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Finite Element Model for Axial Stiffness of Metal-Plate-Connected Tension Splice Wood Truss Joint
Jose M. Cabrero
Assistant Professor University of Navarra, Department of Structural Analysis and Design, School of Architecture
Navarra, Spain Kifle G. Gebremedhin
Professor Department of Biological and Environmental Engineering, Cornell University
Ithaca, NY, 14853, U.S.A.
Abstract
A finite element model that predicts stiffness for metal-plate-connected (MPC) tension splice joint of wood trusses is developed. The commercial software ABAQUS was used in developing the model. The model is two-dimensional, and the properties of the wood and metal plate are assumed to be linearly isotropic. Contacts between wood and teeth of the metal plate are modeled with finite sliding formulation. The contact elements model the slip behavior that occurs at the wood-tooth interface. The tangential contact properties are set to a specified coefficient of friction while the normal contact properties are set to a “hard” contact formulation, allowing for a possible separation of the nodes after contact is achieved. Contact elements represent the stiffness of the interface, and stiffness is lost once the contact elements are disengaged due to tooth withdrawal. Model predictions are validated against experimentally measured stiffness values obtained in the literature. The data covers two wood species and three levels of modulus of elasticity (MOE). The model predicts within 5 percent of the experimentally measured stiffness values.
1. Introduction
Conventional methods of design of metal-plate connected (MPC) wood truss joints assume that connections between the metal-plate connector and wood are either pinned or rigid. In reality, these joints exhibit a semi- rigid behavior, i.e., not purely pinned or rigid but somewhere in-between [1,2,3]. Therefore, the challenge is to determine the stiffness of these joints so that their semi rigidity could be accounted for in design of MPC wood trusses. Modeling the behaviour of the connector in the truss member is complicated by the composite nature of the metal and wood and the configuration of the system (a row of teeth embedded in wood and a gap existing between the wood elements). The metal plate connection is the lease understood in truss design.
The simplified approach of truss design is to assume truss joints to be pin connected, which means no moment is transferred between adjacent members. This assumption violates the continuity of chord members at the joints. To account for the indeterminacy of a truss when analyzed as pin-joined approximations, the Truss Plate Institute (TPI) has provided empirically-based Q-factors to modify the bending moment or the buckling length of truss members [4]. The Q-factors were developed based upon many years of experience of design and extensive simulated investigation of wood trusses of standard configurations using the Purdue Plane Structures Analyzer (PPSA) [5]. The PPSA is a matrix method of structural analysis that determines the axial forces and bending moments of truss-frame models. The
tabulated Q-factors provided by TPI do not cover all ranges and combinations of loading conditions, spans, and geometry. Therefore, theoretical models that provide realistic treatment of joints are needed so that forces and moments can be predicted with greater accuracy. Because of the wide application of MPC wood trusses in commercial, industrial, residential and agricultural buildings, even a reasonably small improvement in characterization of truss joints may result in significant cost savings.
The main focus of this research is to develop a finite element model for the wood-tooth interface of MPC tension-splice joint based on fundamental principles of contact mechanics that, apart from basic material properties, does not require empirical corrections. Linear elastic finite elements represent the metal plate, teeth, and wood; and contact elements are virtual (imaginary) spring elements that transfer compressive and frictional forces between the wood and the teeth of the metal plate as the joint is externally loaded. The commercial software package ABQUS is used to develop the contact elements. Modeling the interface using contact elements can have wide engineering applications such as in modeling the bondage between steel and concrete in reinforced concrete structures, the transfer of frictional forces between piles and soil in pile foundations, and modeling rotational stiffness of MPC wood joints.
1.1 Objectives
The specific objectives of this study were:
1. To develop a finite element model for the wood-tooth interface of metal-plate connected tension-splice joint of wood trusses using linear contact elements.
