# Effects of Morphology and Topology on the Effective Stiffness of Chiral Cellular Materials in the Transverse Plane

Authors: Alp Karakoç; Ertuǧrul Taciroǧlu
Journal: Advances in Materials Science and Engineering
 (2016)

---

## Abstract

The present study investigates the influence of topology and morphology on the effective stiffness of chiral cellular materials in the transverse plane by means of a homogenization method. For this purpose, finite element models of representative volume elements for regular hexagonal and hexagonal-chiral configurations are used and simulations are conducted to quantify how cell topology—that is, chirality inside the cell—and cell wall slenderness affect the effective stiffness. Closed form solutions for regular hexagonal square and triangular RVEs provided in the literature are then taken as a basis for model validation. The results indicate that there are drastic differences between regular hexagonal and hexagonal-chiral configurations, which can be explained in terms of deformation mechanism transformations between bending and stretching. The investigations also reveal the positive impact of cell wall slenderness on stiffness due to volumetric increase in the cell wall material resisting the deformation.


---

## Body

## 1. Introduction

In recent years, with growing interest in energy efficient, robust, and lightweight material systems, cellular materials have found their way into numerous engineering applications. They are nowadays used as high-stiffness sandwich panels, energy absorbers, thermal insulators, and vibration dampers. Due to their low densities and high potential as being tailored materials in terms of effective stiffness and strength properties, there are ongoing research and development activities on these materials [1–3].Dependence of these effective properties on cell wall geometrical, topological, and mechanical properties has been investigated in the framework of computational homogenization methods [4, 5]. The framework is used to solve the associated boundary value problem with proper boundary conditions on representative volume elements (RVEs) that capture the prominent features of the material [6]. In the case of cellular materials, the term RVE refers to an individual cell or a group of cells, as depicted in Figure 1, that are assumed to represent the effective material properties at the mesoscale.Figure 1
Hexagonal and hexagonal-chiral structures and corresponding representative volume elements.As a contribution to the current state of the art on cellular material characterization in the framework of computational homogenization, the current study aims at (i) understanding the effect of cell topology on the effective stiffness properties of cellular materials in the transverse plane by using regular hexagonal and hexagonal-chiral RVEs shown in Figure1, (ii) understanding the effect of cell wall slenderness—that is, cell wall thickness-to-height ratio—on these effective properties, and (iii) comparing the extracted stiffness properties with analytical results given in the literature.


## 2. Materials and Methods

Computational homogenization has been a useful tool for determining the effective properties of materials that can be described through their microscopic properties. The basic idea behind this methodology is to evaluate the effective properties by solving the boundary value problem with appropriate boundary conditions defined on a representative volume element (RVE), which contains all necessary information [7, 8]. Some of the key advantages include being able to introduce all of the necessary geometrical and constitutive information at appropriate scales of the material behavior and being able to use requisitely detailed yet computationally effective idealization—such as beam and plate models—at the scale of the material cells [9, 10].In the literature, numerous analytical and computational approaches have been offered to the homogenization problems involving cellular materials (see, e.g., [11–13]). Due to advances in theory and hardware, computational homogenization methods have become more frequently used for material characterization. In the present study, a computational homogenization method is thus used to investigate the effective stiffness properties of cellular materials, which is explained in detail in the following section.


