# Modeling of constitutive behaviour of anisotropic composite material using multiscale approach.

1. Introduction

Particle-reinforced metal matrix composites have found application in many areas of engineering practice. They usually provide higher strength, stiffness and weight savings in comparison with conventional metal alloys. Moreover, this group of materials is attractive due to their cost-effectiveness [1]. Estimation of elastic-plastic response in particle-reinforced composites is a complex problem depending on variety of factors such as particle size, shape, distribution or orientation [1, 2]. In this paper, special attention is put into consideration of material anisotropy caused by manufacturing process. One of the most popular ways of manufacturing particle-reinforced composites is through an extrusion. Extrusion is a process connected with creating objects with fixed cross section. It allows to manufacture complex cross sections with brittle materials that in turn result in parts with excellent surface finish [3]. Because extrusion is classified as secondary processing method, it is preceded by one of primary processing methods such as powder metallurgy [3, 4]. In case of application of powder metallurgy, raw composite constituents in the form of powders are mixed, milled, pressed into compacted powder and finally extruded [4]. After extrusion, generally a significant degree of orientation of the reinforcement particles is expected along the extrusion axis. However, the degree of mechanical property anisotropy is related to the volume fraction of particles. In particular, mechanical property anisotropy increases with increasing volume fraction of particles due to the reduction in mean free path between the particles [5]. Therefore, during this study, composite with 0.3 volume fraction of the reinforcement is taken into consideration. In this case, anisotropy of mechanical properties plays a significant role in overall material performance. During this research, spatial distribution of the particles, measured experimenttally, is taken into account by assuming results presented in work [6]. The three dimensional representative volume element (RVE) geometry that represents the material microstructure is created by using Digimat-FE software. The RVE is a statistical representation of material properties. It should contain enough information to describe the behavior of considered composite. The analysis of the RVE is conducted by the finite element method, in particular commercial MSC Marc solver is applied. In addition, different approaches based on the two step homogenization method [7] and the orientation averaging procedure [8] are proposed. Results obtained numerically by using different approaches are presented, compared and related to experimental results that can be found in work [9].

2. Determination of the RVE geometry

The RVE geometry is created by taking into account the spatial distribution of the particles measured experimentally. In particular, results presented in work [6] are considered. In the analyzed case, the shape of the particles is simplified and modeled as ellipsoids with constant size and aspect ratio of 2.68. The histogram that represents the probability distribution of the angle between the particle axis and the extrusion axis is presented in Fig. 1. To create the RVE geometry eight families of particles with angles and probability density corresponding to this histogram were set up. The created RVE that contains 250 particles is presented in Fig. 2, each color indicating different family of the particles, X is the axis of the extrusion. Considered RVE is a rectangular cuboid with the dimensions 500x250x500 pm. The orientation of the particles in the extrusion plane YZ is usually random. In the other two symmetry planes distribution shows similar trend that is in accordance with the histogram presented in Fig. 1 [6].

[FIGURE 1 OMITTED]

[FIGURE 2 OMITTED]

3. Determination of effective anisotropic properties

3.1. Homogenization based on finite element analysis of the RVE

To calculate the effective elasticity tensors of heterogeneous materials, the usage of homogenization procedure is essential. The homogenization procedure involves replacing the heterogeneous material with an equivalent homogeneous material. Calculating the equivalent material properties requires solving six RVE boundary value problems (BVP) in three dimensional case [2, 10]. For each BVP a prescribed strain is applied in accordance with Eq. (1) (a superscript j = 1-6 indicates the number of analysis, I = 1-6).

[[epsilon].sup.(j).sub.i] = [[delta].sup.ij] (1)

In addition, periodic boundary conditions are introduced [11]. After solving six BVPs, both the stresses Eq. (2) and strains Eq. (3) are averaged in post-processing stage of the analysis.

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (2)

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (3)

where <[[sigma].sub.ij]> is average stress, <[[epsilon].sub.ij]> is average strain, [[sigma].sub.ij] is stress in the RVE, [[epsilon].sub.ij] is strain in the RVE and [V.sub.RVE] is volume of the RVE.