2. To predict the stiffness of a tension-splice joint.
3. To validate the predicted stiffness against measured values.
2. Literature Review
A thorough literature review of experimental and theoretical studies conducted on MPC wood-truss joints are reported in Amanuel et al. [1]. The reader is referred to that study for extensive literatura review.
3. Model Formulation
A bi-dimensional finite element (FE) model that predicts stiffness of MPC tension-splice joints is developed using the ABAQUS software.
3.1 Assumptions
1. Since the main deformation arises from the axial force in the x-direction, the deformation along the z-direction (perpendicular to the direction of the axial force) is assumed to be zero. Because of this assumption, the model is reduced to a plane strain model.
2. The behavior of the joint is governed by teeth-wood contacts and the resulting deformation of the teeth.
3. Tandi
4. BfoanR
5. Ethwex
3.2 B
Since botBecause x-directiocorresponcenterlinemotion.
3.3 L
Axial tenpressure.the load w
3.4 G
Wood lumPine. Theand werewere useactual ge
The stress disnd nonlinearistribution in
Both wood anor both matend Poisson’s
Riley and Geb
Even though his model be
wood is assumxperimentall
Boundary
th sides of thof symmetryon (directionnds to the cee. In the y-d
Load Appl
nsion force w In order to was applied
eometrica
mber speciee actual size e 76.2 mm byd in the expe
eometry of th
stribution in rity of the ben each row o
nd steel are merials. Moduls ratio is 0.3bremedhin [
wood is an oecause the jomed to be 0.ly by Riley a
Condition
he member ay, rollers aren of the axialenterline of tdirection, dis
lication
was applied aprovide unif50 mm awa
al Model
s used in thiof the lumb
y 102 mm inerimental stuhe metal plat
(
(b)
the connectiehavior of thof teeth is as
modeled as elus of elastic. These mate[6].
orthotropic moint is model4 and MOEand Gebrem
ns
are symmetre defined at tl load). The the plate. Alsplacement r
at the free enform load diay from the l
s study wereber was 38-mn size. Theseudy of Rileyte is shown i
(a)
b
ion is rather he wood-tootsumed to be
elastic matercity for steelerial propert
material, an ed as a planevalues used
medhin [6].
ical, only onthe bottom ometal plate ill displacemrestriction w
nd of the mestribution anast row of te
e 2 x 4 Sprucmm thick ande are the samy and Gebremin Figure 1.
complex beth interface.
e the same.
rials. Isotrop is assumed ies correspo
isotropic fore strain mod
d are the sam
ne side of theof the wood tis fixed alon
ments are restwas imposed
ember, and isnd avoid locaeeth.
ce-Pine-Fir ad 89-mm wid
me species, dmedhin [6].
ecause of pla In this stud
pic behavior to be 203,00nd to those r
rmulation is del. Poisson'
me values obt
e member is to allow mov
ng its left edgtricted alongto avoid rigi
s applied as aal stress con
and Southernde. Plates wimensions anA represent
ate geometrydy, force
is assumed 00 N/mm2 reported by
adequate for's ratio of tained
modeled. vement in thge, which the id-body
a uniform ncentration,
n Yellow were 20 gage
nd gage thatation of the
y
r
he
s, t
Figure 1
Some simbecause otoward thnominal computat
The hole good initestablishsurface.
3.5 EThe elemadapted fhas two dshape, it teeth due The meanelements(wood an
Figure 2.
1. (a and b) A[6
mplificationsof punched the end but arthickness oftional domai
in the woodtial contact bed by relocaThis is acco
Element Ument used in for the planedegrees of fris less sensit
e to bending.
n size of the for the teeth
nd steel). Th
. Finite elem
Axial joint c6] and (c) ge
s were madeteeth were nore modeled af the plate. Bin for the mo
d is 0.01 mmbetween the wating the nodomplished in
Used in thethe model is
e strain modereedom – trative to geom.
