Multiple scale eigendeformation-based reduced order homogenization
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Transcript of Multiple scale eigendeformation-based reduced order homogenization
Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038
Contents lists available at ScienceDirect
Comput. Methods Appl. Mech. Engrg.
journal homepage: www.elsevier .com/locate /cma
Multiple scale eigendeformation-based reduced order homogenization
Zheng Yuan, Jacob Fish *
Multiscale Science and Engineering Center, Rensselaer Polytechnic Institute, CII 7129 110 8th St., Troy, NY 12180, United States
a r t i c l e i n f o
Article history:Received 24 February 2008Received in revised form 29 August 2008Accepted 31 December 2008Available online 23 January 2009
Keywords:Homogenization model-reductioneigendeformation
0045-7825/$ - see front matter � 2009 Elsevier B.V. Adoi:10.1016/j.cma.2008.12.038
* Corresponding author. Tel.: +1 518 276 6191.E-mail address: [email protected] (J. Fish).
a b s t r a c t
Multiple scale eigendeformation-based reduced order homogenization method, which provides consider-able computational cost saving in comparison to the direct homogenization method, has been developed,verified against the direct homogenization method, and validated against experimental data. The salientfeature of the method is in the formulation of the unit cell problem in terms of residual-free stresses, andtherefore eliminating the need for costly equilibrium calculations required by the direct homogenizationmethod. This is accomplished by introducing discretized eigendeformation fields at different scales,which are collectively referred to as eigenstrains and eigenseparations, and then precomputing asequence of elasticity solutions of the unit cell problem subjected to the eigendeformation fields priorto nonlinear analysis.
� 2009 Elsevier B.V. All rights reserved.
1. Introduction
Since the pioneering works of and Hill [1], Babuska [2], Benssousan [3] and Sanchez-Palencia [4], homogenization methods made sig-nificant strides, recently finding their way into industrial arena. The new comers are the so-called direct computational homogenizationand direct mathematical homogenization approaches. The direct computational homogenization approach, based on the Hill–Mandel rela-tion [5] in combination with numerical methods (see [6–24] for closely related methods), followed the homogenization approach set fourthby Hill [1]. The direct mathematical homogenization approaches, based on the multiple scale asymptotic expansion methods in combina-tion with numerical methods [25–30] follow the formulation pathway set in [2–4].
While computational cost of the direct computational and mathematical homogenization approaches is a small fraction compared tothe direct numerical simulation where a characteristic mesh size is of the heterogeneity order they remain computationally prohibitivefor large scale nonlinear problems. This is because a nonlinear unit cell problem for a two-scale problem has to be solved number of timesequal to the product of number of quadrature points at a coarse scale times the number of load increments and iterations at the coarsescale. With each additional scale the number of times a finest scale unit cell problem has to be solved is increased by a factor equal tothe product of number of quadrature points, load increments and iterations at a previous scale.
It is therefore necessary to reduce the computational complexity of the fine scale problem without significantly compromising on thesolution accuracy of interest, which is typically at the system level. The method presented in this manuscript is a generalization of the two-scale eigendeformation-based approach developed in [31] in the following three respects:
1. The two-scale mathematical framework in [31] is extended to multiple-scales with equations explicitly derived for three scales denotedhereafter as macro, meso and micro.
2. The formulation in [31] was hard-wired to continuum damage mechanics at the fine scale. The present manuscript extends it to arbi-trary inelastic deformation of micro phases and interfaces.
3. Numerical Greens-functions in [31] were developed on the element-by-element basis. The present manuscript is based on the partition-by-partition representation of numerical Greens functions, which results in considerable computational cost savings.
The manuscript is organized as follows. In Section 2, the three-scale mathematical homogenization formulation is developed. The gov-erning equations are reformulated in terms of residual-free stresses based on analytical influence (Green’s) functions in Section 3. Section 4presents a reduced order model based on the partition-by-partition representation of numerical influence functions. Solution of a system ofnonlinear equations corresponding to the micro and meso scales is described in Section 5. Derivation of the two-scale formulation as a
ll rights reserved.
Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038 2017
special case of the multiple scale formulation is considered in Section 6. Convergence studies of the reduced order model to the directhomogenization are conducted in Section 7. Validation studies on tube crush tests conclude the manuscript.
2. Three-scale mathematical homogenization
Mathematical homogenization is an upscaling technique by which one starts with governing equations at the finest scale of interest andthen scale-by-scale derives coarser scale equations. The strong form of the boundary value problem on the finest (micro) scale of interest isgiven by
rfij;jðxÞ þ bf
i ðxÞ ¼ 0 x 2 X; ð1Þ
rfijðxÞ ¼ Lf
ijklðxÞ efklðxÞ �
XI
IlfklðxÞ
" #x 2 X; ð2Þ
efijðxÞ ¼ uf
ði;jÞðxÞ �12ðuf
i;j þ ufj;iÞ x 2 X; ð3Þ
ufi ðxÞ ¼ �uiðxÞ x 2 Cu; ð4Þ
rfijðxÞnjðxÞ ¼ �tiðxÞ x 2 Ct; ð5Þ
dfi ðxÞ � suf
i ðxÞt ¼ ufi jSf�� uf
i jSfþ
x 2 Sf; ð6Þ
rfijnjjSf
þþ rf
ijnjjSf�¼ tf
i jSfþþ tf
i jSf�¼ 0; ð7Þ
where the superscript f denotes dependence of the response field on the microstructural heterogeneities. Constitutive relations described inEq. (2) are assumed to admit an additive decomposition of total strains ef
ij into elastic and inelastic components (or more generally stated aseigenstrains Ilf
klÞ; the left superscript I indicates different types of eigenstrains, such as inelastic deformation (damage, plasticity, etc.), ther-mal changes, moisture effects and phase transformation. Sf in Eqs. (6) and (7) denotes the interface between the micro-constituents with Sf
þand Sf
� denoting the two sides of the interface. dfi in Eq. (6) is the displacement jump along the interface, and s � t is the jump operator. The
traction continuity along the interface is given by Eq. (7).We assume existence of material heterogeneity at two different scales as schematically illustrated in Fig. 1. Making the usual assump-
tion of scale separation, an approximate solution of Eqs. (12), (3)–(7) is sought of within the framework of the mathematical homogeni-zation theory where material heterogeneity is expressed in terms of locally periodic representative volume elements (RVEs or unitcells) at the meso- and the micro-scales. The volume of the unit cells at the two scales are denoted by Hy and Hz, respectively. The cor-responding interfaces in the meso and micro unit cells are denoted by Sy and Sz, respectively. Two additional position vectors, y � x=fin Hy and z � y=f in Hz, are introduced to track the position of a point at any scale, where 0 < f� 1. Any locally periodic function canbe represented in terms of the two position vectors as
/fðxÞ � /ðx; y; zÞ: ð8Þ
The indirect spatial derivative is calculated by the chain rule as
/f;iðxÞ ¼ /;xi
ðx; y; zÞ þ 1f
/;yiðx; y; zÞ þ 1
f2 /;ziðx; y; zÞ; ð9Þ
where a comma followed by a subscript variable xi, yi or zi denotes the partial derivative with respect to the macro, meso or micro positionvector.
A three-scale asymptotic expansion is employed to approximate the displacement field
uiðx; y; zÞ ¼ u0i ðxÞ þ fu1
i ðx; yÞ þ f2u2i ðx; y; zÞ þ � � � ð10Þ
Using the chain rule of the differentiation (9) and the kinematical relation (3), the asymptotic expansion of the strain field can be expressedas
eijðx; y; zÞ ¼ e0ijðx; y; zÞ þ fe1
ijðx; y; zÞ þ f2e2ijðx; y; zÞ þ � � � ð11Þ
Fig. 1. Three-scale representation of a heterogeneous material [27].