The relation between stress and strain tensors is expressed by:

<[[sigma].sub.ij]> = C < [[epsilon].sub.ij] > (4)

where C is elasticity tensor.

The presented methodology is applied to the estimation of effective properties of the material which is represented by the RVE presented in Fig. 2, as well as for material with inclusions perfectly aligned with the extrusion axis.

3.2. Orientation averaging

Another approach that deals with determining the effective properties of composite materials with non-homogenous orientation of the reinforcement is orientation averaging. The orientation averaging procedure is based on equation proposed by Advani and Tucker [8]:

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (5)

where [a.sub.ij], [a.sub.ijlkl] are second and fourth-order orientation tensors and [B.sub.1]-[B.sub.5] are scalar constants related to the components of stiffness tensor of unidirectional composite.

A drawback of this approach is that the fourth-order tensor [a.sub.ijkl] is required to calculate the effective stiffness. In practice, very frequently only the second order orientation tensor is known. The graphical representation of the second-order orientation tensor is presented in Fig. 3 where [[lambda].sub.i] and [n.sub.i] are eigenvalues and eigenvectors.

[FIGURE 3 OMITTED]

The second-order orientation tensor has the following properties:

[a.sub.ii] = 1, (6)

[a.sub.ij] = [a.sub.ji]. (7)

Therefore, the second-order orientation tensor has five independent components. To estimate the fourth-order orientation tensor, closure approximations are commonly considered where the fourth-order tensor components are calculated from the components of the second-order tensor. The closure that provide the most accurate results in comparison with experimentally measured fourth-order tensors is the orthotropic closure proposed by Cintra and Tucker [12, 13] in their work [14]. The orthotropic closures are based on the assumption that the principal axes of the approximated fourth order tensors are in alignment with the principal axes of the second order tensor [14]. The definition of orthotropic closure approximation reduces the choice to three scalar functions f such as [a.sub.iiii] =[f.sub.i]([a.sub.1], [a.sub.2]). Cintra and Tucker used in their work second-degree polynomials:

[a.sub.iii] = [T.sup.1.sub.i1] + [T.sup.2.sub.i2][a.sub.(1)] + [T.sup.3.sub.i3][a.sub.(1)] + [T.sup.4.sub.i4][a.sub.(2)] + [T.sup.5.sub.i5][a.sub.(2)] + [T.sup.6.sub.i6][a.sub.(1)][a.sub.(2)], (8)

where there is no sum on i, [a.sub.(1)] and [a.sub.(2)] are the first and the second eigenvalue of the second-order orientation tensor, [T.sub.m.sup.i] is a matrix of coefficients which can be determined by using specific orientation distributions (smooth version) or by fitting it to distributions evaluated for a set of flow fields (fitted version). It requires additional transformation between the global coordinate and the principal coordinate.

To determine the effective properties of the composite from Eq. (2), besides the second and the fourth-order orientation tenors, scalar constants [B.sub.1]-[B.sub.5] also have to be calculated. These constants are related to the components of unidirectional composite stiffness tensor CU as follows [8]:

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (9)

During this study, unidirectional composite effective properties were determined by using the finite element based homogenization in the same way as for establishing the properties of RVE presented in Fig. 1. The effective stiffness tensor of the misaligned composite is evaluated by considering the average second-order orientation tensor corresponding to the created RVE:

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (10)

3.3. Two step homogenization

Another approach that allows to consider the spatial distribution of the particles presented in Fig. 1 is the two-step homogenization. Inclusions are divided into different families characterized by different orientation vector similarly as during the preparation of the RVE geometry. In the first step, the stiffness tensors of perfectly aligned composite corresponding to each particle family are computed. In this case, the properties of unidirectional composite determined by the finite element based homogenization are transformed in accordance with the spatial orientation of a particular particle family. At this step the stiffness tensors are evaluated individually for each family of particles. In the second step, stiffness tensors determined in the first step are aggregated by assuming Voigt homogenization model [15]. The two step homogenization approach was proposed with application of mean-filed homogenization methods presented in works [7, 15].

4. Analysis results

The geometry has been divided on a regular mesh of cube shaped finite elements creating discrete system of approximately 3 million degrees of freedom (Fig. 4). The properties of the composite constituents are collected in Table 1. Moreover the stress-strain curve representing matrix material elastic-plastic behavior is shown in Fig. 5.

