# Summability Methods for Elastic Local Fields in Periodic Heterogeneous Materials

Authors: Andrea Caporale
Journal: Mathematical Problems in Engineering
 (2018)

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## Abstract

In the past, Eshelby’s method for a single inclusion in an infinite medium has been extended to periodic heterogeneous materials for the evaluation of global properties. In this work, the extended Eshelby’s method is used for the evaluation of local fields such as strain and stress in periodic heterogeneous materials characterized by unit cells containing multiple fibres or voids with different geometric and mechanical properties. The proposed method provides Fourier coefficients that are used to construct partial sums of three-dimensional trigonometric Fourier series of local fields. These partial sums exhibit unwanted effects such as the Gibbs phenomenon. In order to attenuate these effects, the behaviour of iterated Fejér partial sums and means of the Riesz summability method is investigated. Extensive numerical examples on both a multiphase composite and a material with voids are provided: in the examples, partial sums, iterated Fejér partial sums, and Riesz means for the local stress are compared with FEM solutions. The numerical comparison shows Riesz means perform better than partial sums and iterated Fejér partial sums and are effective in approximating elastic local fields in periodic heterogeneous solids.


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## Body

## 1. Introduction

The Fourier series are widely used in engineering [1, 2]. In the mechanics of solids and structures, Fourier series are frequently adopted for finding numerical and analytic solutions [3–5]. Geometric, mechanical properties, and local fields in heterogeneous materials with periodic microstructure seem to be naturally suited to being represented with periodic functions, but Fourier series and relevant partial sums exhibit large oscillations, known as Gibbs phenomenon, at the jump discontinuity of the field they represent. It is noted that the subdivision of the domain in smaller subdomains, as adopted in the Finite Element Method (FEM), favours the representation of jump discontinuity so that one can find many FEM applications [6, 7] in many scientific disciplines. Many authors [8, 9] have successfully used partial sums of Fourier series for determining global (averaged) properties of periodic composite materials. Specifically, Eshelby’s method introduced for a single inclusion in an infinite medium has been extended to the periodic heterogeneous materials for the evaluation of global properties. Few works [10, 11] have tried to use Fourier series for determining local fields such as strain and stress distribution in phases of composite materials and have observed anomalous large oscillations due to the Gibbs phenomenon. Recently, Caporale et al. [12] have applied summability methods in order to reduce the Gibbs phenomenon in unidirectional composites characterized by a simple geometry. In this work, the extended Eshelby’s method is used for determining the Fourier coefficients of the local strain in periodic heterogeneous materials with more complex microstructure and summability methods are applied in order to reduce the Gibbs phenomenon. Section 2 deals with Eshelby’s method extended to periodic materials for the evaluation of local fields. The means of the summability methods adopted in this work are briefly described in Section 3. Extensive numerical examples on both a multiphase composite and a material with voids are provided in Section 4: in these examples, partial sums, iterated Fejér partial sums, and Riesz means for the local stress are compared with solutions provided by accurate FEM analyses.