2018 Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038
with the leading order strain given as
e0ijðx; y; zÞ ¼ u0
ði;xjÞðxÞ þ u1ði;yjÞðx; yÞ þ u2
ði;zjÞðx; y; zÞ: ð12Þ
The macro strain is defined as an average strain over Hy �Hz. With consideration of periodicity at the two scales it is given as
emacij ðxÞ �
1jHyj
1jHzj
ZHy
ZHz
e0ijðx; y; zÞdHzdHy ¼ u0
ði;xjÞðxÞ: ð13Þ
The meso strain is defined as an average strain over Hz. Assuming periodicity at the micro scale it is given as
emesoij ðx; yÞ � 1
jHzj
ZHz
e0ijðx; y; zÞdH ¼ u0
ði;xjÞðxÞ þ u1ði;yjÞðx; yÞ ¼ emac
ij ðxÞ þ u1ði;yjÞðx; yÞ: ð14Þ
Thus the micro scale strain can be expressed as
emicij ðx; y; zÞ � e0
ijðx; y; zÞ ¼ u0ði;xjÞðxÞ þ u1
ði;yjÞðx; yÞ þ u2ði;zjÞðx; y; zÞ ¼ emeso
ij ðx; yÞ þ u2ði;zjÞðx; y; zÞ: ð15Þ
Throughout the manuscript the superscripts mic, meso and mac are used to denote quantities at different scales.The asymptotic expansion of the stress field is given as
rijðx; y; zÞ ¼ r0ijðx; y; zÞ þ fr1
ijðx; y; zÞ þ f2r2ijðx; y; zÞ þ � � � ð16Þ
where the leading order stress is given by
r0ijðx; y; zÞ ¼ Lijklðy; zÞ e0
klðx; y; zÞ �X
I
Ilklðx; y; zÞ" #
: ð17Þ
The micro-, meso- and macro-stresses are defined as
rmicij ðx; y; zÞ � r0
ijðx; y; zÞ; ð18Þ
rmesoij ðx; yÞ � 1
jHzj
ZHz
rmicij ðx; y; zÞdH; ð19Þ
rmacij ðxÞ �
1jHyj
ZHy
rmesoij ðx; yÞdH: ð20Þ
Inserting the asymptotic expansion of the stress field (16) into the equilibrium (1) and identifying terms with equal powers of f gives variousorder equilibrium equations
Oðf�2Þ : r0ij;zjðx; y; zÞ ¼ 0; ð21Þ
Oðf�1Þ : r0ij;yjðx; y; zÞ þ r1
ij;zjðx; y; zÞ ¼ 0; ð22Þ
Oðf0Þ : r0ij;xjðx; y; zÞ þ r1
ij;yjðx; y; zÞ þ r2
ij;zjðx; y; zÞ þ bi ¼ 0: ð23Þ
Using the definition (18) and Eq. (21), the micro equilibrium equation can be restated as
Oðf�2Þ : rmicij;zjðx; y; zÞ ¼ 0 : ð24Þ
Integrating Eq. (22) over Hz, exploiting periodicity at the microscale and using the definition (19) yields the meso equilibrium
Oðf�1Þ : rmesoij;yjðx; yÞ ¼ 0 : ð25Þ
Integrating Eq. (23) over Hz and Hy, exploiting periodicity at the micro and meso scales and using the definition (20) yields the equilibriumequation at the macro scale
Oðf0Þ : rmacij;xjðxÞ þ �bi ¼ 0 ; ð26Þ
where
�bi ¼1jHyj
1jHzj
ZHy
ZHz
bi dHz dHy: ð27Þ
For more details on the three-scale mathematical homogenization the reader is referred to [27].
3. Residual-free governing equations
In this section, we formulate equilibrium equations in terms of equilibrated (or residual-free) micro and meso stresses. By this approachthe computational bottle neck of solving large discrete system equilibrium equations corresponding to the unit cell problems is removed.
Using the definitions (18) and (15) together with the constitutive relation (16), the equilibrium equation at the micro scale (24) can beexpressed as
Lmicijkl ðy; zÞ emeso
kl ðx; yÞ þ u2ðk;zlÞðx; y; zÞ �
XI
Ilklðx; y; zÞ" #( )
;zj
¼ 0: ð28Þ
Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038 2019
Following [31], the micro displacement field is decomposed using the elastic influence function Hmicikl , the eigenstrain influence function hmic l
ikl
and the eigenseparation influence function hmic din as
u2i ðx; y; zÞ ¼ u2e
i ðx; y; zÞ þX
I
Iu2li ðx; y; zÞ þ u2d
i ðx; y; zÞ
¼ Hmicikl ðy; zÞemeso
kl ðx; yÞ þZ
Hz
hmic likl ðy; z; zÞ
XI
Ilklðx; y; zÞdHþZ
Sz
hmic din ðy; z; zÞdnðx; y; zÞdS; ð29Þ
where the influence (or Green’s) functions Hmicikl , hmic l
ikl and hmic din are computed by solving a sequence of elastic boundary value problems
independent of and prior to the nonlinear macro analysis. The subscript n in the eigenseparation influence function denotes the componentin the local Cartesian coordinate system of the interface. The expression similar to the second term in (29) can be found in [32]. These func-tions are chosen to satisfy the equilibrium Eq. (28) for arbitrary emeso
kl ðx; yÞ, Ilklðx; y; zÞ and dnðx; y; zÞ.The governing equation for the elastic influence function Hmic
ikl is obtained by substituting (29) into (28) for vanishing eigendeformationIlklðx; y; zÞ, dnðx; y; zÞ and arbitrary meso strain emeso
kl ðx; yÞ
fLmicijkl ðy; zÞ½Iklmnðy; zÞ þ Gmic
klmnðy; zÞ�g;zj¼ 0; y 2 Hy; z 2 Hz; ð30Þ
where
Gmicijkl ðy; zÞ ¼ Hmic
ði;zjÞklðy; zÞ ð31Þ
and Iijkl is the fourth order identity tensor.The governing equation for the eigenstrain influence function hmic l
ikl is obtained by substituting (29) into (28), assuming vanishingdnðx; y; zÞ and emeso
kl ðx; yÞ, and eigenstrain Ilklðx; y; zÞ in the form of the Dirac delta function, which gives
fLmicijkl ðy; zÞ½g
mic lklmn ðy; z; zÞ � Iklmnðy; zÞdðy; z� zÞ�g;zj
¼ 0; y 2 Hy; z; z 2 Hz; ð32Þ
where
gmic lijkl ðy; z; zÞ ¼ hmic l
ði;zjÞklðy; z; zÞ ð33Þ
and d is the Dirac delta function.Similarly, the governing equation for the eigenseparation influence function hmic d
in is obtained by substituting (29) into (28), assumingvanishing eigenstrain and meso strain, and eigenseparation in the form of the Dirac delta function, which gives
fLmicijkl ðy; zÞgmic d
kln ðy; z; zÞg;zj¼ 0; y 2 Hy; z 2 Hz; z 2 Sz;
E:B:C: dnðy; ~zÞ ¼ dðy; ~z� zÞ; ~z 2 Sz;ð34Þ
where
gmic dijn ðy; z; zÞ ¼ hmic d
ði;zjÞn ðy; z; zÞ ð35Þ
and dnðy; ~zÞ is the displacement jump along the interface at the micro scale defined in the local interface Cartesian coordinate system.Note that the relation between elastic and eigenstrain polarization functions can be found by integrating (32) over z 2 Hz, which gives
ZHz
gmic lijkl ðy; z; zÞdH ¼ �Gmic
ijkl ðy; zÞ; ð36Þ
where we have exploited the relationR
HzIijklðy; zÞdðy; z� zÞdH ¼ Iijklðy; zÞ.
The residual-free micro stress ðrmicij;zj¼ 0Þ follows from Eqs. (28) and (29)
rmicij ¼ Lmic
ijkl ðy; zÞ
Amicklmnðy; zÞemeso
mn ðx; yÞþR
Szgmic d
kln ðy; z; zÞdnðx; y; zÞdS
þR
Hzgmic l
klmn ðy; z; zÞP
I
Ilmnðx; y; zÞdH�P
I
Ilklðx; y; zÞ
26664
37775; ð37Þ
where
Amicijkl ðy; zÞ ¼ Iijklðy; zÞ þ Gmic
ijkl ðy; zÞ: ð38Þ
Using the definitions (19), (14) and the residual-free micro stress (37), the meso equilibrium Eq. (25) can be expressed in terms of the mesoeigenstrains as
fLmesoijkl ðyÞ½emac
kl ðxÞ þ u1ðk;ylÞðx; yÞ � lmeso
kl ðx; yÞ�g;yj¼ 0; ð39Þ
where
Lmesoijkl ðyÞ ¼
1jHzj
ZHz
Lmicijmnðy; zÞA
micmnklðy; zÞdH: ð40Þ
2020 Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038
The meso eigenstrain is related to the micro eigendeformation by
lmesoij ðx; yÞ ¼ �½Lmeso
ijst ðyÞ��1 1jHzj
ZHz
Lmicstmnðy; zÞ
RSz
gmic dmnn ðy; z; zÞdnðx; y; zÞdS
þR
Hzgmic l
mnkl ðy; z; zÞP
I
Ilklðx; y; zÞdH
�P
I
Ilmnðx; y; zÞ
266664
377775
8>>>><>>>>:
9>>>>=>>>>;
dH: ð41Þ
Note that while the meso eigenstrain is completely determined by micro eigendeformation, the meso eigenseparation is independent of microeigendeformation. The meso displacement u1
i ðx; yÞ assumes a similar decomposition to that of the micro deformation u2i ðx; yÞ given in (29)
u1i ðx; yÞ ¼ u1e
i ðx; yÞ þ u1li ðx; yÞ þ u1d
i ðx; yÞ ¼ Hmesoikl ðyÞemac
kl ðxÞ þZ
Hy
hmeso likl ðy; yÞlmeso
kl ðx; yÞdHþZ
Sy
hmeso din ðy; yÞdmeso
n ðx; yÞdS: ð42Þ
The meso influence functions are defined to satisfy equilibrium at mesoscale (39) for arbitrary emackl ðxÞ, lmeso
kl ðx; yÞ and dmeson ðx; yÞ.