### 2.1. A First-Order Strain-Driven Computational Homogenization Method

In the homogenization approach adopted here, the macroscopic straine
i
j
M for i
,
j
∈
X
,
Y is assumed to be uniform over the material and imposed at the RVE boundary ∂
ω as illustrated in Figure 2. Therefore, a first-order microscopic displacement field decomposition for the RVE can be given as(1)
u
→
m
=
r
→
·
e
M
+
u
_
→
,for which the first term on the right-hand side represents the macroscopic displacement contribution and the second one represents the displacement fluctuation field u
_
→ due to heterogeneities within the RVE [4]. Here, r
→ represents the position vector with respect to any described origin.Figure 2
Strain-driven homogenization scheme with imposed macroscopic straine
i
j
M and computed stress s
i
j
M for i
,
j
∈
X
,
Y. Here, Ω and ∂
Ω represent the volume and boundary of aggregate, and ω and ∂
ω represent the volume and boundary of RVE.Since the overall body is assumed to be composed of periodic arrays of repeating RVEs, continuity conditions for the displacements and tractions must be satisfied at the boundaries of each neighbouring cell. The first condition can be satisfied by taking the relative positions of the node sets, for example, nodes at the opposite edges on∂
ω, for which displacement fluctuations have the same value due to the periodicity condition [14]. Hence, (1) can be expanded as(2)
u
→
1
m
-
u
→
2
m
=
r
→
1
-
r
→
2
·
e
M
,which forms the basis of the displacement boundary condition for periodic arrays. The traction boundary condition is satisfied with antiperiodicity of traction field in case of existence of traction on the boundaries [6]. However, the current study focuses on the displacement boundary conditions; therefore, only (2) is studied for the periodic boundary conditions.In order to establish a consistent relationship between different scales, the Hill-Mandel principle can be used such that [15](3)
s
M
:
e
M
=
1
ω
∫
ω
s
m
:
e
m
d
ω
,for which the superscript “m” represents the microscopic or RVE scale. The symbol “:” denotes an inner product, and for second-order tensors it is defined as(4)
a
:
b
=
a
i
j
b
i
j
.By using Gauss’s theorem, (3) can be rewritten at the RVE boundary ∂
ω as(5)
s
M
:
e
M
=
1
ω
∫
∂
ω
t
→
m
·
u
→
m
d
∂
ω
,where t
→
m is the microscopic traction vector at ∂
ω. By plugging (1) into (5),(6)
s
M
:
e
M
=
1
ω
∫
∂
ω
t
→
m
·
r
→
·
e
M
d
∂
ω
+
1
ω
∫
∂
ω
t
→
m
·
u
_
→
d
∂
ω
,which yields to(7)
s
M
:
e
M
=
1
ω
∫
∂
ω
t
→
m
⊗
r
→
d
∂
ω
:
e
M
+
1
ω
∫
∂
ω
t
→
m
·
u
_
→
d
∂
ω
.Here, the symbol ⊗ denotes a dyadic product. The second integrand at the right-hand side vanishes in case of periodic boundary conditions, as elaborated in (2). Hence, the macroscopic stress s
i
j
M can be expressed as the volume average of the microscopic stress s
i
j
m such that(8)
s
M
=
1
ω
∫
∂
ω
t
→
m
⊗
r
→
d
∂
ω
=
1
ω
∫
ω
s
m
d
ω
,where ω is the total volume of the RVE.Thereafter, the effective stiffness can be determined by means of the relationship between the macroscopic straine
i
j
M and stress s
i
j
M under the linear elasticity assumption. This relationship can be constructed in terms of macroscopic compliance so that [16](9)
e
M
=
C
M
:
s
M
.Then, the Voigt notation for C
M can be constructed as(10)
C
M
=
e
X
X
M
,
1
e
X
X
M
,
2
e
X
X
M
,
3
e
Y
Y
M
,
1
e
Y
Y
M
,
2
e
Y
Y
M
,
3
2
e
X
Y
M
,
1
2
e
X
Y
M
,
2
2
e
X
Y
M
,
3
s
X
X
M
,
1
s
X
X
M
,
2
s
X
X
M
,
3
s
Y
Y
M
,
1
s
Y
Y
M
,
2
s
Y
Y
M
,
3
s
X
Y
M
,
1
s
X
Y
M
,
2
s
X
Y
M
,
3
-
1
,for which C
M is taken to be symmetric matrix. Superscripts 1, 2, and 3 represent three different loading conditions fulfilling the minimum requirement to obtain the compliance matrix. Under the assumption of orthotropic material properties,(11)
C
M
=
1
E
X
-
v
Y
X
E
Y
0
-
v
X
Y
E
X
1
E
Y
0
0
0
1
G
X
Y
,for which E
X and E
Y are the effective Young’s moduli, G
X
Y are the shear modulus, and v
X
Y and v
Y
X are Poisson’s ratios with reciprocal relation v
X
Y
/
E
X
=
v
Y
X
/
E
Y [17].