[FIGURE 4 OMITTED]

The results of the analyses carried out by using different approaches are collected in Table 2. Additionally, Table 3 shows percent relative error between material parameters determined by numerical methods [E.sup.NUM] and experimental data [E.sup.EXP] defined as follows:

[[chi].sup.E] = [absolute value of ([E.sup.EXP] - [E.sup.NUM])]/[E.sup.NUM] x 100% (11)

The investigation of the composite behavior after plasticizing of matrix material is conducted by enforcing uniaxial strain on the RVE presented in Fig. 2. Three analyses, for different strains, are performed: [[[epsilon].sub.11].sup.(1)] = 0.01, [[[epsilon].sub.22].sup.(2)] = 0.01, [[[epsilon].sub.33].sup.(2)] (3) = 0.01.

The results of these analyses are presented in the form of stress-strain curves shown in Fig. 5, additionally curve that represents matrix material behavior is attached. The differences between the curves caused by non-homogenous orientation of the reinforcement can be noticed. Moreover, anisotropic plasticity of metal matrix may have a significant impact on the result. Generally, in the extruded aluminum alloy parts there are differences between yield stress in the extrusion direction and the transverse directions [16]. However, during this research, the plastic behaviour of matrix material is simplified and treated as isotropic so Fig. 5 accounts only for the distribution of particles effects on the material response. In addition micro-fields of equivalent plastic strain (Fig. 6) and maximum principal stress in the extrusion plane (Fig. 7) are presented. In the case of Fig. 7 micro-field is shown in randomly chosen section view. High stress values exceeding even the ultimate stress of the reinforcement material can be noticed, however this phenomenon occurs only locally. It indicates the areas of probable damage or crack initiation. During this study material failure is not considered, it should be investigated in the further, detailed analysis.

[FIGURE 5 OMITTED]

[FIGURE 6 OMITTED]

[FIGURE 7 OMITTED]

The distribution of probability density of maximum principal stress values in the reinforcement and matrix phases in case of prescribed uniaxial strain [[[epsilon].sub.11].sup.(1)]=0.01 is presented in Fig. 8.

[FIGURE 8 OMITTED]

5. Conclusions

This work presents methodology of determining effective material properties of particle reinforced composites with non-homogenous distribution of orientation of the particles. Three different approaches are presented: homogenization based on analysis of RVE that reflects simplified material microstructure, orientation averaging procedure and two step homogenization method. All presented methods give acceptable results when compared with the experimental data. The first method needs complex geometry preparation which requires the creation of huge discrete models. Therefore, this method is very expensive from the computational point of view. The orientation averaging procedure requires the determination of the effective properties of composite with perfectly aligned inclusions and the second-order orientation tensor. Nevertheless, it also requires an application of closure approximation to compute the fourth-order orientation tensor. The third method, based on two step homogenization, involves determining effective properties of crated sub domains separately in the first step and homogenization of the sub domains in the second step. From the numerical point of view, the orientation averaging and the two step homogenization procedures are more complex than the first method, but on the other hand they are fast and flexible. For example, different orientation distributions can be analyzed by considering the same, previously determined unidirectional material properties. Neglecting the consideration of the actual orientation distribution of the particles and considering the material as orthotropic (unidirectional composite) can lead to unacceptable errors in determining the effective material properties. In particular, the biggest error, amounting to 11.4%, is connected with overestimation of young modulus in the extrusion direction. Although the investigation of composite behavior after plasticizing of matrix material is conducted, improvements-involving the consideration of anisotropic plasticity of matrix material and the damage should be considered in further work.

http://dx.doi.org/10.5755/j01.mech.2L2.10276

Acknowledgement

The results presented in the paper are partially financed from BKM-504/RMT-4/2014.

References

[1.] Chawla, N.; Shen, Y-L. 2001. Mechanical behavior of particle reinforced metal matrix composites, Advanced Engineering Materials 3(6): 357-370. http://dx.doi.org/10.1002/1527-2648(200106)3:6<357: AID-ADEM357>3.0.CO;2-I.