## 2. Partial Sums of Fourier Series via Eshelby’s Method Extended to Periodic Solids

The consideration is focused on an infinite periodic heterogeneous material, i.e., an infinitely extended solid that can be obtained by the infinite repetition of a representative unit cell along thex1-, x2-, and x3-axes of a Cartesian coordinate system. Figure 1(a) shows the boundary of the unit cell and the adopted coordinate system. The centre of the unit cell coincides with origin of the coordinate system. Figure 1(b) shows the unit cell with several inclusions, which may be fibres, particles, voids, defects, and so on. The dimensions of the unit cell along the x1-, x2-, and x3-axes of the coordinate system are denoted by 2a1, 2a2, and 2a3, respectively. In this work, it is assumed that a1=a2=a3=π, but the proposed formulation can be easily extended to unit cell with arbitrary dimensions. Because of periodicity, entities defining the geometry, the mechanical properties, and the local fields (such as strain and stress) of the considered material are defined by periodic functions. Here, Fourier series representations are adopted for the above-mentioned variables. Next, Z and N denote the set of integers and nonnegative integers, respectively, and i=-1. The geometric and mechanical properties are defined by the following fourth-order tensor:(1)Cx=∑ζ∈Z3C^ζeiζ·xwhere x=x1,x2,x3∈T3 with T≔[-π,π], ζ=ζ1,ζ2,ζ3 and ζ·x=ζ1x1+ζ2x2+ζ3x3. Tensor Cx also represents the local elasticity of the considered material. The Fourier coefficient C^ζ is(2)C^ζ=12π3∫T3Cxe-iζ·xdxClosed-form expressions of the Fourier coefficients (2) for different types of heterogeneous materials can be found in [11]. The first aim of this work is to determine local fields, such as strain and stress, in heterogeneous materials subject to given loads in the framework of linear elasticity. Therefore, the considered strain ε is the infinitesimal strain tensor, which is equal to the symmetric part of the displacement gradient; and the considered stress σ is the Cauchy stress tensor. Both ε and σ are second-order symmetric tensors and are functions of the spacial variable x, which represents a point of the unit cell. Under these assumptions, ε and σ appear as local fields in contrast with global entities (such as the overall properties of the material) which are averages over the volume of the unit cell. The local strain is given by(3)εx=∑ζ∈Z3ε^ζeiζ·xwhere the Fourier coefficient ε^ζ is(4)ε^ζ=12π3∫T3εxe-iζ·xdxThe average of the strain (3) over the unit cell is(5)ε0=ε^0=12π3∫T3εxdxTherefore, the local strain is represented as the addition of the average strain ε0 and the periodic part εp of the local strain:(6)εx=ε0+εpxwith(7)εpx=∑ζ∈Z3,ζ≠0ε^pζeiζ·xand(8)ε^pζ=ε^ζ∀ζ≠0Next, local strain and stress are evaluated in a periodic heterogeneous material subject to a given average strain ε0. According to Eshelby’s method, a homogeneous material equivalent to the considered periodic heterogeneous material is taken into account. The equivalence is made possible by imposing on the homogeneous material an eigenstrain ε∗(x), which is the unknown of the problem. The relation imposing this equivalence is the following consistency condition:(9)Cx:ε0+εpx=CR:ε0+εpx-ε∗x∀x∈T3where CR is the constant elasticity of the above-mentioned homogeneous material. The eigenstrain admits the Fourier series representation(10)ε∗x=∑ζ∈Z3ε^∗ζeiζ·xIn order to solve (9), coefficients ε^pζ for ζ≠0 are expressed in terms of ε^∗ζ through the following relation obtained by solving the equilibrium equation of the homogeneous material with elasticity CR subject to a periodic eigenstrain ε∗(x) [8]:(11)ε^pζ=S^pζ:ε^∗ζTaking into account (11), the consistency condition (9) becomes(12)∑ζ∈Z3C^ζeiζ·x:ε0+∑η∈Z3,η≠0S^pη:ε^∗ηeiη·x=CR:ε0+∑ζ∈Z3,ζ≠0S^pζ:ε^∗ζeiζ·x-∑ζ∈Z3ε^∗ζeiζ·x∀x∈T3Relation (12) provides a square system of equations in the unknowns ε^∗ζ if the infinite Fourier series in (12) are truncated. After solving this system imposing the truncation ζi,ηi≤ni=1,2,3 with n∈N, n<∞, and η≠0, all the coefficients ε^∗ζ such that ζi≤ni=1,2,3 with n∈N and n<∞ are known [11]. From (8) and (11), the Fourier coefficients ε^pζ and ε^ζ are also known for ζ≠0 and ζi≤ni=1,2,3 with n∈N and n<∞. Finally, it is possible to build the followingnth rectangular partial sum (n∈N) for the strain (given an integrable function fx with x∈R, the nth partial sum of the Fourier series of fx is denoted by snfx in mathematical literature. This convention is also used in this work, where thenth rectangular partial sum of the Fourier series of the strain tensor εx is denoted by snεx. Both εx and snεx are second-order tensors and the ij-component of snεx is denoted by snεijx. Similar notations can be found in scientific literature for other operators: for example, in [8], Fεζ denotes a Fourier coefficient of εx and its ij-component is denoted by Fεijζ):(13)snεx=∑ζ1≤n∑ζ2≤n∑ζ3≤nε^ζeiζ·xFormula (13) represents the following definition:(14)snεijx=∑ζ1≤n∑ζ2≤n∑ζ3≤nε^ijζeiζ·xwhere the scalar snεijx is thenth rectangular partial sum of the ij-component of the local strain tensor εx. Next, the expressions of the local stress σ(x) in periodic heterogeneous material subject to a given average strain ε0 are provided. In Eshelby’s method, the local stress σ(x) can be evaluated on the heterogeneous material or on the equivalent homogeneous material. The following relation provides the local stress on the equivalent homogeneous material:(15)σx=CR:ε0+εpx-ε∗x∀x∈T3A first approximation of the local stress σ(x) is obtained by replacing the periodic strain and eigenstrain in (15) with the corresponding partial sums. The resulting stress is(16)snσx=CR:snεx-snε∗x∀x∈T3where(17)snε∗x=∑ζ1≤n∑ζ2≤n∑ζ3≤nε^∗ζeiζ·xRewriting formula (16) in index notation, one obtains(18)snσijx=CijklR:snεklx-snεkl∗x∀x∈T3where the scalar snσijx is thenth rectangular partial sum of the ij-component of the local stress tensor σx. In Section 4, the partial sum stress (16) is plotted for two different types of periodic solids and is compared with the solution provided by the Finite Element Method (FEM). This comparison between partial sum stress and FEM solution shows that the partial sum stress is not adequate to describe accurately the local stress in heterogeneous solids: in fact, the Gibbs phenomenon occurs at the jump discontinuity of the local field and does not vanish by increasing n in the rectangular partial sums. In order to overcome this difficulty, means of summability methods are introduced in Section 3.Figure 1
(a) Boundary of the unit cell and adopted coordinate system; (b) unit cell containing several inclusions.
(a) (b)