For the elastic influence function Hmesoikl ðyÞ, we have
fLmesoijkl ðyÞ½IklmnðyÞ þ Gmeso
klmn ðyÞ�g;yj¼ 0; y 2 Hy; ð43Þ
where
Gmesoijkl ðyÞ ¼ Hmeso
ði;yjÞklðyÞ: ð44Þ
The eigenstrain influence function hmeso likl ðy; yÞ are given as
fLmesoijkl ðyÞ½g
meso lklmn ðy; yÞ � IklmnðyÞdðy � yÞ�g;yj
¼ 0; y; y 2 Hy; ð45Þ
where
gmeso lijkl ðy; yÞ ¼ hmeso l
ði;yjÞkl ðy; yÞ: ð46Þ
Similarly to Eq. (36), we have the following relation between the elastic and eigenstrain polarization functions
ZHzgmeso lijkl ðy; z; zÞdH ¼ �Gmeso
ijkl ðy; zÞ: ð47Þ
For the eigenseparation influence function hmeso din ðy; yÞ, we have
fLmesoijkl ðyÞgmeso d
kln ðy; yÞg;yj¼ 0; y 2 Hy; y 2 Sy;
E:B:C: dnð~yÞ ¼ dð~y � yÞ; ~y 2 Sy;ð48Þ
where
gmeso dijn ðy; yÞ ¼ hmeso d
ði;yjÞn ðy; yÞ: ð49Þ
Using Eqs. (39) and (42) the resulting residual-free meso stress ðrmesoij;yj¼ 0Þ is given as
rmesoij ¼ Lmeso
ijmn ðyÞAmeso
mnkl ðyÞemackl ðxÞ
þR
Sygmeso d
mnn ðy; yÞdmeson ðx; yÞdS
þR
Hygmeso l
mnkl ðy; yÞlmesokl ðx; yÞdH� lmeso
mn ðx; yÞ
2664
3775; ð50Þ
where
Amesoijkl ðyÞ ¼ IijklðyÞ þ Gmeso
ijkl ðyÞ: ð51Þ
4. Formulation of the reduced order model
In this section, we focus on reducing computational complexity of the micro and meso unit cell problems derived in Section 3. This isaccomplished by discretizing the eigendeformation and formulating the residual-free discrete (or reduced order) governing equations.
At the micro scale, the micro eigenstrains are discretized in terms of piecewise constant shape function NðazÞðzÞ as
Ilijðx; y; zÞ ¼Xnz
az¼1
NðazÞðzÞIlmicðazÞij ðx; yÞ; ð52Þ
where
NðazÞðzÞ ¼1; z 2 HðazÞ
z ;
0; z R HðazÞz ;
(ð53Þ
IlmicðazÞij ðx; yÞ ¼ 1
jHðazÞz j
ZHðazÞ
z
Ilijðx; y; zÞdH ð54Þ
in which the total volume of the micro unit cell is partitioned into nz nonoverlapping subdomains denoted by HðazÞz . Partitions at various
scales are denoted by a superscript enclosed in parenthesis: ðazÞ; ðbzÞ and ðayÞ; ðbyÞ denote the phase (volume) partitions at the micro andmesoscale, respectively; ðnzÞ; ðgzÞ and ðnyÞ; ðgyÞ denote the interface partitions at the micro and mesoscale, respectively.
Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038 2021
The eigenseparation dnðx; y; ~zÞ is discretized in terms of C0 continuous interface partition shape function NðnzÞð~zÞ as
dnðx; y; ~zÞ ¼Xmz
nz¼1
NðnzÞð~zÞdmicðnzÞn ðx; yÞ; ð55Þ
where NðnzÞð~zÞ is a linear combination of piecewise linear finite element shape functions defined over partition nz
NðnzÞð~zÞ ¼
Pa2Sðnz Þ
z
Na ~zð Þ; ~z 2 SðnzÞz ;
0; ~z R SðnzÞz ;
8><>: ð56Þ
dmicðnzÞn ðx; yÞ ¼ 1
jSðnzÞz j
ZSðnzÞ
z
dnðx; y; ~zÞdS ð57Þ
in which the total interface at the microscale is divided into mz partitions denoted by SðnzÞz , and Nað~zÞ is a linear shape function associated with
a finite element mesh node a along the micro interface. Note that in contrast to the volume partitions, the surface partitions are overlappingas illustrated in Fig. 2 for the case of fibrous unit cell. Fig. 2a depicts the unit cell finite element mesh. Fig. 2b shows the two interface par-titions. The overlapping areas are shown in brown. Fig. 2c and d illustrate the two interface partition shape functions.
Substituting Eqs. (52) and (55) into Eq. (37) yields the reduced order residual-free micro stress
ð58Þ
where
Q micðnzÞijn ðy; zÞ ¼
ZSz
gmic dijn ðy; z; zÞNðnzÞðzÞdS; ð59Þ
SmicðazÞijkl ðy; zÞ ¼ PmicðazÞ
ijkl ðy; zÞ � ImicðazÞijkl ðy; zÞ ð60Þ
and
PmicðazÞijkl ðy; zÞ ¼
ZHz
gmic lijkl ðy; z; zÞN
ðazÞðzÞdH;¼Z
Hðaz Þz
gmic lijkl ðy; z; zÞdH; ð61Þ
ImicðazÞijkl ðy; zÞ ¼
Iijkl; z 2 HðazÞz ;
0; z R HðazÞz :
(ð62Þ
The reduced order influence functions, PmicðazÞklmn ðy; zÞ and QmicðnzÞ
kln ðy; zÞ, can be computed in two ways: (i) directly from Eqs. (59) and (61) incombination with Eq. (32), or by requiring the reduced order micro stress (58) to be residual-free.
By integrating (32) over partition z 2 HðazÞz and exploiting (61) yields
fLmicijkl ðy; zÞ½P
micðazÞklmn ðy; zÞ � ImicðazÞ
klmn ðy; zÞ�g;zj¼ 0; y 2 Hy; z 2 Hz ð63Þ
from which the reduced order eigenstrain influence function can be solved for. Precisely the same expression can be obtained from (58)assuming vanishing meso strain and partitioned eigenseparation dmicðnzÞ
n ðx; yÞ.The governing equation for the reduced order eigenseparation influence function is given by
fLmicijkl ðy; zÞQ
micðnzÞkln ðy; zÞg;zj
¼ 0; y 2 Hy; z 2 Hz;
E:B:C: dnðy; ~zÞ ¼ NðnzÞð~zÞ; ~z 2 Sz:ð64Þ
At the meso scale, the relation between the meso eigenstrain and the reduced order micro eigendeformation is obtained by substituting Eqs.(52) and (55) into Eq. (41), which gives
lmesoij ðx; yÞ ¼
Xnz
az¼1
SmesoðazÞijkl ðyÞ
XI
IlmicðazÞkl ðx; yÞ þ
Xmz
nz¼1
TmesoðnzÞijn ðyÞdmicðnzÞ
n ðx; yÞ; ð65Þ
where
SmesoðazÞijkl ðyÞ ¼ �½Lmeso
ijst ðyÞ��1 1jHzj
ZHz
fLmicstmnðy; zÞS
micðazÞmnkl ðy; zÞgdH; ð66Þ
TmesoðnzÞijn ðyÞ ¼ �½Lmeso
ijmn ðyÞ��1 1jHzj
ZHz
Lmicmnklðy; zÞQ
micðnzÞkln ðy; zÞdH: ð67Þ
Fig. 2. Interface partitions: (a) unit cell mesh; (b) interface partitions; (c) shape function of partition 1; (d) shape function of partition 2.