[2.] Ogierman, W.; Kokot, G. 2014. Particle shape influence on elastic-plastic behavior of particle-reinforced composites, Archives of Material Science and Engineering 67(2): 70-76.

[3.] Ramesh, C.S.; Hirianiach, A.; Harishanad, K.S.; Noronha, N.P. 2012. A review on hot extrusion of metal matrix composites (MMC'S), International Journal of Engineering and Science 1(10): 30-35.

[4.] Adamiak, M. 2012. The effect of TiAl and [Ti.sub.3]Al reinforcement on microstructure changes and properties of aluminum matrix composites, Archives of Materials Science and Engineering 58(2): 55-79.

[5.] Ganesh, V.V.; Chawla, N. 2005. Effect of particle orientation anisotropy on the tensile behaviour of metal matrix composites: experiments and microstructure-based simulation, Materials Science and Engineering A, 391: 342-353. http://dx.doi.org/10.1016/j.msea.2004.09.017.

[6.] Jeong, H.; Hsu. D.K.; Shannon, R.E.; Liaw, P.K. 1991. Effect of particle orientation on the elastic anisotropy pf Al/SiC Metal Matrix Composites, Review of Progress in Quantitive Nondestructive Evaluation, 10b: 1461-1468.

[7.] Doghri, I.; Tinel, L. 2005. Micromechanical modeling and computation of elasto-plastic materials reinforced with distributed-orientation fibers, International Journal of Plasticity, 21(10): 1919-1940. http://dx.doi.org/10.1016/jijplas.2004.09.003.

[8.] Advani, S.G.; Tucker III, C.L. 1987. The use of tensors to describe and predict fibre orientation in short fibre composites, Journal of Rheology 31(8): 751-784. http://dx.doi.org/10.1122/1.549945.

[9.] Jeong, H.; Hsu. D.K.; Shannon, R.E.; Liaw, P.K. 1990, Elastic moduli of silicon carbide particulate reinforced aluminum metal matrix composites, Review of Progress in Quantitive Nondestructive Evaluation 9: 1395-1402. http://dx.doi.org/10.1007/978-1-4684-5772-8_179.

[10.] Makowski, P.; John, A.; Kus W.; Kokot, G. 2013. Multiscale modeling of the simplified trabecular bone structure, Proceedings of 18th International Conference "Mechanika 2013": 156-161.

[11.] Bohm, H.J. 2004. Mechanics of Microstructured Materials, Springer-Verlag, 306p. http://dx.doi.org/10.1007/978-3-7091-2776-6.

[12.] Dray, D.; Gilormini, P.; Regnier, G. 2007. Comparison of several closure approximations for evaluating the thermoelastic properties of an injection molded short-fiber composite, Composites Science and Technology, 67: 1601-1610. http://dx.doi.org/10.1016/j.compscitech.2006.07.008.

[13.] Agboola, B.O.; Jack, D.A.; Montgomery-Smith, S. 2012. Effectives of recent fiber-interaction diffusion models for orientation and the part stiffness predictions in injection molded short-fiber reinforced composites, Composites: Part A, 43: 1959-1970. http://dx.doi.org/10.1016/j.compositesa.2012.06.015.

[14.] Cintra, J.S.; Tucker III, C.L. 1995. Orthotropic closure approximations for flow-induced fiber orientation, Journal of Rheology 39(6): 207-227. http://dx.doi.org/10.1122/1.550630.

[15.] Pierard, O.; Friebel, C.; Doghri, I. 2004, Mean-field homogenization of multi-phase thermo-elastic composites: a general framework and its validation, Composites Science and Technology 64: 1587-1603. http://dx.doi.org/10.1016/j.compscitech.2003.11.009.

[16.] Meunier, J. 1986. Influence of Hydrogen on the Ductility of 7091 and 7090 PM Aluminum Alloys, Rapidly solidified powder aluminum alloys: American Society of Testing and Materials: 260-280.