e element is fh in bendinge resulting m
ment model,
onsidered ineometry and
in modelingot considereas flat rectan
Because of syodel (Figure
m smaller thawood and th
des on the wonside the soft
e Model s CPE3 availel is solid co
anslation in tmetrical disto
fixed at 0.5 mg. The same mmesh is show
(a) meshed
n this study ateeth layout
g the geometed in modelinngular surfacymmetry, on
1c).
an the thicknhe plate. Fromood (initiallytware.
lable in the Aontinuum 3-nthe x and y dortions, whic
mm. This sizmesh density
wn in Figure
(a)
(b)
metal plate,
(c)
and tested byt of the metal
try of the plang. The teetces having a ne-fourth of t
ness of the tom the start, gy “inside” th
ABAQUS libnode triangudirections. Bch could pote
ze assures, ay was used f2.
(b) meshed
y Riley and Gl plate.
ate. The slotth are twistedthickness eq
the joint is u
ooth. This wogood contact
he steel) to th
brary [7]. Thular element. ecause of itsentially happ
at least, two lfor both part
wood memb
Gebremedhin
ts created d and taperequal to the used as the
ould allow t is he metal-plat
he element Each node
s triangular pen to the
layers of ts of the joint
ber.
n
ed
te
t
3.6 Contact
Load transfer between teeth and wood occurs at the contact interfaces. Contact interface is defined by two surfaces, one for the wood and the other for the metal plate. The required contact elements are internally defined by the software.
ABAQUS requires that one of the surfaces to be defined as “master” and the other surface as “slave”. The specification of the surfaces is critical because of the way the surface interactions are discretized. For each node on the slave surface, ABAQUS attempts to find the closest point on the master surface of the contact pair where the normal of the master surface passes through the node on the slave surface. The interaction is then discretized between the point on the master surface and the slave node. In the model, the surface corresponding to the metal plate is defined as master, and the wood is defined as the slave (see Figure 3 for definition of contact surfaces).
Figure 3. Definition for contact surfaces.
A “hard” contact formulation is employed for the properties of the contact elements. This relationship minimizes the penetration of slave nodes into the master surface and does not allow transfer of tensile stress across the interface. The classical Lagrange multiplier method was applied to enforce no penetration between the surfaces. When the surfaces are in contact, any contact pressure can be transmitted between them. When the contact pressure reduces to zero, the surfaces separate. Once contact is achieved, the related nodes are allowed to separate again.
In addition to pressing on the wood, the teeth may also slip and transmit tangential forces. A basic isotropic Coulomb friction model with a coefficient of friction equal to 0.5 was used. In this model, for the sake of simplicity, the same static and kinetic friction coefficients were assumed. No shear limit is indicated, therefore, any tangential force could be transferred.
A finite sliding model formulation is applied. This formulation allows the defined contact surfaces to separate and slide with finite amplitude and arbitrary rotation.
As mentioned previously, the hole in the wood is made a little bit smaller (by 0.01 mm) than the thickness of the idealized tooth. This assures an initial contact between wood and tooth. The initial contact is adjusted automatically by the finite element program by “moving” the over passing nodes to the exact contact position. This technique assures the necessary initial contact.
4. Results and Discussion
The predicted results were compared against test results of Riley and Gebremedhin [6]. The test results were based on two wood species (Southern Yellow Pine and Spruce Pine Fir). Riley and Gebremedhin [6] experimentally obtained the modulus of elasticity of these species
and reporPine. The
The displidentifiedsymmetrytooth.
Figu
The predcorresponthereforeare comp
Table 1. wood truvalues.