2022 Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038
The variation of the micro eigendeformation fields IlmicðazÞij ðx; yÞ and dmicðnzÞ
n ðx; yÞ over mesoscale is assumed to be governed by C�1 continuousmesoscale shape functions NðayÞ as
IlmicðazÞij ðx; yÞ ¼
Xny
ay¼1
NðayÞðyÞIlmicðay :azÞij ðxÞ; ð68Þ
dmicðnzÞn ðx; yÞ ¼
Xny
ay¼1
NðayÞðyÞdmicðay :nzÞn ðxÞ; ð69Þ
where
NðayÞðyÞ ¼1; y 2 HðayÞ
y ;
0; y R HðayÞy ;
(ð70Þ
Ilmicðay :azÞij ðxÞ ¼ 1
jHðayÞy j
ZHðay Þy
IlmicðazÞij ðx; yÞdH; ð71Þ
dmicðay :nzÞn ðxÞ ¼ 1
jHðayÞy j
ZHðay Þy
dmicðnzÞn ðx; yÞdH ð72Þ
in which the total volume of the meso unit cell is partitioned into ny nonoverlapping subdomains denoted by HðayÞy . Note that the micro par-
titions az and nz occupy the domain within the meso partition ay and that there could be different micro partitions embedded within variousmeso partitions. Hereafter, such parent–children relation is denoted by colon ‘‘:”.
Similarly to the micro eigenseparations, the meso eigenseparations are discretized as
dmeson ðx; ~yÞ ¼
Xmy
ny¼1
NðnyÞð~yÞdmesoðnyÞn ðxÞ; ð73Þ
where
NðnyÞð~yÞ ¼
Pa2S
ðny Þy
Nað~yÞ; ~y 2 SðnyÞy ;
0; ~y R SðnyÞy ;
8><>: ð74Þ
dmesoðnyÞn ðxÞ ¼ 1
jSðnyÞy j
ZSðny Þy
dmeson ðx; ~yÞdS ð75Þ
in which the meso interface is divided into my partitions denoted by SðnyÞy .
A woven unit cell at the mesoscale and a fibrous unit cell at the microscale depicted in Fig. 3 is used to demonstrate various partitions.At the mesoscale, there are two phase partitions (matrix-1, weave-2) and one interface partition. At the microscale, there are two phasepartitions (matrix-1, fiber-2) and one interface partition. All microscale partitions are within the weave partition at the mesoscale.
Fig. 3. Unit cell partitions at the mesoscale (left) and microscale (right).
Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038 2023
Using Eq. (65), and substituting Eqs. (73), (68) and (69) into Eq. (50) yields the reduced order residual-free meso stress
rmesoij ¼ Lmeso
ijmn ðyÞ
Amesomnkl ðyÞemac
kl ðxÞ þPmy
ny¼1Q mesoðnyÞ
mnn ðyÞdmesoðnyÞn ðxÞ
þPny
ay¼1
Pnz
az¼1Smesoðay :azÞ
mnkl ðyÞP
I
Ilmicðay :azÞkl ðxÞ
þPny
ay¼1
Pmz
nz¼1Tmesoðay :nzÞ
mnn ðyÞdmicðay :nzÞn ðxÞ
26666666664
37777777775; ð76Þ
where
Q mesoðnyÞijn ðyÞ ¼
ZSðny Þy
gmeso dijn ðy; yÞNðnyÞðyÞdS; ð77Þ
Smesoðay :azÞijkl ðyÞ ¼ Pmesoðay :azÞ
ijkl ðyÞ � ImesoðayÞijmn ðyÞSmesoðazÞ
mnkl ðyÞ; ð78Þ
Tmesoðay :nzÞijn ðyÞ ¼ Q mesoðay :nzÞ
ijn ðyÞ � ImesoðayÞijkl ðyÞTmesoðnzÞ
kln ðyÞ ð79Þ
and
Pmesoðay :azÞijkl ðyÞ ¼
ZHðay Þy
gmeso lijmn ðy; yÞSmesoðazÞ
mnkl ðyÞdH; ð80Þ
Q mesoðay :nzÞijn ðyÞ ¼
ZHðay Þy
gmeso lijkl ðy; yÞTmesoðnzÞ
kln ðyÞdH; ð81Þ
ImesoðayÞijkl ðyÞ ¼
Iijkl; y 2 HðayÞy ;
0; y R HðayÞy :
(ð82Þ
In the above, ‘‘Q” is used to indicate polarization functions associated with the two eigenseparation fields. The superscripts ðay : nzÞ and ðnyÞare used to distinguish between the association with the micro eigenseparations and meso displacements, respectively.
The reduced order eigenstrain influence functions are computed by solving the following elasticity problem
fLmesoijkl ðyÞ½P
mesoðay :azÞklmn ðyÞ � ImesoðayÞ
klst ðyÞSmesoðazÞstmn ðyÞ�g;yj
¼ 0; y 2 Hy; ð83Þ
fLmesoijkl ðyÞ½Q
mesoðay :nzÞkln ðyÞ � ImesoðayÞ
klmn ðyÞTmesoðnzÞmnn ðyÞ�g;yj
¼ 0; y 2 Hy: ð84Þ
It can be seen that solution of the meso eigenstrain influence function requires a priori solutions of the micro scale eigendeformation influ-ence functions (recall the definitions (66) and (67)).
The reduced order eigenseparation influence functions are computed from
fLmesoijkl ðyÞQ
mesoðnyÞkln ðyÞg;yj
¼ 0; y 2 Hy;
E:B:C: dnð~yÞ ¼ NðnyÞð~yÞ; ~y 2 Sy:ð85Þ
Finally, from the reduced order meso stress (76) and the definition (20), the macro stress can be expressed in terms of the micro- and meso-eigendeformation as
rmacij ¼ Lmac
ijkl emackl ðxÞ þ
Pmy
ny¼1Q macðnyÞ
ijn dmesoðnyÞn ðxÞ þ
Pny
ay¼1
Pnz
az¼1Smacðay :azÞ
ijkl
PI
Ilmicðay :azÞkl ðxÞ þ
Pny
ay¼1
Pmz
nz¼1Tmacðay :nzÞ
ijn dmicðay :nzÞn ðxÞ ; ð86Þ
Table 1Summary of the influence function problems for the three-scale analysis.
Governing equation Solution tensor Calculated tensor(s)
Micro elastic (30) Gmicijkl Amic
ijkl (38), Lmesoijkl (40)
Micro eigenstrain (63) PmicðazÞijkl SmicðazÞ
ijkl (60), SmesoðazÞijkl (66)
Micro eigenseparation (64) QmicðnzÞijn TmesoðnzÞ
ijn (67)
Meso elastic (43) Gmesoijkl Ameso
ijkl (51), Lmacijkl (87)
Meso eigenstrain (83); (84) Pmesoðay :azÞijkl ; Qmesoðay :nzÞ
ijn Smesoðay :azÞijkl (78), Smacðay :azÞ
ijkl (89); Tmesoðay :nzÞijn (79), Tmacðay :nzÞ
ijn (90)
Meso eigenseparation (85) QmesoðnyÞijn QmacðnyÞ
ijn (88)
2024 Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038
where
Lmacijkl ¼
1jHyj
ZHy
Lmesoijmn ðyÞA
mesomnkl ðyÞdH; ð87Þ
QmacðnyÞijn ¼ 1
jHyj
ZHy
Lmesoijkl ðyÞQ
mesoðnyÞkln ðyÞdH; ð88Þ
Smacðay :azÞijkl ¼ 1
jHyj
ZHy
Lmesoijmn ðyÞS
mesoðay :azÞmnkl ðyÞdH; ð89Þ
Tmacðay :nzÞijn ¼ 1
jHyj
ZHy
Lmesoijkl ðyÞT
mesoðay :nzÞkln ðyÞdH: ð90Þ
To this end, Table 1 summarizes all the coefficient tensors needed to be precomputed for the reduced order model. The salient feature of themethod is that the influence functions can be obtained by approximately solving the corresponding elastic boundary value problem using thefinite element method independent of and prior to the nonlinear macro analysis. Once the influence functions have been computed, allthe coefficient tensors of the reduced order model can be calculated. Since these computations are independent of the nonlinear macroanalysis, they are precomputed in the preprocessing stage.