W. Ogierman *, G. Kokot **

* Silesian University of Technology, ul. Konarskiego 18A, 44-100 Gliwice, Poland, E-mail: witold.ogierman@polsl.pl

** Silesian University of Technology, ul. Konarskiego 18A, 44-100 Gliwice, Poland, E-mail: grzegorz.kokot@polsl.pl

Received March 10, 2015

Accepted April 02, 2015

Particle-reinforced metal matrix composites have found application in many areas of engineering practice. They usually provide higher strength, stiffness and weight savings in comparison with conventional metal alloys. Moreover, this group of materials is attractive due to their cost-effectiveness [1]. Estimation of elastic-plastic response in particle-reinforced composites is a complex problem depending on variety of factors such as particle size, shape, distribution or orientation [1, 2]. In this paper, special attention is put into consideration of material anisotropy caused by manufacturing process. One of the most popular ways of manufacturing particle-reinforced composites is through an extrusion. Extrusion is a process connected with creating objects with fixed cross section. It allows to manufacture complex cross sections with brittle materials that in turn result in parts with excellent surface finish [3]. Because extrusion is classified as secondary processing method, it is preceded by one of primary processing methods such as powder metallurgy [3, 4]. In case of application of powder metallurgy, raw composite constituents in the form of powders are mixed, milled, pressed into compacted powder and finally extruded [4]. After extrusion, generally a significant degree of orientation of the reinforcement particles is expected along the extrusion axis. However, the degree of mechanical property anisotropy is related to the volume fraction of particles. In particular, mechanical property anisotropy increases with increasing volume fraction of particles due to the reduction in mean free path between the particles [5]. Therefore, during this study, composite with 0.3 volume fraction of the reinforcement is taken into consideration. In this case, anisotropy of mechanical properties plays a significant role in overall material performance. During this research, spatial distribution of the particles, measured experimenttally, is taken into account by assuming results presented in work [6]. The three dimensional representative volume element (RVE) geometry that represents the material microstructure is created by using Digimat-FE software. The RVE is a statistical representation of material properties. It should contain enough information to describe the behavior of considered composite. The analysis of the RVE is conducted by the finite element method, in particular commercial MSC Marc solver is applied. In addition, different approaches based on the two step homogenization method [7] and the orientation averaging procedure [8] are proposed. Results obtained numerically by using different approaches are presented, compared and related to experimental results that can be found in work [9].

2. Determination of the RVE geometry

The RVE geometry is created by taking into account the spatial distribution of the particles measured experimentally. In particular, results presented in work [6] are considered. In the analyzed case, the shape of the particles is simplified and modeled as ellipsoids with constant size and aspect ratio of 2.68. The histogram that represents the probability distribution of the angle between the particle axis and the extrusion axis is presented in Fig. 1. To create the RVE geometry eight families of particles with angles and probability density corresponding to this histogram were set up. The created RVE that contains 250 particles is presented in Fig. 2, each color indicating different family of the particles, X is the axis of the extrusion. Considered RVE is a rectangular cuboid with the dimensions 500x250x500 pm. The orientation of the particles in the extrusion plane YZ is usually random. In the other two symmetry planes distribution shows similar trend that is in accordance with the histogram presented in Fig. 1 [6].

[FIGURE 1 OMITTED]

[FIGURE 2 OMITTED]

3. Determination of effective anisotropic properties

3.1. Homogenization based on finite element analysis of the RVE

To calculate the effective elasticity tensors of heterogeneous materials, the usage of homogenization procedure is essential. The homogenization procedure involves replacing the heterogeneous material with an equivalent homogeneous material. Calculating the equivalent material properties requires solving six RVE boundary value problems (BVP) in three dimensional case [2, 10]. For each BVP a prescribed strain is applied in accordance with Eq. (1) (a superscript j = 1-6 indicates the number of analysis, I = 1-6).

[[epsilon].sup.(j).sub.i] = [[delta].sup.ij] (1)

In addition, periodic boundary conditions are introduced [11]. After solving six BVPs, both the stresses Eq. (2) and strains Eq. (3) are averaged in post-processing stage of the analysis.

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (2)

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (3)

where <[[sigma].sub.ij]> is average stress, <[[epsilon].sub.ij]> is average strain, [[sigma].sub.ij] is stress in the RVE, [[epsilon].sub.ij] is strain in the RVE and [V.sub.RVE] is volume of the RVE.