### 2.2. Implementation of Computational Homogenization

In this study, regular hexagonal and hexagonal-chiral RVEs are investigated. Therefore, the aforementioned equation sets are applied on matching node sets that form the periodicity conditions. The mapping is illustrated on a regular hexagonal RVE geometry as seen in Figure3(a), whereas the geometrical parameters of regular hexagonal and hexagonal-chiral RVEs are depicted in Figure 3(b).Figure 3
Schematics of the investigated geometrical properties and matching nodes for periodic boundary conditions: (a) nodal mapping for periodic boundary conditions and (b) cell geometric parameters, cell wall thicknesst, height h, and hub diameter D.
(a)
(b)


## 2.1. A First-Order Strain-Driven Computational Homogenization Method

In the homogenization approach adopted here, the macroscopic straine
i
j
M for i
,
j
∈
X
,
Y is assumed to be uniform over the material and imposed at the RVE boundary ∂
ω as illustrated in Figure 2. Therefore, a first-order microscopic displacement field decomposition for the RVE can be given as(1)
u
→
m
=
r
→
·
e
M
+
u
_
→
,for which the first term on the right-hand side represents the macroscopic displacement contribution and the second one represents the displacement fluctuation field u
_
→ due to heterogeneities within the RVE [4]. Here, r
→ represents the position vector with respect to any described origin.Figure 2
Strain-driven homogenization scheme with imposed macroscopic straine
i
j
M and computed stress s
i
j
M for i
,
j
∈
X
,
Y. Here, Ω and ∂
Ω represent the volume and boundary of aggregate, and ω and ∂
ω represent the volume and boundary of RVE.Since the overall body is assumed to be composed of periodic arrays of repeating RVEs, continuity conditions for the displacements and tractions must be satisfied at the boundaries of each neighbouring cell. The first condition can be satisfied by taking the relative positions of the node sets, for example, nodes at the opposite edges on∂
ω, for which displacement fluctuations have the same value due to the periodicity condition [14]. Hence, (1) can be expanded as(2)
u
→
1
m
-
u
→
2
m
=
r
→
1
-
r
→
2
·
e
M
,which forms the basis of the displacement boundary condition for periodic arrays. The traction boundary condition is satisfied with antiperiodicity of traction field in case of existence of traction on the boundaries [6]. However, the current study focuses on the displacement boundary conditions; therefore, only (2) is studied for the periodic boundary conditions.In order to establish a consistent relationship between different scales, the Hill-Mandel principle can be used such that [15](3)
s
M
:
e
M
=
1
ω
∫
ω
s
m
:
e
m
d
ω
,for which the superscript “m” represents the microscopic or RVE scale. The symbol “:” denotes an inner product, and for second-order tensors it is defined as(4)
a
:
b
=
a
i
j
b
i
j
.By using Gauss’s theorem, (3) can be rewritten at the RVE boundary ∂
ω as(5)
s
M
:
e
M
=
1
ω
∫
∂
ω
t
→
m
·
u
→
m
d
∂
ω
,where t
→
m is the microscopic traction vector at ∂
ω. By plugging (1) into (5),(6)
s
M
:
e
M
=
1
ω
∫
∂
ω
t
→
m
·
r
→
·
e
M
d
∂
ω
+
1
ω
∫
∂
ω
t
→
m
·
u
_
→
d
∂
ω
,which yields to(7)
s
M
:
e
M
=
1
ω
∫
∂
ω
t
→
m
⊗
r
→
d
∂
ω
:
e
M
+
1
ω
∫
∂
ω
t
→
m
·
u
_
→
d
∂
ω
.Here, the symbol ⊗ denotes a dyadic product. The second integrand at the right-hand side vanishes in case of periodic boundary conditions, as elaborated in (2). Hence, the macroscopic stress s
i
j
M can be expressed as the volume average of the microscopic stress s
i
j
m such that(8)
s
M
=
1
ω
∫
∂
ω
t
→
m
⊗
r
→
d
∂
ω
=
1
ω
∫
ω
s
m
d
ω
,where ω is the total volume of the RVE.Thereafter, the effective stiffness can be determined by means of the relationship between the macroscopic straine
i
j
M and stress s
i
j
M under the linear elasticity assumption. This relationship can be constructed in terms of macroscopic compliance so that [16](9)
e
M
=
C
M
:
s
M
.Then, the Voigt notation for C
M can be constructed as(10)
C
M
=
e
X
X
M
,
1
e
X
X
M
,
2
e
X
X
M
,
3
e
Y
Y
M
,
1
e
Y
Y
M
,
2
e
Y
Y
M
,
3
2
e
X
Y
M
,
1
2
e
X
Y
M
,
2
2
e
X
Y
M
,
3
s
X
X
M
,
1
s
X
X
M
,
2
s
X
X
M
,
3
s
Y
Y
M
,
1
s
Y
Y
M
,
2
s
Y
Y
M
,
3
s
X
Y
M
,
1
s
X
Y
M
,
2
s
X
Y
M
,
3
-
1
,for which C
M is taken to be symmetric matrix. Superscripts 1, 2, and 3 represent three different loading conditions fulfilling the minimum requirement to obtain the compliance matrix. Under the assumption of orthotropic material properties,(11)
C
M
=
1
E
X
-
v
Y
X
E
Y
0
-
v
X
Y
E
X
1
E
Y
0
0
0
1
G
X
Y
,for which E
X and E
Y are the effective Young’s moduli, G
X
Y are the shear modulus, and v
X
Y and v
Y
X are Poisson’s ratios with reciprocal relation v
X
Y
/
E
X
=
v
Y
X
/
E
Y [17].