## 3. Means of the Summability Methods for Local Fields in Periodic Solids

Summability methods are known to provide means with convergence properties better than those of the original partial sums, such as (13). In the last decade, many authors [13–17] have demonstrated the convergence properties of the means of the partial sums of the multidimensional trigonometric Fourier series. An aim of this work is to show the behaviour of the summability means in an area of the mechanics of solids. Next, Fejér and Riesz means together with the iterated Fejér partial sums [18] for the local strain are described and then used for the evaluation of local stress in periodic heterogeneous materials. In-depth details on convergence properties of the summability means adopted in this work can be found in [17]. Thenth lq-Fejér mean (n∈N) of the local strain εx is defined by(19)σnqεx=∑ζ∈Z3,ζq≤n1-ζqnε^ζeiζ·xAnalogously to Section 2, the left-hand side of (19) is a second-order tensor, whose ij-component is σnqεijx and represents thenth lq-Fejér mean ofij-component of the local strain tensor εx. A generalization of the mean (19) is the followingnth lq-Riesz mean (n∈N) of the local strain εx:(20)σnq,αεx=∑ζ∈Z3,ζq≤n1-ζqnγαε^ζeiζ·xwhere (in this work, the conceptual difference between partial sums and summability means is highlighted by the adoption of appropriate symbols. For example, sn is used to denote partial sums (see formula (13)) and σnq,α is used for Riesz summability means (see formula (20)), as also done in mathematical literature [17]) 0≤α<∞ and 1≤γ<∞. Finally, the iterated Fejér partial sum of the Fourier series (3) is(21)σnεx=∑ζ1≤n∑ζ2≤n∑ζ3≤n1-ζ1n+11-ζ2n+11-ζ3n+1ε^ζeiζ·xAs done at the end of Section 2, approximations of local stress are obtained by replacing periodic strain and eigenstrain in (15) with the relevant Riesz means or iterated Fejér partial sums. Therefore, the Riesz approximation of the local stress is(22)σnq,ασx=CR:σnq,αεx-σnq,αε∗x∀x∈T3and the iterated Fejér partial sum stress is(23)σnσx=CR:σnεx-σnε∗x∀x∈T3In Section 4, the approximations (22) and (23) are plotted for two different types of periodic solids and are compared with the solution provided by FEM.


## 4. Results and Discussion

The methods proposed in the previous sections are applied here to calculate the local stress in two different types of heterogeneous materials: the first type is a composite material containing long fibres with various geometrical and mechanical properties; the second type is a material containing circular voids with various sizes. In both applications, the behaviour of the partial sums (of the Fourier series) is first investigated, observing that these are not adequate to represent the local fields especially at the jump discontinuities of the local fields. The improvement provided by the iterated Fejér partial sums is also shown. Finally, the Riesz means are used, showing that they exhibit better convergence properties than those of the original partial sums of Fourier series.