5. Solving the reduced order unit cell problems
Since all the coefficient tensors of the reduced order model can be precomputed prior to macro analysis, only partitioned eigendefor-mations d
mesoðnyÞn ðxÞ, Ilmicðay :azÞ
kl ðxÞ and dmicðay :nzÞn ðxÞ need to be updated at each increment of macro analysis. The constitutive relations at the
finest scale of interest are assumed to be known based on the material models of phases and interfaces
Ilmicij ðx; y; zÞ ¼ f micðemic
ij ðx; y; zÞ;rmicij ðx; y; zÞÞ; ð91Þ
tmicn ðx; y; zÞ ¼ gmicðdmic
n ðx; y; zÞÞ; ð92Þtmeso
n ðx; y; zÞ ¼ gmesoðdmeson ðx; y; zÞÞ; ð93Þ
where
Ilmicij ðx; y; zÞ � Ilijðx; y; zÞ; ð94Þ
dmicij ðx; y; zÞ � dijðx; y; zÞ ð95Þ
and tmicn and tmeso
n are the micro and meso tractions in the corresponding local interface coordinate system.Consider the micro strain field first. Referring to the reduced order micro stress (58)the micro strain is given as
emicij ðx; y; zÞ ¼ Amic
ijkl ðy; zÞemesokl ðx; yÞ þ
Xnz
az¼1
PmicðazÞijkl ðy; zÞ
XI
IlmicðazÞkl ðx; yÞ þ
Xmz
nz¼1
Q micðnzÞijn ðy; zÞdmicðnzÞ
n ðx; yÞ: ð96Þ
Applying the averaging operator 1jHðbzÞ
z j
RHðbzÞ
z�dH on both sides of (96) yields
emicðbzÞij ðx; yÞ ¼ AmicðbzÞ
ijkl ðyÞemesokl ðx; yÞ þ
Xnz
az¼1
Pmicðbz�azÞijkl ðyÞ
XI
IlmicðazÞkl ðx; yÞ þ
Xmz
nz¼1
Q micðbz�nzÞijn ðyÞdmicðnzÞ
n ðx; yÞ; ð97Þ
where
Pmicðbz�azÞijkl ðyÞ ¼
1jHðbz Þ
z j
RHðbz Þ
zPmicðazÞ
ijkl ðy; zÞdH if bz;az 2 the same Hz;
0 else;
(ð98Þ
Q micðbz�nzÞijn ðyÞ ¼
1jHðbz Þ
z j
RHðbz Þ
zQ micðnzÞ
ijn ðy; zÞdH if bz; nz 2 the same Hz;
0 else:
(ð99Þ
Note that the integrals in (98) and (99) are defined only when bz and az (or nz) belong to the same micro unit cell. We use the symbol ‘‘�” toindicate this sibling relation.
Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038 2025
Referring to the reduced order meso stress (76), the meso strain is given as
emesoij ðx; yÞ ¼ Ameso
ijkl ðyÞemackl ðxÞ þ
Xmy
ny¼1
Q mesoðnyÞijn ðyÞdmesoðnyÞ
n ðxÞ þXny
ay¼1
Xnz
az¼1
Pmesoðay :azÞijkl ðyÞ
XI
Ilmicðay :azÞkl ðxÞ
þXny
ay¼1
Xmz
nz¼1
Q mesoðay :nzÞijn ðyÞdmicðay :nzÞ
n ðxÞ: ð100Þ
Substituting Eqs. (100), (68) and (69) into Eq. (97) yields
emicðbzÞij ðx; yÞ ¼ AmicðbzÞ
ijkl ðyÞAmesoklmn ðyÞemac
mn ðxÞ þXmy
ny¼1
AmicðbzÞijkl ðyÞQmesoðnyÞ
kln ðyÞdmesoðnyÞn ðxÞ
þXny
ay¼1
Xnz
az¼1
AmicðbzÞijmn ðyÞPmesoðay :azÞ
mnkl ðyÞ
þPmicðbz�azÞijkl ðyÞNðayÞðyÞ
24
35X
IIlmicðay :azÞ
kl ðxÞ
|fflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflffl{zfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflfflffl}Xmicðbz Þ
ij
þXny
ay¼1
Xmz
nz¼1
AmicðbzÞijkl ðyÞQ mesoðay :nzÞ
kln ðyÞ
þQ micðbz�nzÞijn ðyÞNðayÞðyÞ
24
35dmicðay :nzÞ
n ðxÞ: ð101Þ
The partitioned micro eigenstrain Ilmicðay :azÞkl on emicðbzÞ
ij can be better understood by writing out the third term of RHS of Eq. (101) as
XmicðbzÞij ðx; yÞ ¼
Pmicðbz�azÞijkl ðyÞþAmicðbzÞ
ijmn ðyÞPmesoðay :azÞmnkl ðyÞ
" #PI
Ilmicðay :azÞkl ðxÞ for bz � az;
AmicðbzÞijmn ðyÞPmesoðay :azÞ
mnkl ðyÞP
I
Ilmicðay :azÞkl ðxÞ otherwise;
8>>><>>>: ð102Þ
where bz � az denote that partitions az and bz belong to the same unit cell. It can be seen that the partitioned micro eigenstrain from thesame micro unit cell ðbz � azÞ influences the micro strain emicðbzÞ
ij ðx; yÞ in the following two ways: (i) through a direct influence within themicro unit cell ðPmicðbz�azÞ
ijkl Þ and (ii) by indirect influence through meso scale ðAmicðbzÞijmn Pmesoðay :azÞ
mnkl Þ. All the partitioned micro eigenstrains fromother micro unit cell(s) influence through the meso scale ðAmicðbzÞ
ijmn Pmesoðay :azÞmnkl Þ only. A similar observation follows for the last term in the
RHS of Eq. (101).Applying 1
jHðby Þy j
RHðby Þy�dH (where bz partition in embedded in byÞ on both sides of (101) yields the expression for the partitioned micro
strain in terms of the macro strain and partitioned eigendeformations
emicðby :bzÞij ðxÞ¼A
mixðby :bzÞijkl emac
kl ðxÞþPmy
ny¼1Q
mixðby :bzÞðnyÞijn d
mesoðnyÞn ðxÞþ
Pny
ay¼1
Pnz
az¼1P
mixðby :bzÞðay :azÞijkl
PI
Ilmicðay :azÞkl ðxÞþ
Pny
ay¼1
Pmz
nz¼1Q
mixðby :bzÞðay :nzÞijn dmicðay :nzÞ
n ðxÞ ;
ð103Þ
where
Amixðby :bzÞijkl ¼ 1
jHðbyÞy j
ZHðby Þy
AmicðbzÞijmn ðyÞAmeso
mnkl ðyÞdH; ð104Þ
Qmixðby :bzÞðnyÞijn ¼ 1
jHðbyÞy j
ZHðby Þy
AmicðbzÞijkl ðyÞQ mesoðnyÞ
kln ðyÞdH; ð105Þ
Pmixðby :bzÞðay :azÞijkl ¼ 1
jHðbyÞy j
ZHðby Þy
AmicðbzÞijmn ðyÞPmesoðay :azÞ
mnkl ðyÞþPmicðbz�azÞ
ijkl ðyÞNðayÞðyÞ
" #dH; ð106Þ
Qmixðby :bzÞðay :nzÞijn ¼ 1
jHðbyÞy j
ZHðby Þy
AmicðbzÞijkl ðyÞQ mesoðay :nzÞ
kln ðyÞþQmicðbz�nzÞ
ijn ðyÞNðayÞðyÞ
" #dH: ð107Þ
Next, we focus on the micro traction field. Substituting Eqs. (100), (68) and (69) into the reduced order micro stress (58) yields
rmicij ðx; y; zÞ ¼ Lmic
ijkl ðy; zÞAmicklmnðy; zÞA
mesomnst ðyÞemac
st ðxÞ þ Lmicijkl ðy; zÞA
micklmnðy; zÞ
Xmy
ny¼1
Q mesoðnyÞmnn ðyÞdmesoðnyÞ
n ðxÞ
þXny
ay¼1
Xnz
az¼1
Lmicijkl ðy; zÞ Amic
klmnðy; zÞPmesoðay :azÞmnst ðyÞ þ Smixðay :azÞ
klst ðy; zÞh iX
I
Ilmicðay :azÞst ðxÞ
þXny
ay¼1
Xmz
nz¼1
Lmicijkl ðy; zÞ Amic
klmnðy; zÞQmesoðay :nzÞmnn ðyÞ þ Q mixðay :nzÞ
kln ðy; zÞh i
dmicðay :nzÞn ðxÞ; ð108Þ
where
Smixðay :azÞijkl ðy; zÞ ¼ SmicðazÞ
ijkl ðy; zÞNðayÞðyÞ; ð109Þ
Q mixðay :nzÞijn ðy; zÞ ¼ QmicðnzÞ
ijn ðy; zÞNðayÞðyÞ: ð110Þ
The corresponding traction along the micro interface is given by
tmicm ðx; y; zÞ ¼ amic
mi tmici ðx; y; zÞ ¼ amic
mi rmicij ðx; y; zÞnmic
j ðy; zÞ; z 2 Sz; ð111Þ
where amicmi is the transformation matrix from the global coordinates system to the local interface.