## 2.2. Implementation of Computational Homogenization

In this study, regular hexagonal and hexagonal-chiral RVEs are investigated. Therefore, the aforementioned equation sets are applied on matching node sets that form the periodicity conditions. The mapping is illustrated on a regular hexagonal RVE geometry as seen in Figure3(a), whereas the geometrical parameters of regular hexagonal and hexagonal-chiral RVEs are depicted in Figure 3(b).Figure 3
Schematics of the investigated geometrical properties and matching nodes for periodic boundary conditions: (a) nodal mapping for periodic boundary conditions and (b) cell geometric parameters, cell wall thicknesst, height h, and hub diameter D.
(a)
(b)


## 3. Results and Discussion

### 3.1. Design of Experiments

In the present study, cell walls are taken to be transversely isotropic under the assumption of uniform distribution of cell wall material in the plane of interest. Mechanical parameters of the cell walls are selected asE
s
=
1000 Pa and v
s
=
0.4, which refer to typical cell wall Young’s modulus and Poisson’s ratio value, respectively. In relation to (9) and (10), three different in-plane loading conditions—that is, tensile load along the X- and Y-directions and the X
Y-shear load as listed in Table 1 and illustrated in Figure 4—are used to compute the effective stiffness properties and understand the effect of cell wall slenderness t
_
/
h, for which t
_
=
2
t, t is cell wall thickness, and h refers to cell wall height (as depicted in Figure 3), on the computed properties. The reason for taking the cell wall slenderness as t
_
=
2
t is to be able to compare the numerical results with the closed form solutions provided for double cell walls in the literature [5, 9]. The slenderness is taken to be in the range so that t
_
/
h
∈
0.02,0.20 with increment of Δ
t
_
/
h
=
0.02 whereas hub diameter is taken as D
=
h
/
2 for the chiral configuration illustrated in Figure 3(b).Table 1
Loading conditions.
Case
Imposed strains
e
X
X
M
e
Y
Y
M
2
e
X
Y
M
1
0.01
0
0
2
0
0.01
0
3
0
0
0.01Figure 4
Schematic representation of loading conditions based on the listed cases in Table1 (presented deformations are scaled larger than the actual ones for readability): (a) undeformed hexagonal RVE, (b) deformation under e
X
X
M, (c) deformation under e
Y
Y
M, (d) deformation under e
X
Y
M, (e) undeformed hexagonal-chiral RVE, (f) deformation under e
X
X
M, (g) deformation under e
Y
Y
M, and (h) deformation under e
X
Y
M.
(a)
(b)
(c)
(d)
(e)
(f)
(g)
(h)