### 4.1. Multiphase Composite

In the first numerical example, a unidirectional composite with unit cell containing multiple fibres with various sizes and various mechanical properties is considered. The origin of the Cartesian coordinate system is located at the centre of the unit cell. The lengths of the unit cell are given by2a1=2a2=2a3=2π; the unit of the lengths is not specified as the next results do not depend on it. The fibres are infinitely long right circular cylinders whose axes are parallel to the x1-axis of the coordinate system. The unit cell contains Nf=12 fibres. The generic fibre and its volume are denoted by Ωi for i=1,…,Nf. The intersection of a generic volume Ωi with plane x1=0 is a circle with radius ρi and position vector of centre denoted by xi, as shown in Figure 2 representing the intersection of a unit cell with the plane x1=0. Centres xi=0,x2i,x3i and radii ρi of fibres Ωi for i=1,…,12 are reported in Table 1. It is assumed that the unit cell is symmetric with respect to the coordinate planes: thus, xki+j=xki for i=1,2,3, j=3,6,9, and k=1,2,3. xi+j for i=1,2,3 is the position vector of the centres of the fibres in the volume characterized by -π≤x2≤0 and 0≤x3≤π for j=3 and the volume characterized by -π≤x2≤0 and -π≤x3≤0 for j=6. Matrix and fibres are linear elastic and isotropic; the interface between matrix and fibres is perfect. Young’s modulus of the matrix is denoted by E0 and is equal to one GPa; Young’s modulus of the generic fibre Ωi for i=1,…,12 is denoted by Ei. Poisson’s ratio of the matrix is ν0 and is equal to 0.35. Poisson’s ratio of the generic fibre Ωi for i=1,…,12 is denoted by νi. The geometrical and mechanical properties adopted for the fibres of the multiphase composite considered in this first example are reported in Table 1. It is noted that the considered composite is unidirectional and now the previous three-dimensional series (such as (13), (20), and (21)) applied to unidirectional composites reduce to two-dimensional series by imposing ζ1=0.Table 1
Geometrical and mechanical properties of the fibres of the multiphase composite.
i x 2 i / 2 π x 3 i / 2 π ρ i / 2 π E i (GPa) ν i 1 0.12 0.12 0.09 5.0 0.2 2 0.35 0.16 0.10 4.5 0.2 3 0.20 0.35 0.08 4.0 0.2 4 −0.12 0.12 0.09 5.0 0.2 5 −0.35 0.16 0.10 4.5 0.2 6 −0.20 0.35 0.08 4.0 0.2 7 −0.12 −0.12 0.09 5.0 0.2 8 −0.35 −0.16 0.10 4.5 0.2 9 −0.20 −0.35 0.08 4.0 0.2 10 0.12 −0.12 0.09 5.0 0.2 11 0.35 −0.16 0.10 4.5 0.2 12 0.20 −0.35 0.08 4.0 0.2Figure 2
FibresΩi for i=1,…,Nf in the unit cell of the multiphase composite with Nf=12.In the following, the multiphase composite is subject to an average strainε0ij=(δi1δj3+δi3δj1)/2, where ε0ij is the ij-component of the tensor ε0 and δij is the Kronecker delta. Figure 3 shows a three-dimensional surface, whose points are x2,x3,s110σ130,x2,x3 for x2≤π and x3≤π. The function s110σ130,x2,x3 is the approximation (16) of the local stress σ13 evaluated at the plane x1=0 for n=110. In the figures of this work, the stress is in GPa and “pi” in the axes stands for π. Gibbs phenomenon is evident and large oscillations of the surface occur not only at the jump discontinuity along the fibre-matrix interface but also in the interior of the generic fibre and in some portion of the matrix. This behaviour is confirmed in Figure 4, where approximations (16) and (23) of the local stress σ13 and σ12 are plotted in different view sections for n=110. Specifically, Figures 4(a) and 4(b) show the plots of stress approximations s110σ130,x2,x3 and s110σ120,x2,x3, respectively, for x2≤π and x3≤π. Figures 4(c) and 4(d) show the plots of s110σ130,x2,π/4 and s110σ120,x2,π/4, respectively, against x2-axis for x2≤π: in other words, the approximations are plotted along the straight line segment with end points given by 0,-π,π/4 and 0,π,π/4. Figures 4(e) and 4(f) show the plots of stress approximations s110σ130,3π/4,x3 and s110σ120,3π/4,x3, respectively, against x3-axis for x3≤π: these approximations are plotted along the straight line segment with end points given by 0,3π/4,-π and 0,3π/4,π. The iterated Fejér partial sum stress σ110σ13x is also plotted in Figures 4(c) and 4(e): σ110σ13x represents the approximation (23) of the local stress σ13 for n=110. A similar description applies to σ110σ12x, which is plotted in Figures 4(d) and 4(f). In the figure legends of this work, the iterated Fejér partial sum stress is denoted by “Iter. Fejér.” In Figures 4(c)–4(f), the solutions provided by accurate FEM analyses are also plotted for comparison purpose and are denoted by the acronym “FEM” in the figure legends (FEM solution is plotted only for 0≤x2≤π in Figures 4(c) and 4(d)).Figure 3
Partial sum stresss110σ13x for the longitudinal shear stress of the multiphase composite.Figure 4
Gibbs phenomenon in partial sums and iterated Fejér partial sums for the local stress of the multiphase composite: (a) partial sum stresss110σ13x; (b) partial sum stress s110σ12x; (c) partial sum stress s110σ130,x2,π/4 and iterated Fejér partial sum σ110σ130,x2,π/4 along the x2-axis; (d) partial sum stress s110σ120,x2,π/4 and iterated Fejér partial sum σ110σ120,x2,π/4 along the x2-axis; (e) partial sum stress s110σ130,3π/4,x3 and iterated Fejér partial sum σ110σ130,3π/4,x3 along the x3-axis; (f) partial sum stress s110σ120,3π/4,x3 and iterated Fejér partial sum σ110σ120,3π/4,x3 along the x3-axis.
(a) (b) (c) (d) (e) (f)Figures4(c)–4(f) show the iterated Fejér partial sum stress behaves better than the partial sum stress given by approximation (16). However, accuracy of the iterated Fejér partial sum stress is not satisfactory in some portions of the solids; see, e.g., the behaviour of the green curve in the matrix phase of Figure 4(c). In order to obtain better approximations of the local stress, means of summability methods have been introduced in Section 3 and are applied to the considered multiphase composite in Section 4.1. Relevant results are shown in Figure 5, where Riesz approximations (22) of the local stress σ13 and σ12 are plotted in different view sections for n=110. The values α=γ=1.8 are adopted in the results of Section 4. Figures 5(a) and 5(b) show the plots of σ110∞,ασ130,x2,x3 and σ110∞,ασ120,x2,x3, respectively, for x2≤π and x3≤π. Figures 5(c) and 5(d) show the plots of stress approximations σ110∞,ασ130,x2,π/4 and σ110∞,ασ120,x2,π/4, respectively, against x2-axis for x2≤π. Figures 5(e) and 5(f) show the plots of stress approximations σ110∞,ασ130,3π/4,x3 and σ110∞,ασ120,3π/4,x3, respectively, against x3-axis for x3≤π. In Figures 5(c)–5(f), the solutions provided by accurate FEM analyses are also plotted for comparison purpose (FEM solution is plotted only for 0≤x2≤π in Figures 5(c) and 5(d)). Figure 5 shows Riesz means σ110∞,ασ(x) greatly reduce the Gibbs phenomenon and this also appears in Figure 6, which represents a three-dimensional surface, whose points are x2,x3,σ110∞,ασ130,x2,x3 for x2≤π and x3≤π. Finally, Figure 7 illustrates a comparison between Riesz mean and FEM approximations: Figure 7(a) shows the plot of the Riesz mean σ110∞,ασ130,x2,x3 for x2≤π and x3≤π; Figure 7(b) shows the FEM approximation of the local stress σ13 for 0≤x2≤π and x3≤π.Figure 5
Riesz approximations of the local stress for the multiphase composite: (a)σ110∞,ασ13x; (b) σ110∞,ασ12x; (c) σ110∞,ασ130,x2,π/4 along the x2-axis; (d) σ110∞,ασ120,x2,π/4 along the x2-axis; (e) σ110∞,ασ130,3π/4,x3 along the x3-axis; (f) σ110∞,ασ120,3π/4,x3 along the x3-axis.
(a) (b) (c) (d) (e) (f)Figure 6
Riesz longitudinal shear stressσ110∞,ασ13x of the multiphase composite.Figure 7
Comparison between Riesz mean and FEM solutions: (a)σ110∞,ασ13x; (b) FEM approximation of σ13.
(a) (b)Figure5 shows a good agreement between Riesz means and FEM solution. Some critical points appear at the fibre-matrix interface mainly where the maximum shear stress occurs. In order to quantify a disagreement, the following percentage error is evaluated:(24)e=τFEM,max-τS,maxτFEM,max×100where τFEM,max is the maximum shear stress provided by FEM solution in a given previous figure and τS,max is the maximum value of the iterated Fejér partial sum stress or the Riesz mean in the same figure where τFEM,max has been evaluated. For each of Figures 4(c), 4(d), 5(c), and 5(d), the percentage error e is reported in Table 2, where the value adopted for τS,max is also specified. For the shear stress σ13, the percentage error is below 1% and the error provided by the iterated Fejér partial sum stress is less than the error provided by the Riesz mean, whose overall behaviour is better than iterated Fejér partial sum stress. For the shear stress σ12, the Riesz mean provides a percentage error equal to 3.93%. This relatively high value of e occurs at some portions of the fibre-matrix interface, where the stress field has a jump discontinuity; elsewhere the Riesz mean performs better as shown in Figure 5. It is noted that the proposed Riesz means reduce not only the Gibbs phenomenon but also the percentage error: a greater value of n in σnq,ασ(x) involves smaller values of the percentage error e. Therefore, a relatively high value of e can be reduced by adopting larger values of n. On the other hand, the partial sum stress (16) does not exhibit this convergent behaviour at jump discontinuity.Table 2
Percentage errore in critical points of the multiphase composite.
Figure4(c) Figure5(c) Figure4(d) Figure5(d) τ S , m a x max ⁡ s 110 σ 13 max ⁡ σ 110 ∞ , α σ 13 max ⁡ s 110 σ 12 max ⁡ σ 110 ∞ , α σ 12 e 0.40 0.85 12.64 3.93Finally, an observation on the CPU memory usage is provided. In order to evaluate the partial sum stresssnσ(x) or the Riesz mean σnq,ασ(x), one has to solve a system of nS scalar equations in nS scalar unknowns, where nS=2n+12 thanks to polar symmetry and the symmetry of the unit cell with respect to the x1-x2 and x1-x3 coordinate planes. Therefore, the number of scalar equations is nS=24642 for n=110. The number of equations in each of the accurate FEM analyses (which have been executed on half of the unit cell) is more than 1.5×105: this value should not be compared with ns and is provided with the sole intent to highlight the refinement of the adopted FEM mesh and the accuracy of the relevant results.