2026 Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038
Substituting Eq. (108) into (111) and applyingR Rðby :gzÞ
� averaging operator on both sides of (111) yields the partitioned micro traction interms of the macro strain and the partitioned eigendeformations
tmicðby :gzÞm ðxÞ¼B
mixðby :gzÞmkl emac
kl ðxÞþPmy
ny¼1W
mixðby :gzÞðnyÞmn d
mesoðnyÞn ðxÞþ
Pny
ay¼1
Pnz
az¼1V
mixðby :gzÞðay :azÞmkl
PI
Ilmicðay :azÞkl ðxÞþ
Pny
ay¼1
Pmz
nz¼1W
mixðby :gzÞðay :nzÞmn dmicðay :nzÞ
n ðxÞ ;
ð112Þ
where Z Zðby :gzÞ� � 1
jHðbyÞy j
ZHðby Þy
1
jSðgzÞz j
ZSðgzÞ
z
�dSdH; ð113Þ
Bmixðby :gzÞmkl ¼
Z Zðby :gzÞ
amicmi Lmic
ijmnðy; zÞAmicmnstðy; zÞA
mesostkl ðyÞnmic
j ðy; zÞ; ð114Þ
Wmixðby :gzÞðnyÞmn ¼
Z Zðby :gzÞ
amicmi Lmic
ijkl ðy; zÞAmicklmnðy; zÞQ
mesoðnyÞmnn ðyÞnmic
j ðy; zÞ; ð115Þ
Vmixðby :gzÞðay :azÞmkl ¼
Z Zðby :gzÞ
amicmi Lmic
ijmnðy; zÞAmic
mnstðy; zÞPmesoðay :azÞstkl ðyÞ
þSmixðay :azÞmnkl ðy; zÞ
" #nmic
j ðy; zÞ; ð116Þ
Wmixðby :gzÞðay :nzÞmn ¼
Z Zðby :gzÞ
amicmi Lmic
ijkl ðy; zÞAmic
klmnðy; zÞQmesoðay :nzÞmnn ðyÞ
þQ mixðay :nzÞkln ðy; zÞ
" #nmic
j ðy; zÞ: ð117Þ
To this end, we consider the meso traction field. With the reduced order meso stress given by (76), the corresponding traction field along themeso interface is given as
tmesom ðx; yÞ ¼ ameso
mi tmesoi ðx; yÞ ¼ ameso
mi rmesoij ðx; yÞnmeso
j ðyÞ y 2 Sy: ð118Þ
Applying 1
jSðgy Þy j
RSðgy Þy�dS on both sides of (118) yields the partitioned meso traction in terms of the macro strain and the partitioned
eigendeformations
tmesoðgyÞm ðxÞ ¼ B
mesoðgyÞmkl emac
kl ðxÞ þPmy
ny¼1W
mesoðgyÞðnyÞmn d
mesoðnyÞn ðxÞ þ
Pny
ay¼1
Pnz
az¼1V
mesoðgyÞðay :azÞmkl
PI
Ilmicðay :azÞkl ðxÞ þ
Pny
ay¼1
Pmz
nz¼1W
mesoðgyÞðay :nzÞmn dmicðay :nzÞ
n ðxÞ ;
ð119Þ
where
BmesoðgyÞmkl ¼ 1
jSðgyÞy j
ZSðgy Þy
amesomi Lmeso
ijmn ðyÞAmesomnkl ðyÞnmeso
j ðyÞdS; ð120Þ
WmesoðgyÞðnyÞmn ¼ 1
jSðgyÞy j
ZSðgy Þy
amesomi Lmeso
ijmn ðyÞQmesoðnyÞmnn ðyÞnmeso
j ðyÞdS; ð121Þ
VmesoðgyÞðay :azÞmkl ¼ 1
jSðgyÞy j
ZSðgy Þy
amesomi Lmeso
ijmn ðyÞSmesoðay :azÞmnkl ðyÞnmeso
j ðyÞdS; ð122Þ
WmesoðgyÞðay :nzÞmn ¼ 1
jSðgyÞy j
ZSðgy Þy
amesomi Lmeso
ijmn ðyÞTmesoðay :nzÞmnn ðyÞnmeso
j ðyÞdS: ð123Þ
The partitioned variant of the constitutive relations (91)–(93) can be expressed as
Ilmicðay :azÞij ðxÞ ¼ f micðemicðay :azÞ
ij ðxÞ;rmicðay :azÞij ðxÞÞ; ð124Þ
tmicðay :nzÞn ðxÞ ¼ gmicðdmicðay :nzÞ
n ðxÞÞ; ð125Þ
tmesoðnyÞn ðxÞ ¼ gmesoðdmesoðnyÞ
n ðxÞÞ; ð126Þ
where emicðay :azÞij is the partitioned micro strain; tmicðay :nzÞ
n the partitioned micro traction; and tmesoðnyÞn the partitioned meso traction. Eqs. (103),
(112) and (119) along with the partitioned constitutive relations (124)–(126) form a system of nonlinear equations for the unknowns(emicðay :azÞ
ij ðxÞ; dmicðay :nzÞn ðxÞ and d
mesoðnyÞn ðxÞÞ. The number of equations (and unknowns) is given as
6ðny : nzÞ þ 3ðny : mzÞ þ 3my;
where ny : nz ¼Xny
ay¼1
nzjay; ny : mz ¼
Xny
ay¼1
mzjay:
ð127Þ
The partitioned eigendeformations are obtained by solving the system of equations within each macro increment. Once partitioned eigende-formations have been determined, Eq. (86) is used to update the macro stress.
6. Two-scale reduced order homogenization
In the previous sections we derived a three-scale reduced order homogenization formulation, which can be generalized to arbitrarynumber of scales. From the practical point of view, the most interesting case is that of two-scales, which is considered in this section.
Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038 2027
We start with the three-scale boundary value problem defined by Eqs. (1)–(7). For two-scales, the composite material is represented bya locally periodic unit cell on the mesoscale denoted by Hy with the interface denoted by Sy. A single additional position vector y � x=f isintroduced. For any locally periodic function, the spatial derivative reduces to
/fðxÞ � /ðx; yÞ; ð128Þ
/f;iðxÞ ¼ /;xi
ðx; yÞ þ 1f
/;yiðx; yÞ: ð129Þ
The two-scale asymptotic expansion of the displacement field is given as
uiðx; yÞ ¼ u0i ðxÞ þ fu1
i ðx; yÞ þ � � � ð130Þ
and the asymptotic expansion of the strain field is
eijðx; yÞ ¼ e0ijðx; yÞ þ fe1
ijðx; yÞ þ � � � ð131Þ
with the leading order strain
e0ijðx; yÞ ¼ u0
ði;xjÞðxÞ þ u1ði;yjÞðx; yÞ: ð132Þ
The macro strain is defined as an average strain over Hy
emacij ðxÞ �
1jHyj
ZHy
e0ijðx; yÞdHy ¼ u0
ði;xjÞðxÞ: ð133Þ
Thus the meso strain can be expressed as
emesoij ðx; yÞ � e0
ijðx; yÞ ¼ u0ði;xjÞðxÞ þ u1
ði;yjÞðx; yÞ ¼ emacij ðxÞ þ u1
ði;yjÞðx; yÞ: ð134Þ
The asymptotic expansion of the stress field is given as
rijðx; yÞ ¼ r0ijðx; yÞ þ fr1
ijðx; yÞ þ � � � ð135Þ
where
r0ijðx; yÞ ¼ LijklðyÞ e0
klðx; yÞ �X
I
Ilklðx; yÞ" #
: ð136Þ
The meso- and macro-stresses are defined as
rmesoij ðx; yÞ � r0
ijðx; yÞ; ð137Þ
rmacij ðxÞ �
1jHyj
ZHy
rmesoij ðx; yÞdH: ð138Þ
The resulting meso and macro equilibrium equations are identical to those obtained in the three-scale case
Oðf�1Þ : rmesoij;yjðx; yÞ ¼ 0 ; ð139Þ
Oðf0Þ : rmacij;xjðxÞ þ �bi ¼ 0 ; ð140Þ
where
�bi ¼1jHyj
ZHy
bidH: ð141Þ
Due to the homogeneity of the meso-phases the following can be deduced:
1. All the terms related to the micro eigenseparation dmicn vanish since they no longer exist; we denote dn � dmeso
n to simplify the notation.2. The micro elastic polarization function Gmic
ijkl , the micro eigenstrain polarization function gmic lijkl and the corresponding partitioned Pmic
ijkl areall zero tensors.
3. The superscripts ‘‘mic”, ‘‘: az” and ‘‘: bz” can be dropped since there are no partitions at the micro scale.
The resulting reduced order residual-free meso stress can be directly deduced from Eq. (76)
rmesoij ¼ Lmeso
ijmn ðyÞAmeso
mnkl ðyÞemackl ðxÞ þ
Pmy
ny¼1Q mesoðnyÞ
mnn ðyÞdðnyÞn ðxÞ
þPny
ay¼1SmesoðayÞ
mnkl ðyÞP
I
IlðayÞkl ðxÞ
266664
377775 ; ð142Þ
where
SmesoðayÞijkl ðyÞ ¼ PmesoðayÞ
ijkl ðyÞ � ImesoðayÞijmn ðyÞ ð143Þ
Table 2Summary of influence function problems for the two-scale analysis.