### 3.2. Results

For understanding how cell wall slenderness (namely, cell wall thickness-to-height ratio) and cell topology (namely, chirality introduced inside the cell) affect the effective stiffness properties, simulation experiments are carried out on the RVEs. For this purpose, Abaqus/CAE is used, in which the periodic boundary conditions can be implemented. Thereafter, the solution domain is discretized into sets of finite elements—here, 6-noded quadratic triangular CPS6 provided in Abaqus/CAE. The results are compared with closed form solutions provided in Table2.Table 2
Effective Young’s moduli, shear modulus, and Poisson’s ratios as functions of cell wall slendernesst
_
/
h, where t
_
=
2
t for regular hexagonal, square, and equilateral triangular unit cells.
Prop.
Survey I_HEX [5]
Survey II_HEX [9]
Survey III_SQU [5]
Survey IV_TRI [5]
E
X
E
s
4
3
t
_
/
h
3
1
+
3
t
_
/
h
2
4
3
t
_
/
h
3
1
+
5.4
+
1.5
v
s
t
_
/
h
2
t
_
h
2
3
t
_
/
h
+
t
_
/
h
3
3
+
t
_
/
h
2
E
Y
E
s
4
3
t
_
/
h
3
1
+
3
t
_
/
h
2
4
3
t
_
/
h
3
1
+
5.4
+
1.5
v
s
t
_
/
h
2
t
_
h
2
3
t
_
/
h
+
t
_
/
h
3
3
+
t
_
/
h
2
G
X
Y
E
s
1
3
t
_
/
h
3
1
+
t
_
/
h
2
1
3
t
_
/
h
3
1
+
3.3
+
1.75
v
s
t
_
/
h
2
1
2
t
_
h
3
3
4
t
_
h
+
t
_
h
3
v
X
Y
1
-
t
_
/
h
2
1
+
3
t
_
/
h
2
1
+
1.4
+
1.5
v
s
t
_
/
h
2
1
+
5.4
+
1.5
v
s
t
_
/
h
2
0
1
-
t
_
/
h
2
3
+
t
_
/
h
2
v
Y
X
1
-
t
_
/
h
2
1
+
3
t
_
/
h
2
1
+
1.4
+
1.5
v
s
t
_
/
h
2
1
+
5.4
+
1.5
v
s
t
_
/
h
2
0
1
-
t
_
/
h
2
3
+
t
_
/
h
2


#### 3.2.1. Effect of Cell Wall Slenderness via Hexagonal RVE Simulations

Computational and analytical investigations on hexagonal RVEs are conducted so as to understand the effect of cell wall slendernesst
_
/
h on the effective stiffness properties in the transverse plane. In case of regular hexagonal RVEs, cell walls are assumed to behave as mechanisms rather than rigid structures where the bending moments are the dominant deformation mechanisms under both uniaxial and shear loadings [18].The comparison graphs presented in Figure5 indicate that there is a positive effect of t
_
/
h on the effective Young’s moduli E
X and E
Y and shear modulus G
X
Y. However, with increase in t
_
/
h, there is a decrease in Poisson’s ratio values v
X
Y and v
Y
X. In addition to the comparative studies, it is also deduced that Surveys I and II for regular hexagonal unit cells are in accordance with the computational homogenization results. This validates the current model and can hence be implemented on the proposed hexagonal-chiral configuration, which is elaborated in the following section.Figure 5
Comparison of effective elastic parameters based on analytical and computational homogenization results.