### 4.2. Material with Voids

In this section, the approximations provided by partial sums, iterated Fejér partial sums, and Riesz means are compared with FEM solutions for a material containing voids. To this end, one should realize methods and models appropriate for a material with voids. In contrast with this rigorous approach, one can assume that inclusions with sufficiently small stiffness represent the voids. Following this approach, this section considers a heterogeneous material identical to that described in Section4.1 except for Ei=10-6 GPa for i=1,…,12. Fibres with such Young’s moduli are practically voids embedded in the matrix. Figure 8 illustrates the Gibbs phenomenon in partial sum stress s110σ13x. Approximations provided by partial sums, iterated Fejér partial sums, and FEM simulations are compared with each other in Figure 9. Finally, the improvements of Riesz means are shown in Figures 10 and 11. For brevity, detailed descriptions of results presented in this section are omitted: symbols reported in captions and legends of Figures 8, 9, 10, and 11 have already been commented in Section 4.1.Figure 8
Partial sum stresss110σ13x for the longitudinal shear stress of the material with voids.Figure 9
Gibbs phenomenon in partial sums and iterated Fejér partial sums for the local stress of the material with voids: (a) partial sum stresss110σ13x; (b) partial sum stress s110σ12x; (c) partial sum stress s110σ130,x2,π/4 and iterated Fejér partial sum σ110σ130,x2,π/4 along the x2-axis; (d) partial sum stress s110σ120,x2,π/4 and iterated Fejér partial sum σ110σ120,x2,π/4 along the x2-axis; (e) partial sum stress s110σ130,3π/4,x3 and iterated Fejér partial sum σ110σ130,3π/4,x3 along the x3-axis; (f) partial sum stress s110σ120,3π/4,x3 and iterated Fejér partial sum σ110σ120,3π/4,x3 along the x3-axis.
(a) (b) (c) (d) (e) (f)Figure 10
Riesz approximations of the local stress for the material with voids: (a)σ110∞,ασ13x; (b) σ110∞,ασ12x; (c) σ110∞,ασ130,x2,π/4 along the x2-axis; (d) σ110∞,ασ120,x2,π/4 along the x2-axis; (e) σ110∞,ασ130,3π/4,x3 along the x3-axis; (f) σ110∞,ασ120,3π/4,x3 along the x3-axis.
(a) (b) (c) (d) (e) (f)Figure 11
Riesz longitudinal shear stressσ110∞,ασ13x of the material with voids.