Governing equation Solution tensor Calculated tensor(s)
Meso elastic (43) Gmesoijkl Ameso
ijkl (51), Lmacijkl (87)
Meso eigenstrain (145) PmesoðayÞijkl SmesoðayÞ
ijkl (143), SmacðayÞijkl (147)
Meso eigenseparation (85) QmesoðnyÞijn QmacðnyÞ
ijn (88)
2028 Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038
and
Table 3Coeffici
Macro
Lmac ¼ E
Smacð1Þ ¼
�E
Qmacð1Þ ¼
PmesoðayÞijkl ðyÞ ¼
ZHðay Þy
gmeso lijmn ðy; yÞdH: ð144Þ
The elasticity problem at the mesoscale from which the reduced order eigenstrain influence are determined directly follows from Eq. (83)
fLmesoijkl ðyÞ½P
mesoðayÞklmn ðyÞ � ImesoðayÞ
klst ðyÞ�g;yj¼ 0 y 2 Hy: ð145Þ
The reduced order meso stress follows from Eq. (86)
rmacij ¼ Lmac
ijkl emackl ðxÞ þ
Pmy
ny¼1QmacðnyÞ
ijn dðnyÞn ðxÞ þ
Pny
ay¼1SmacðayÞ
ijkl
PI
IlðayÞkl ðxÞ ; ð146Þ
where
SmacðayÞijkl ¼ 1
jHyj
ZHy
Lmesoijmn ðyÞS
mesoðayÞmnkl ðyÞdH: ð147Þ
Table 2 summarizes the coefficient tensors, which follow from Table 1.
Fig. 4. A one-dimensional model problem.
ent tensors for the 1D model problem.
Phase Interface
2E1 E2
1þE2Amesoð1Þ ¼ 2E2
E1þE2; Ameso
ð2Þ ¼ 2E1E1þE2
Bmesoð1Þ ¼
2E1 E2E1þE2
E1 E2
1þE2; Smac
ð2Þ ¼�E1 E2E1þE2
Pmesoð1Þð1Þ ¼
E1E1þE2
; Pmesoð1Þð2Þ ¼
�E2E1þE2
; Pmesoð2Þð1Þ ¼
�E1E1þE2
; Pmesoð2Þð2Þ ¼
E2E1þE2
Vmesoð1Þð1Þ ¼
�E1 E2E1þE2
; Vmesoð1Þð2Þ ¼
�E1 E2E1þE2
�2E1E2E1þE2
Qmesoð1Þð1Þ ¼
�2E2E1þE2
; Qmesoð2Þð1Þ ¼
�2E1E1þE2
Wmesoð1Þð1Þ ¼
�2E1 E2E1þE2
Fig. 5. The unit cell for 1D model problem.
Fig. 6. The fibrous unit cell for convergence study.
Fig. 7. The stress–strain curves for longitudinal loading.
Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038 2029
The system of equations for calculating the meso eigendeformations is obtained from Eqs. (103) and (119). The partitioned strain field isgiven as
eðbyÞij ðxÞ ¼ A
mesoðbyÞijkl emac
kl ðxÞ þPmy
ny¼1Q
mesoðbyÞðnyÞijn d
ðnyÞn ðxÞ þ
Pny
ay¼1P
mesoðbyÞðayÞijkl
PI
IlðayÞkl ðxÞ ; ð148Þ
where
AmesoðbyÞijkl ¼ 1
jHðbyÞy j
ZHðby Þy
Amesoijkl ðyÞdH; ð149Þ
QmesoðbyÞðnyÞijn ¼ 1
jHðbyÞy j
ZHðby Þy
Q mesoðnyÞijn ðyÞdH; ð150Þ
PmesoðbyÞðayÞijkl ¼ 1
jHðbyÞy j
ZHðby Þy
PmesoðayÞijkl ðyÞdH: ð151Þ
The partitioned traction field becomes
tmesoðgyÞm ðxÞ ¼ B
mesoðgyÞmkl emac
kl ðxÞ þPmy
ny¼1W
mesoðgyÞðnyÞmn d
ðnyÞn ðxÞ þ
Pny
ay¼1V
mesoðgyÞðayÞmkl
PI
IlðayÞkl ðxÞ ; ð152Þ
Fig. 8. The stress–strain curves for transverse loading.
Fig. 9. Braid architectures considered for validation.
Table 4The virgin properties of micro phases (manufacture’s values).
E (GPa) m
Matrix 3.170 0.35Fiber 234.0 (231.0 for bias tow) � (assume 0.1 for calibration)
Table 5Initial properties of the tow.
E22 (GPa) E11 (GPa) m23 m12 G23a (GPa) G12 (GPa)
43.89 210.9 0.40 0.12 15.71 18.45
a Where G23 ¼ E22=ð2ð1þ m23ÞÞ.
Table 6Elastic calibration of tow properties.
Lower bound Upper bound Calibrated value
E22 (GPa) 10.0 100.0 31.62E11 (GPa) 100.0 1000 348.8
2030 Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038
Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038 2031
where
Table 7Identifie
EA (GPaET (GPa
Table 8Multi-s
Step #
123
BmesoðgyÞmkl ¼ 1
jSðgyÞy j
ZSðgy Þy
amesomi Lmeso
ijmn ðyÞAmesomnkl ðyÞnmeso
j ðyÞdS; ð153Þ
WmesoðgyÞðnyÞmn ¼ 1
jSðgyÞy j
ZSðgy Þy
amesomi Lmeso
ijmn ðyÞQmesoðnyÞmnn ðyÞnmeso
j ðyÞdS; ð154Þ
VmesoðgyÞðayÞmkl ¼ 1
jSðgyÞy j
ZSðgy Þy
amesomi Lmeso
ijmn ðyÞSmesoðayÞmnkl ðyÞnmeso
j ðyÞdS: ð155Þ
d macro properties.
Experiment Simulation
) 60.3 ± 2.95 60.42) 8.7 ± 0.24 8.76
Fig. 11. The overall stress–strain curves in tow tension and compression.
Fig. 10. Partitions for the braided unit cell (45�).
tep calibration of inelastic parameters.
Active parameter Used tests of composite Overall ultimate strength of composite (MPa)
Experiment Simulation
Smatrix Transverse tension 65.2 62.7Stow Longitudinal tension 654.3 651.7Cmatrix and Sb
tow Longitudinal compression 375.8 380.1
2032 Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038
The constitutive relations for the partitioned eigendeformations are deduced from Eqs. (124) and (126)
IlðayÞij ðxÞ ¼ f ðeðayÞ
ij ðxÞ;rðayÞij ðxÞÞ; ð156Þ
tðnyÞn ðxÞ ¼ gðdðnyÞ
n ðxÞÞ: ð157Þ
Eqs. (148) and (152) along with the partitioned constitutive relations (156) and (157) form a system of nonlinear equations for the unknowns(eðayÞ
ij ðxÞ and dðnyÞn ðxÞÞ. The number of equations (and unknowns) is 6ny þ 3my, which follows from Eq. (127).
Partitioned eigendeformations are obtained by solving a system of equations within each macro increment. Once partitioned eigende-formations have been determined, Eq. (146) is used to update the macro stress.
7. Verification
In this section, a one-dimensional model is used for verification of the reduced order model influence functions. Convergence of the re-duced order model to the direct homogenization is studied next.
We consider a one-dimensional heterogeneous bar made of a periodic arrangement of two different materials (E1 on the left and E2 onthe right) as shown in Fig. 4.
Fig. 12. Circular tube model.
Fig. 13. Comparison of the multiscale simulation and experimental results for circular tube made of 45� braid architecture.
Fig. 14. Comparison of the multiscale simulation and experimental results for circular tube made of 30� braid architecture.
Fig. 15. Comparison of the multiscale simulation and experimental results for circular tube made of 60� braid architecture.
Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038 2033
For the 1D model problem, we can obtain an analytical solution of coefficient tensors, which are given in Table 3.We select several pairs of Young’s Modulus values for the two phases (Fig. 5) to verify the values of coefficient tensors. The simulation
results coincide with the analytical solutions given in Table 3 for all pairs of Young’s Modulus selected.Next, we study the convergence of the reduced order model to the direct homogenization model. The reduced order model should con-
verge to direct homogenization model when partition number approaches the number of elements in the unit cell. For this study, we con-sider a fibrous unit cell with 226 elements as shown Fig. 6. Only the matrix phase (160 elements) is assumed to be damageable. Weincrease the partition number for matrix phase from 1, 4, 8, and up to 160 and compare the overall stress–strain curves with the directhomogenization results. The results of two loading cases, longitudinal loading and transverse loading, are shown in Figs. 7 and 8, respec-tively. It can bee seen that for both cases, the reduced order model converges to the direct homogenization model. However, the compu-tational cost of one matrix partition is three orders of magnitude smaller than of the direct cost homogenization. For more details see [31].