#### 3.2.2. Effect of Topology

For understanding the topological effects on the effective in-plane elastic parameters, closed form equations for regular hexagonal, square, and equilateral triangular unit cells listed in Table2 are compared with the current computational investigations on hexagonal-chiral RVEs. The results plotted for effective moduli E
X, E
Y, and G
X
Y in Figure 6 show that stiffness is favored as the topology changes from hexagonal to triangular RVE. As stated in [3, 11], the main reason is the increasing dominancy of stretching over bending with this type of topological change. As also seen in Figure 6, the proposed hexagonal-chiral configuration results in much higher effective Young’s moduli compared to regular hexagonal RVE. For instance, the ratio between the effective Young’s moduli of two configurations for t
_
/
h
=
0.20 is ~100, favoring the use of chirality. According to Figure 6, the hexagonal-chiral configuration yields the highest shear moduli among all of the investigated topologies. It is a promising result especially for the materials subject to shear loads—for example, packaging products and cargo containers.Figure 6
Comparison of effective elastic and shear moduli based on analytical and computational homogenization results.Comparison of effective Poisson’s ratiosv
X
Y and v
Y
X in Figure 7 indicates that the regular hexagonal RVE has the highest linear elastic response—in terms of stretching or contraction—to the loading in the perpendicular direction. However, this response is lower for the triangular RVE and almost negligible for square one. The proposed hexagonal-chiral configuration has v
X
Y and v
Y
X values that are much lower than the regular hexagonal RVE, which are comparable with those for the triangular and square RVEs.Figure 7
Comparison of effective Poisson’s ratios based on analytical and computational homogenization results.


## 3.1. Design of Experiments

In the present study, cell walls are taken to be transversely isotropic under the assumption of uniform distribution of cell wall material in the plane of interest. Mechanical parameters of the cell walls are selected asE
s
=
1000 Pa and v
s
=
0.4, which refer to typical cell wall Young’s modulus and Poisson’s ratio value, respectively. In relation to (9) and (10), three different in-plane loading conditions—that is, tensile load along the X- and Y-directions and the X
Y-shear load as listed in Table 1 and illustrated in Figure 4—are used to compute the effective stiffness properties and understand the effect of cell wall slenderness t
_
/
h, for which t
_
=
2
t, t is cell wall thickness, and h refers to cell wall height (as depicted in Figure 3), on the computed properties. The reason for taking the cell wall slenderness as t
_
=
2
t is to be able to compare the numerical results with the closed form solutions provided for double cell walls in the literature [5, 9]. The slenderness is taken to be in the range so that t
_
/
h
∈
0.02,0.20 with increment of Δ
t
_
/
h
=
0.02 whereas hub diameter is taken as D
=
h
/
2 for the chiral configuration illustrated in Figure 3(b).Table 1
Loading conditions.
Case
Imposed strains
e
X
X
M
e
Y
Y
M
2
e
X
Y
M
1
0.01
0
0
2
0
0.01
0
3
0
0
0.01Figure 4
Schematic representation of loading conditions based on the listed cases in Table1 (presented deformations are scaled larger than the actual ones for readability): (a) undeformed hexagonal RVE, (b) deformation under e
X
X
M, (c) deformation under e
Y
Y
M, (d) deformation under e
X
Y
M, (e) undeformed hexagonal-chiral RVE, (f) deformation under e
X
X
M, (g) deformation under e
Y
Y
M, and (h) deformation under e
X
Y
M.
(a)
(b)
(c)
(d)
(e)
(f)
(g)
(h)