## 4.1. Multiphase Composite

In the first numerical example, a unidirectional composite with unit cell containing multiple fibres with various sizes and various mechanical properties is considered. The origin of the Cartesian coordinate system is located at the centre of the unit cell. The lengths of the unit cell are given by2a1=2a2=2a3=2π; the unit of the lengths is not specified as the next results do not depend on it. The fibres are infinitely long right circular cylinders whose axes are parallel to the x1-axis of the coordinate system. The unit cell contains Nf=12 fibres. The generic fibre and its volume are denoted by Ωi for i=1,…,Nf. The intersection of a generic volume Ωi with plane x1=0 is a circle with radius ρi and position vector of centre denoted by xi, as shown in Figure 2 representing the intersection of a unit cell with the plane x1=0. Centres xi=0,x2i,x3i and radii ρi of fibres Ωi for i=1,…,12 are reported in Table 1. It is assumed that the unit cell is symmetric with respect to the coordinate planes: thus, xki+j=xki for i=1,2,3, j=3,6,9, and k=1,2,3. xi+j for i=1,2,3 is the position vector of the centres of the fibres in the volume characterized by -π≤x2≤0 and 0≤x3≤π for j=3 and the volume characterized by -π≤x2≤0 and -π≤x3≤0 for j=6. Matrix and fibres are linear elastic and isotropic; the interface between matrix and fibres is perfect. Young’s modulus of the matrix is denoted by E0 and is equal to one GPa; Young’s modulus of the generic fibre Ωi for i=1,…,12 is denoted by Ei. Poisson’s ratio of the matrix is ν0 and is equal to 0.35. Poisson’s ratio of the generic fibre Ωi for i=1,…,12 is denoted by νi. The geometrical and mechanical properties adopted for the fibres of the multiphase composite considered in this first example are reported in Table 1. It is noted that the considered composite is unidirectional and now the previous three-dimensional series (such as (13), (20), and (21)) applied to unidirectional composites reduce to two-dimensional series by imposing ζ1=0.Table 1
Geometrical and mechanical properties of the fibres of the multiphase composite.
i x 2 i / 2 π x 3 i / 2 π ρ i / 2 π E i (GPa) ν i 1 0.12 0.12 0.09 5.0 0.2 2 0.35 0.16 0.10 4.5 0.2 3 0.20 0.35 0.08 4.0 0.2 4 −0.12 0.12 0.09 5.0 0.2 5 −0.35 0.16 0.10 4.5 0.2 6 −0.20 0.35 0.08 4.0 0.2 7 −0.12 −0.12 0.09 5.0 0.2 8 −0.35 −0.16 0.10 4.5 0.2 9 −0.20 −0.35 0.08 4.0 0.2 10 0.12 −0.12 0.09 5.0 0.2 11 0.35 −0.16 0.10 4.5 0.2 12 0.20 −0.35 0.08 4.0 0.2Figure 2
FibresΩi for i=1,…,Nf in the unit cell of the multiphase composite with Nf=12.In the following, the multiphase composite is subject to an average strainε0ij=(δi1δj3+δi3δj1)/2, where ε0ij is the ij-component of the tensor ε0 and δij is the Kronecker delta. Figure 3 shows a three-dimensional surface, whose points are x2,x3,s110σ130,x2,x3 for x2≤π and x3≤π. The function s110σ130,x2,x3 is the approximation (16) of the local stress σ13 evaluated at the plane x1=0 for n=110. In the figures of this work, the stress is in GPa and “pi” in the axes stands for π. Gibbs phenomenon is evident and large oscillations of the surface occur not only at the jump discontinuity along the fibre-matrix interface but also in the interior of the generic fibre and in some portion of the matrix. This behaviour is confirmed in Figure 4, where approximations (16) and (23) of the local stress σ13 and σ12 are plotted in different view sections for n=110. Specifically, Figures 4(a) and 4(b) show the plots of stress approximations s110σ130,x2,x3 and s110σ120,x2,x3, respectively, for x2≤π and x3≤π. Figures 4(c) and 4(d) show the plots of s110σ130,x2,π/4 and s110σ120,x2,π/4, respectively, against x2-axis for x2≤π: in other words, the approximations are plotted along the straight line segment with end points given by 0,-π,π/4 and 0,π,π/4. Figures 4(e) and 4(f) show the plots of stress approximations s110σ130,3π/4,x3 and s110σ120,3π/4,x3, respectively, against x3-axis for x3≤π: these approximations are plotted along the straight line segment with end points given by 0,3π/4,-π and 0,3π/4,π. The iterated Fejér partial sum stress σ110σ13x is also plotted in Figures 4(c) and 4(e): σ110σ13x represents the approximation (23) of the local stress σ13 for n=110. A similar description applies to σ110σ12x, which is plotted in Figures 4(d) and 4(f). In the figure legends of this work, the iterated Fejér partial sum stress is denoted by “Iter. Fejér.” In Figures 4(c)–4(f), the solutions provided by accurate FEM analyses are also plotted for comparison purpose and are denoted by the acronym “FEM” in the figure legends (FEM solution is plotted only for 0≤x2≤π in Figures 4(c) and 4(d)).Figure 3
Partial sum stresss110σ13x for the longitudinal shear stress of the multiphase composite.Figure 4
Gibbs phenomenon in partial sums and iterated Fejér partial sums for the local stress of the multiphase composite: (a) partial sum stresss110σ13x; (b) partial sum stress s110σ12x; (c) partial sum stress s110σ130,x2,π/4 and iterated Fejér partial sum σ110σ130,x2,π/4 along the x2-axis; (d) partial sum stress s110σ120,x2,π/4 and iterated Fejér partial sum σ110σ120,x2,π/4 along the x2-axis; (e) partial sum stress s110σ130,3π/4,x3 and iterated Fejér partial sum σ110σ130,3π/4,x3 along the x3-axis; (f) partial sum stress s110σ120,3π/4,x3 and iterated Fejér partial sum σ110σ120,3π/4,x3 along the x3-axis.