The calcumeasuredwithin 8.deformatwood. Th
The loadrelationshmetal pla
rted: 8.49 Me same value
lacement of d by the twoy below the
re 4. Model
dicted node dnding force
e, calculated pared in Tabl
Measured auss joint. The
LumSpruce Southe Southe 1 From
ulated stiffned stiffness va7% differention due to bhe other nod
-displacemehip is almostate was estab
MPa for Spruces were used
the joint wa nodes showlast tooth, an
definition an
displacement( hF ) is equaby dividing le 1.
and predictede values in th
mber Species e Pine Fur
ern Yellow Pin
ern Yellow Pin
[6]
ess values foalues. The stce of the me
bending of alde location, h
ent relationsht linear. The
blished from
ce Pine Fir, d in the mode
as calculated wn in Figure
nd the secon
nd node loca
t ( hΔ ) is equal to the reac
Fh by hΔ . T
d stiffness vahe parenthes
Wood MOE (MPa)8.49
ne 10.85
ne 15.17
or the two notiffness at Neasured valull teeth, axialhowever, doe
hips for the te plots show
m the very be
and 10.85 anel herein.
at two locat4. Node NA
nd node (NB)
ations where
ual to one-haction force atThe predicted
alues for mesis are the pe
Measuredstiffness1
(kN/mm)21.3
29.8
35.9
odes ( NA anode NA is wes. The local extension oes not take a
three MOE vthat good coginning.
nd 15.17 MP
tions. These is located al
) is located a
e stiffness va
alf the displat the node. Td and measu
etal-plate conercent differe
d
Predicteat specif
(kNNA
22.22 (+4%) 29.69 (-0.4%) 36.67 (+2%)
nd NB ) are reithin 2% difation of Nodof the plate, all these com
values are giontact betwe
Pa for South
two locationlong the axisat the tip end
alues were ca
acement of thThe effectiveured [6] stiffn
nnected tensence from th
ed stiffness fied nodes
N/mm)NB
19.48 (-9%) 26.7
(-10%) 33.41 (-7%)
easonably clfference and de NA accounand deforma
mponents into
iven in Figureen wood and
ern Yellow
ns are s of d of the last
alculated.
he joint. Thee stiffness is,ness values
ion splice he measured
lose to the that of NB is
nts for ation of the o account.
re 5. The d teeth of th
e
s
e
Figu
The calcurespectivdecreasesdisplacemformed inuniform dformulatiteeth to b
Figure 6
re 5. Load-d
ulated stressvely. As the rs. The teeth ment at this ln the wood bdistribution ion of the mbe the same.
6. Stress distr
displacemen
distributionrow of teeth closest to thlocation (NAbetween teetof stress in t
model. The m
ribution in th
nt curves for
ns in the wooapproaches
he gap are thuA) was not acth holes whethe teeth doe
model only as
he wood for =
three MOE
od and metalthe joint gap
us least loadccurately preen there are tes not invalidssumed that t
MOE = 15.= 50).
values of th
l plate are shp, the magni
ded. That is wedicted. A dtwo adjacentdate the assuthe force dis
17 MPa (sca
e tension-sp
hown in Figuitude of the swhy the preddiagonal strest rows of teeumption madstribution in
ale of the def
plice joint.
ures 6 and 7,stress dicted ss field is
eth. This nonde in each row of
formed shap
,
n-
f
pe
Figure 7
5. Co
A simpleconnectecommercof the intwere com
6. R [1] A
m43
[2] G
tr [3] R
co88
[4] T
wW
[5] Pu
of [6] R
pl [7] A
7. Stress dis
onclusions
e and accuratd tension-sp
cial computeterface of wompared again
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urdue Reseaf Forestry an
Riley G.J., anlate connecte
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tribution in
s
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arch Foundatnd Natural R
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ersion 6.5. H
the metal plashap
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estructive tengineering 1
White R.N. “ous members
ional design1-1985. Trus
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entation.
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esting of met16, 1990, pp
Semi-rigid as”, Trans. of
n standard foss Plate Insti
uctures Analyersity.
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Pa (scale of
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Modeling thmethod”, Tra
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analysis of mf ASAE 36(3)
r metal-plateitute, Madiso
yzer”, 1993,
fness model o999, pp. 761-
the deformed
tal-plate US ood contact iffness valueercent.
he interface oans. of ASAE
nnected wood2.
metal plate-), 1993, pp.
e-connected on,
Department
of metal--770.
d
es
of E,
d
t