## 3.2. Results

For understanding how cell wall slenderness (namely, cell wall thickness-to-height ratio) and cell topology (namely, chirality introduced inside the cell) affect the effective stiffness properties, simulation experiments are carried out on the RVEs. For this purpose, Abaqus/CAE is used, in which the periodic boundary conditions can be implemented. Thereafter, the solution domain is discretized into sets of finite elements—here, 6-noded quadratic triangular CPS6 provided in Abaqus/CAE. The results are compared with closed form solutions provided in Table2.Table 2
Effective Young’s moduli, shear modulus, and Poisson’s ratios as functions of cell wall slendernesst
_
/
h, where t
_
=
2
t for regular hexagonal, square, and equilateral triangular unit cells.
Prop.
Survey I_HEX [5]
Survey II_HEX [9]
Survey III_SQU [5]
Survey IV_TRI [5]
E
X
E
s
4
3
t
_
/
h
3
1
+
3
t
_
/
h
2
4
3
t
_
/
h
3
1
+
5.4
+
1.5
v
s
t
_
/
h
2
t
_
h
2
3
t
_
/
h
+
t
_
/
h
3
3
+
t
_
/
h
2
E
Y
E
s
4
3
t
_
/
h
3
1
+
3
t
_
/
h
2
4
3
t
_
/
h
3
1
+
5.4
+
1.5
v
s
t
_
/
h
2
t
_
h
2
3
t
_
/
h
+
t
_
/
h
3
3
+
t
_
/
h
2
G
X
Y
E
s
1
3
t
_
/
h
3
1
+
t
_
/
h
2
1
3
t
_
/
h
3
1
+
3.3
+
1.75
v
s
t
_
/
h
2
1
2
t
_
h
3
3
4
t
_
h
+
t
_
h
3
v
X
Y
1
-
t
_
/
h
2
1
+
3
t
_
/
h
2
1
+
1.4
+
1.5
v
s
t
_
/
h
2
1
+
5.4
+
1.5
v
s
t
_
/
h
2
0
1
-
t
_
/
h
2
3
+
t
_
/
h
2
v
Y
X
1
-
t
_
/
h
2
1
+
3
t
_
/
h
2
1
+
1.4
+
1.5
v
s
t
_
/
h
2
1
+
5.4
+
1.5
v
s
t
_
/
h
2
0
1
-
t
_
/
h
2
3
+
t
_
/
h
2


### 3.2.1. Effect of Cell Wall Slenderness via Hexagonal RVE Simulations

Computational and analytical investigations on hexagonal RVEs are conducted so as to understand the effect of cell wall slendernesst
_
/
h on the effective stiffness properties in the transverse plane. In case of regular hexagonal RVEs, cell walls are assumed to behave as mechanisms rather than rigid structures where the bending moments are the dominant deformation mechanisms under both uniaxial and shear loadings [18].The comparison graphs presented in Figure5 indicate that there is a positive effect of t
_
/
h on the effective Young’s moduli E
X and E
Y and shear modulus G
X
Y. However, with increase in t
_
/
h, there is a decrease in Poisson’s ratio values v
X
Y and v
Y
X. In addition to the comparative studies, it is also deduced that Surveys I and II for regular hexagonal unit cells are in accordance with the computational homogenization results. This validates the current model and can hence be implemented on the proposed hexagonal-chiral configuration, which is elaborated in the following section.Figure 5
Comparison of effective elastic parameters based on analytical and computational homogenization results.


### 3.2.2. Effect of Topology

For understanding the topological effects on the effective in-plane elastic parameters, closed form equations for regular hexagonal, square, and equilateral triangular unit cells listed in Table2 are compared with the current computational investigations on hexagonal-chiral RVEs. The results plotted for effective moduli E
X, E
Y, and G
X
Y in Figure 6 show that stiffness is favored as the topology changes from hexagonal to triangular RVE. As stated in [3, 11], the main reason is the increasing dominancy of stretching over bending with this type of topological change. As also seen in Figure 6, the proposed hexagonal-chiral configuration results in much higher effective Young’s moduli compared to regular hexagonal RVE. For instance, the ratio between the effective Young’s moduli of two configurations for t
_
/
h
=
0.20 is ~100, favoring the use of chirality. According to Figure 6, the hexagonal-chiral configuration yields the highest shear moduli among all of the investigated topologies. It is a promising result especially for the materials subject to shear loads—for example, packaging products and cargo containers.Figure 6
Comparison of effective elastic and shear moduli based on analytical and computational homogenization results.Comparison of effective Poisson’s ratiosv
X
Y and v
Y
X in Figure 7 indicates that the regular hexagonal RVE has the highest linear elastic response—in terms of stretching or contraction—to the loading in the perpendicular direction. However, this response is lower for the triangular RVE and almost negligible for square one. The proposed hexagonal-chiral configuration has v
X
Y and v
Y
X values that are much lower than the regular hexagonal RVE, which are comparable with those for the triangular and square RVEs.Figure 7
Comparison of effective Poisson’s ratios based on analytical and computational homogenization results.