(a) (b) (c) (d) (e) (f)Figures4(c)–4(f) show the iterated Fejér partial sum stress behaves better than the partial sum stress given by approximation (16). However, accuracy of the iterated Fejér partial sum stress is not satisfactory in some portions of the solids; see, e.g., the behaviour of the green curve in the matrix phase of Figure 4(c). In order to obtain better approximations of the local stress, means of summability methods have been introduced in Section 3 and are applied to the considered multiphase composite in Section 4.1. Relevant results are shown in Figure 5, where Riesz approximations (22) of the local stress σ13 and σ12 are plotted in different view sections for n=110. The values α=γ=1.8 are adopted in the results of Section 4. Figures 5(a) and 5(b) show the plots of σ110∞,ασ130,x2,x3 and σ110∞,ασ120,x2,x3, respectively, for x2≤π and x3≤π. Figures 5(c) and 5(d) show the plots of stress approximations σ110∞,ασ130,x2,π/4 and σ110∞,ασ120,x2,π/4, respectively, against x2-axis for x2≤π. Figures 5(e) and 5(f) show the plots of stress approximations σ110∞,ασ130,3π/4,x3 and σ110∞,ασ120,3π/4,x3, respectively, against x3-axis for x3≤π. In Figures 5(c)–5(f), the solutions provided by accurate FEM analyses are also plotted for comparison purpose (FEM solution is plotted only for 0≤x2≤π in Figures 5(c) and 5(d)). Figure 5 shows Riesz means σ110∞,ασ(x) greatly reduce the Gibbs phenomenon and this also appears in Figure 6, which represents a three-dimensional surface, whose points are x2,x3,σ110∞,ασ130,x2,x3 for x2≤π and x3≤π. Finally, Figure 7 illustrates a comparison between Riesz mean and FEM approximations: Figure 7(a) shows the plot of the Riesz mean σ110∞,ασ130,x2,x3 for x2≤π and x3≤π; Figure 7(b) shows the FEM approximation of the local stress σ13 for 0≤x2≤π and x3≤π.Figure 5
Riesz approximations of the local stress for the multiphase composite: (a)σ110∞,ασ13x; (b) σ110∞,ασ12x; (c) σ110∞,ασ130,x2,π/4 along the x2-axis; (d) σ110∞,ασ120,x2,π/4 along the x2-axis; (e) σ110∞,ασ130,3π/4,x3 along the x3-axis; (f) σ110∞,ασ120,3π/4,x3 along the x3-axis.
(a) (b) (c) (d) (e) (f)Figure 6
Riesz longitudinal shear stressσ110∞,ασ13x of the multiphase composite.Figure 7
Comparison between Riesz mean and FEM solutions: (a)σ110∞,ασ13x; (b) FEM approximation of σ13.
(a) (b)Figure5 shows a good agreement between Riesz means and FEM solution. Some critical points appear at the fibre-matrix interface mainly where the maximum shear stress occurs. In order to quantify a disagreement, the following percentage error is evaluated:(24)e=τFEM,max-τS,maxτFEM,max×100where τFEM,max is the maximum shear stress provided by FEM solution in a given previous figure and τS,max is the maximum value of the iterated Fejér partial sum stress or the Riesz mean in the same figure where τFEM,max has been evaluated. For each of Figures 4(c), 4(d), 5(c), and 5(d), the percentage error e is reported in Table 2, where the value adopted for τS,max is also specified. For the shear stress σ13, the percentage error is below 1% and the error provided by the iterated Fejér partial sum stress is less than the error provided by the Riesz mean, whose overall behaviour is better than iterated Fejér partial sum stress. For the shear stress σ12, the Riesz mean provides a percentage error equal to 3.93%. This relatively high value of e occurs at some portions of the fibre-matrix interface, where the stress field has a jump discontinuity; elsewhere the Riesz mean performs better as shown in Figure 5. It is noted that the proposed Riesz means reduce not only the Gibbs phenomenon but also the percentage error: a greater value of n in σnq,ασ(x) involves smaller values of the percentage error e. Therefore, a relatively high value of e can be reduced by adopting larger values of n. On the other hand, the partial sum stress (16) does not exhibit this convergent behaviour at jump discontinuity.Table 2
Percentage errore in critical points of the multiphase composite.
Figure4(c) Figure5(c) Figure4(d) Figure5(d) τ S , m a x max ⁡ s 110 σ 13 max ⁡ σ 110 ∞ , α σ 13 max ⁡ s 110 σ 12 max ⁡ σ 110 ∞ , α σ 12 e 0.40 0.85 12.64 3.93Finally, an observation on the CPU memory usage is provided. In order to evaluate the partial sum stresssnσ(x) or the Riesz mean σnq,ασ(x), one has to solve a system of nS scalar equations in nS scalar unknowns, where nS=2n+12 thanks to polar symmetry and the symmetry of the unit cell with respect to the x1-x2 and x1-x3 coordinate planes. Therefore, the number of scalar equations is nS=24642 for n=110. The number of equations in each of the accurate FEM analyses (which have been executed on half of the unit cell) is more than 1.5×105: this value should not be compared with ns and is provided with the sole intent to highlight the refinement of the adopted FEM mesh and the accuracy of the relevant results.


