials and Pavement Design. Volume 12 – No. 2/2011
shown excellent fatigue performance under Nevada’s conditions, and therefore, the
relatively lower fatigue resistance of the T2C mix should not be of a great concern.
Table 7. Relative ranking of the various mixes in terms of rutting and fatigue
resistance
Individual scoresType of
EvaluationProperty NDOT
T2CCT NRM
At 30°C 1 1 1
At 50°C 2 1 1
Rutting resistance in the
Repeated Load Triaxial
(RLT) testAt 70°C 3 2 1
At 60°C 1 1 1Rutting resistance in the
Asphalt Pavement
Analyzer (APA) test At 76°C 3 2 1
At 4.4°C 2 1 3
At 21°C 2 1 2
Laboratory
evaluation
Fatigue cracking
resistance
At 43°C 2 1 3
Normal
highway speed2 2 1Rutting resistance for
12,000 loading
repetitions Intersection 2 2 1
Normal
highway speed3 1 2
Mechanistic
- empirical
analysis
Fatigue resistance
Intersection 3 1 2
Total sum of scores 26 16 19
Overall ranking 3 1 2
In summary, it can be concluded that the CT mix offers advantages in the fatigue
resistance when compared to the other mixes, whereas the NRM mix offers
advantages in rutting resistance when compared to the other mixes. Based on the
overall ranking of the various mixtures, the CT mix ranked the first followed closely
by the NRM mix. The NDOT T2C was ranked last with a significantly higher
overall sum of scores. However, it should be noted that the mechanistic-empirical
analysis showed in general the resistance to rutting of the NDOT T2C mix to be
similar to that of the CT mix, differing from the laboratory evaluation test results.
This is due to the interaction between the rutting characteristics of the mixes with
their stiffness properties (|E*|) in the mechanistic-empirical analysis. On the other
hand, the NDOT T2C mix showed an acceptable resistance to fatigue cracking.
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Evaluation of Rut Resistant Asphalt Mixtures for Intersection 289
8. Recommendations
Based on the data generated in this study, the NDOT T2C gradation with the
PG76-22 binder is expected to provide acceptable resistance to rutting with a
marginal fatigue cracking resistance. On the other hand, a significant improvement
in mixtures’ resistance to rutting and fatigue cracking is expected with the CT and
NRM gradations.
a)
b)
Figure 11. (a) Comparison of the NRM and NDOT T2C gradations; (b) Proposed
specification limits for intersection mixes
Consequently, NDOT should consider modifying the NDOT T2C gradation to
closely resemble to the NRM gradation. The NRM gradation was recommended
instead of the CT gradation since it involves fewer modifications to the currently
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290 Road Materials and Pavement Design. Volume 12 – No. 2/2011
used NDOT T2C gradation. Figure 11a compares the NDOT T2C and NRM
gradations along with the upper and lower limits specifications of the NDOT T2C
gradation. The data in Figure 11a show that the NRM gradation violates the NDOT
T2C limits only on the 2-mm sieve. Therefore, it is recommended that, for use on
high traffic intersections, NDOT lowers the limit on the percent passing of the T2C
gradation on the 4.75-mm sieve by 3-5 percentage points which will make the T2C
closer to the NRM gradation. This requires lowering the T2C specification limits
between 4.75-mm and 0.425-mm as shown in Figure 11b to force the gradation to
cross the maximum density line. Based on the results of this study, moving the T2C
gradation closer to the NRM gradation (i.e. lowering its percent passing the 4.75-
mm sieve) should significantly improves its resistance to rutting and fatigue
cracking.
Acknowledgement
The authors gratefully acknowledge the support of the Nevada Department of
Transportation.
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Received: 7 July 2009
Accepted: 29 September 2010
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