## 3.2.1. Effect of Cell Wall Slenderness via Hexagonal RVE Simulations

Computational and analytical investigations on hexagonal RVEs are conducted so as to understand the effect of cell wall slendernesst
_
/
h on the effective stiffness properties in the transverse plane. In case of regular hexagonal RVEs, cell walls are assumed to behave as mechanisms rather than rigid structures where the bending moments are the dominant deformation mechanisms under both uniaxial and shear loadings [18].The comparison graphs presented in Figure5 indicate that there is a positive effect of t
_
/
h on the effective Young’s moduli E
X and E
Y and shear modulus G
X
Y. However, with increase in t
_
/
h, there is a decrease in Poisson’s ratio values v
X
Y and v
Y
X. In addition to the comparative studies, it is also deduced that Surveys I and II for regular hexagonal unit cells are in accordance with the computational homogenization results. This validates the current model and can hence be implemented on the proposed hexagonal-chiral configuration, which is elaborated in the following section.Figure 5
Comparison of effective elastic parameters based on analytical and computational homogenization results.


## 3.2.2. Effect of Topology

For understanding the topological effects on the effective in-plane elastic parameters, closed form equations for regular hexagonal, square, and equilateral triangular unit cells listed in Table2 are compared with the current computational investigations on hexagonal-chiral RVEs. The results plotted for effective moduli E
X, E
Y, and G
X
Y in Figure 6 show that stiffness is favored as the topology changes from hexagonal to triangular RVE. As stated in [3, 11], the main reason is the increasing dominancy of stretching over bending with this type of topological change. As also seen in Figure 6, the proposed hexagonal-chiral configuration results in much higher effective Young’s moduli compared to regular hexagonal RVE. For instance, the ratio between the effective Young’s moduli of two configurations for t
_
/
h
=
0.20 is ~100, favoring the use of chirality. According to Figure 6, the hexagonal-chiral configuration yields the highest shear moduli among all of the investigated topologies. It is a promising result especially for the materials subject to shear loads—for example, packaging products and cargo containers.Figure 6
Comparison of effective elastic and shear moduli based on analytical and computational homogenization results.Comparison of effective Poisson’s ratiosv
X
Y and v
Y
X in Figure 7 indicates that the regular hexagonal RVE has the highest linear elastic response—in terms of stretching or contraction—to the loading in the perpendicular direction. However, this response is lower for the triangular RVE and almost negligible for square one. The proposed hexagonal-chiral configuration has v
X
Y and v
Y
X values that are much lower than the regular hexagonal RVE, which are comparable with those for the triangular and square RVEs.Figure 7
Comparison of effective Poisson’s ratios based on analytical and computational homogenization results.


## 4. Conclusions

In the present study, topological and morphological effects on the effective stiffness of cellular materials in the transverse plane are investigated by means of a first-order strain-driven computational homogenization method. For this purpose, representative volume elements (RVEs) of regular hexagonal, square, triangular, and hexagonal-chiral configurations are studied to understand how cell topology (i.e., nominal versus chiral) and cell wall slenderness affect the effective stiffness properties. Closed form solutions for regular hexagonal, square, and triangular RVEs provided in the literature are then taken as the basis for model validation and comparison. The results show that there is a positive effect of cell wall slendernesst
_
/
h on the effective elastic parameters due to increase in the cell wall material volume. In addition to this, it is also deduced that there are drastic differences between regular hexagonal and hexagonal-chiral configurations, which can be explained in terms of deformation mechanism transformations between bending and stretching due to topological changes. Hence, the introduced chirality can be used as a tailored solution for materials and structures subject to high shear loads.



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*Source: 6534648-2016-07-19.xml*