## 4.2. Material with Voids

In this section, the approximations provided by partial sums, iterated Fejér partial sums, and Riesz means are compared with FEM solutions for a material containing voids. To this end, one should realize methods and models appropriate for a material with voids. In contrast with this rigorous approach, one can assume that inclusions with sufficiently small stiffness represent the voids. Following this approach, this section considers a heterogeneous material identical to that described in Section4.1 except for Ei=10-6 GPa for i=1,…,12. Fibres with such Young’s moduli are practically voids embedded in the matrix. Figure 8 illustrates the Gibbs phenomenon in partial sum stress s110σ13x. Approximations provided by partial sums, iterated Fejér partial sums, and FEM simulations are compared with each other in Figure 9. Finally, the improvements of Riesz means are shown in Figures 10 and 11. For brevity, detailed descriptions of results presented in this section are omitted: symbols reported in captions and legends of Figures 8, 9, 10, and 11 have already been commented in Section 4.1.Figure 8
Partial sum stresss110σ13x for the longitudinal shear stress of the material with voids.Figure 9
Gibbs phenomenon in partial sums and iterated Fejér partial sums for the local stress of the material with voids: (a) partial sum stresss110σ13x; (b) partial sum stress s110σ12x; (c) partial sum stress s110σ130,x2,π/4 and iterated Fejér partial sum σ110σ130,x2,π/4 along the x2-axis; (d) partial sum stress s110σ120,x2,π/4 and iterated Fejér partial sum σ110σ120,x2,π/4 along the x2-axis; (e) partial sum stress s110σ130,3π/4,x3 and iterated Fejér partial sum σ110σ130,3π/4,x3 along the x3-axis; (f) partial sum stress s110σ120,3π/4,x3 and iterated Fejér partial sum σ110σ120,3π/4,x3 along the x3-axis.
(a) (b) (c) (d) (e) (f)Figure 10
Riesz approximations of the local stress for the material with voids: (a)σ110∞,ασ13x; (b) σ110∞,ασ12x; (c) σ110∞,ασ130,x2,π/4 along the x2-axis; (d) σ110∞,ασ120,x2,π/4 along the x2-axis; (e) σ110∞,ασ130,3π/4,x3 along the x3-axis; (f) σ110∞,ασ120,3π/4,x3 along the x3-axis.
(a) (b) (c) (d) (e) (f)Figure 11
Riesz longitudinal shear stressσ110∞,ασ13x of the material with voids.


## 5. Conclusions

In literature, methods based on Fourier series have been used to determine the global (averaged) properties of composite materials [8, 9, 19, 20]. On the other hand, few works based on Fourier series have tried to evaluate the local fields, such as the strain and stress distribution in the material microstructure, and have found difficulties due to the Gibbs phenomenon. In this work, summability methods of three-dimensional trigonometric Fourier series are applied in order to attenuate the Gibbs phenomenon occurring in local stress field in periodic heterogeneous materials characterized by unit cells containing multiple fibres or voids with different geometric and mechanical properties. An advantage of the proposed method is the easiness of modelling of the material microstructure through the functions (2), which admit closed-form expressions in many practical cases. Extensive numerical results are provided: partial sums, iterated Fejér partial sums, and Riesz means are compared with the solutions provided by accurate FEM analyses. The results show the effectiveness of the Riesz means, which have better convergence properties than those exhibited by partial sums and iterated Fejér partial sums.



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