8. Validation
In this section the reduced order formulation is validated on the tube crush simulation of braided composite.We consider a triaxially braided composite unit cell model with three different angles (30�, 45� and 60�) as shown in Fig. 9.In each unit cell model we identify bias tows with plus/minus (clockwise/counterclockwise) angles with respect to the axial tow as two
different inclusion phases. Hence there are four phases (matrix, axial tow, bias tow 1 and bias tow 2) and three interfaces associated witheach inclusion phase.
Fig. 16. Size effect studies for three different mesh sizes.
Fig. 17. Square tube model.
2034 Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038
Since each tow in the unit cell consists of thousands of filaments of carbon fiber (axial tow: 80k1 Fortafil 511; bias tow: 12k Grafil 34-700)and epoxy matrix (Ashland Hetron 922), we have a three-scale representation of the composite: fibrous micro unit cell model, braided mesounit cell model (constructed in the previous step) and macro tube model.
To identify the elastic properties of the braided unit cell, we assume that the matrix properties are known from manufacture’s values,and calibrate the tow properties based on a series of coupon tests. The material symmetry of tow is assumed to be transversely isotropic(x1 ¼ xA, 5 independent values) and the initial values of tow for the calibration process (Table 5) are determined using Mori–Tanaka method[33] for the micro fibrous unit cell (volume fraction of fiber 87.7%). The virgin properties of micro phases are given in Table 4.
During calibration process, the two Young’s Moduli of a tow were selected as active parameters. The lower and upper bounds and result-ing calibrated values are summarized in Table 6. The identified macro properties of the braided composite are compared with experimentaltest data in Table 7.
We use one partition per phase strategy and assume no interface. This results in four phase partitions (one matrix partition, one axialtow partition and two bias tow partitions) as shown in Fig. 10. There are 24 (4 partitions time 6 modes) eigenstrain components that needto be updated within each macro increment (reduced order unit cell problem).
1 An 80k tow nominally contains 80,000 individual fibers.
Fig. 18. Comparison of the multiscale simulation and experimental results for square tube made of 45� braid architecture.
Fig. 19. Comparison of the multiscale simulation and experimental results for square tube made of 30� braid architecture.
Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038 2035
The constitutive behavior of phases at the mesoscale is modeled using continuum damage mechanics (see Appendix for details). Modelparameters, the ultimate strength of matrix, Smatrix, the ultimate strength of tow, Stow, the compression factor of matrix, Cmatrix, and the buck-ling strength of tow Sb
tow (see discussion below) are calibrated using inverse methods [34]. The values of the identified parameters and theircomparison to the experimental values are summarized in Table 8.
The buckling strength Sb is introduced to account for tow buckling in the following way
if rtow 6 Sbtow < 0;
wtow ¼ wmatrix;ð158Þ
i.e., when Sbtow is reached, the damage state of tow is associated with the damage state of matrix phase. As an example, in Fig. 11 we give the
overall axial stress–strain curves of a fibrous unit cell subjected to axial tension and compression with displacement control. It can be seenthat under compression loading and with a relative small value of Sb, the damage state of fiber is associate with the damage state of matrixand the entire unit cell loses its loading capacity.
Note, that elastic and inelastic parameters are calibrated based on 45� coupon tests. The 30� and 60� unit cells models use the same setof parameters identified in 45� coupon tests.
Once the model parameters have calibrated, we proceed with crush simulations of circular and square tubes on three different materialarchitectures and compare the simulation results to the experimental data (all test data are from [35]). For all tube crush simulations weconsider a quasi-static loading (load rate = 0.5 in./min), two layers of braided composite.
Fig. 20. Comparison of the multiscale simulation and experimental results for square tube made of 60� braid architecture.
2036 Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038
First we conduct crush simulations of circular tube as shown in Fig. 12. The inner diameter of the tube is 2.35 in. An initiator plug with 5/16 in. fillet radius is considered.
Fig. 13 compares the multiscale simulations to the experimental results for the 45 braid architecture shown in Fig. 9. Excellent agree-ment with the experiment can be observed. Fig. 14 compares the multiscale simulations to the experimental results for the 30 braid archi-tecture shown in Fig. 9. This time the agreement with experiment is not as good. Possibly, this can be attributed to the fact that we have notaccounted for interface failure. Fig. 15 compares the multiscale simulations to the experimental results for the 60 braid architecture shownin Fig. 9. Again, an excellent agreement with the experiment can be observed.
For the circular tube, we also study the size effect – that is the influence of mesh size on simulation results. Fig. 16 summarizes thefindings of these studies. Interestingly, the model shows very little if any influence to the mesh size. For coarser meshes, however, the oscil-lations are higher, which is due to the fact that when the macro element is eroded the load is reduced. The larger element is eroded, thelarger jump is observed.
Next we conduct crush simulations of square tube as shown in Fig. 17. The inner dimensions of the tube are 2 in. � 2 in. and inner cornerradius of 0.33 in. An initiator plug with 1/4 in. fillet radius is considered.
Figs. 18–20 compare the multiscale simulation to the experimental results for the 45, 30 and 60 braid architectures, respectively. Theagreement with experiments is reasonable at best, suggesting the need for considering interface failure. Note that implementation of inter-face failure will affect the calibrated properties of micro-constituents. This is because the failure properties of micro-constituents were cal-ibrated to fit the coupon data.
Acknowledgements
The financial supports of National Science Foundation under grants CMS-0310596, 0303902, 0408359, Rolls-Royce Contract 0518502,Automotive Composite Consortium Contract 606-03-063L, and AFRL/MNAC MNK-BAA-04-0001 contract are gratefully acknowledged.
Appendix
In the present manuscript, continuum damage mechanics with isotropic damage law is used to model constitutive behavior of micro-constituents. By this approach, the constitutive relation is given by
rij ¼ ð1�wphÞLijklekl; ð159Þ
where w 2 ½0;1� is a damage state variable. Thus the partitioned eigenstrain is defined as
lðayÞij ¼ wðayÞ
ph eðayÞij : ð160Þ
The damage state variable wðayÞph is taken to be a piecewise-continuous function of damage equivalent strain jðayÞ
ph . The evolution of phase dam-age may be expressed as
wðayÞph ¼
0; jðayÞph 6
1jðayÞph ;
UðjðayÞph Þ; 1jðayÞ
ph < jðayÞph 6
2jðayÞph ;
1; jðayÞph > 2jðayÞ
ph ;
8>>><>>>: ð161Þ
where 1jðayÞph and 2jðayÞ
ph are model parameters corresponding to the initial and fully damaged state, respectively.
Z. Yuan, J. Fish / Comput. Methods Appl. Mech. Engrg. 198 (2009) 2016–2038 2037
The damage equivalent strain jðayÞph is assumed to be a function of the principal strain
jðayÞph ðtÞ ¼max
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiX3
I¼1
heðayÞI ðsÞi
2
vuut ; s < t
8<:
9=;; ð162Þ
where
hxi ¼x; x P 0;Cx; x < 0
�ð163Þ
and C is the compression factor (one of inelastic material parameters).1jðayÞ
ph can be expressed in terms of material strength S (another inelastic material parameter) and stiffness E
1jðayÞph ¼
SE: ð164Þ
Based on the selection of the damage evolution function, 2jðayÞph can be expressed in terms of physical-based material parameters (E, S and G –
the total strain energy). For various evolution functions UðjðayÞph Þ see [34].
Similarly, eigenseparation are modeled using damage mechanics based cohesive law
tðnyÞn ¼ ð1�wðnyÞ
int ÞKðnyÞd
ðnyÞn ; ð165Þ
where KðnyÞ is the interface stiffness. In the normal direction, wðnyÞint is considered only when d
ðnyÞn > 0.
The interface damage state variable wðnyÞint is assumed to be a function of damage equivalent displacement jðnyÞ
int defined as
jðnyÞint ðtÞ ¼max
ffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffiffihdðnyÞ
n ðsÞi2þ þ ðdðnyÞt1 ðsÞÞ
2 þ ðdðnyÞt2 ðsÞÞ
2q
; s < t� �
; ð166Þ
where
hxiþ ¼x; x P 0;0; x < 0:
�ð167Þ
The evolution of interface damage can be expressed as
wðnyÞint ¼
0; jðnyÞint 6
1jðnyÞint ;
UðjðnyÞint Þ; 1jðnyÞ
int < jðnyÞint 6
2jðnyÞint ;
1; jðnyÞint > 2jðnyÞ
int :
8>><>>: ð168Þ
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