The relation between stress and strain tensors is expressed by:

<[[sigma].sub.ij]> = C < [[epsilon].sub.ij] > (4)

where C is elasticity tensor.

The presented methodology is applied to the estimation of effective properties of the material which is represented by the RVE presented in Fig. 2, as well as for material with inclusions perfectly aligned with the extrusion axis.

3.2. Orientation averaging

Another approach that deals with determining the effective properties of composite materials with non-homogenous orientation of the reinforcement is orientation averaging. The orientation averaging procedure is based on equation proposed by Advani and Tucker [8]:

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (5)

where [a.sub.ij], [a.sub.ijlkl] are second and fourth-order orientation tensors and [B.sub.1]-[B.sub.5] are scalar constants related to the components of stiffness tensor of unidirectional composite.

A drawback of this approach is that the fourth-order tensor [a.sub.ijkl] is required to calculate the effective stiffness. In practice, very frequently only the second order orientation tensor is known. The graphical representation of the second-order orientation tensor is presented in Fig. 3 where [[lambda].sub.i] and [n.sub.i] are eigenvalues and eigenvectors.

[FIGURE 3 OMITTED]

The second-order orientation tensor has the following properties:

[a.sub.ii] = 1, (6)

[a.sub.ij] = [a.sub.ji]. (7)

Therefore, the second-order orientation tensor has five independent components. To estimate the fourth-order orientation tensor, closure approximations are commonly considered where the fourth-order tensor components are calculated from the components of the second-order tensor. The closure that provide the most accurate results in comparison with experimentally measured fourth-order tensors is the orthotropic closure proposed by Cintra and Tucker [12, 13] in their work [14]. The orthotropic closures are based on the assumption that the principal axes of the approximated fourth order tensors are in alignment with the principal axes of the second order tensor [14]. The definition of orthotropic closure approximation reduces the choice to three scalar functions f such as [a.sub.iiii] =[f.sub.i]([a.sub.1], [a.sub.2]). Cintra and Tucker used in their work second-degree polynomials:

[a.sub.iii] = [T.sup.1.sub.i1] + [T.sup.2.sub.i2][a.sub.(1)] + [T.sup.3.sub.i3][a.sub.(1)] + [T.sup.4.sub.i4][a.sub.(2)] + [T.sup.5.sub.i5][a.sub.(2)] + [T.sup.6.sub.i6][a.sub.(1)][a.sub.(2)], (8)

where there is no sum on i, [a.sub.(1)] and [a.sub.(2)] are the first and the second eigenvalue of the second-order orientation tensor, [T.sub.m.sup.i] is a matrix of coefficients which can be determined by using specific orientation distributions (smooth version) or by fitting it to distributions evaluated for a set of flow fields (fitted version). It requires additional transformation between the global coordinate and the principal coordinate.

To determine the effective properties of the composite from Eq. (2), besides the second and the fourth-order orientation tenors, scalar constants [B.sub.1]-[B.sub.5] also have to be calculated. These constants are related to the components of unidirectional composite stiffness tensor CU as follows [8]:

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (9)

During this study, unidirectional composite effective properties were determined by using the finite element based homogenization in the same way as for establishing the properties of RVE presented in Fig. 1. The effective stiffness tensor of the misaligned composite is evaluated by considering the average second-order orientation tensor corresponding to the created RVE:

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (10)

3.3. Two step homogenization

Another approach that allows to consider the spatial distribution of the particles presented in Fig. 1 is the two-step homogenization. Inclusions are divided into different families characterized by different orientation vector similarly as during the preparation of the RVE geometry. In the first step, the stiffness tensors of perfectly aligned composite corresponding to each particle family are computed. In this case, the properties of unidirectional composite determined by the finite element based homogenization are transformed in accordance with the spatial orientation of a particular particle family. At this step the stiffness tensors are evaluated individually for each family of particles. In the second step, stiffness tensors determined in the first step are aggregated by assuming Voigt homogenization model [15]. The two step homogenization approach was proposed with application of mean-filed homogenization methods presented in works [7, 15].

4. Analysis results

The geometry has been divided on a regular mesh of cube shaped finite elements creating discrete system of approximately 3 million degrees of freedom (Fig. 4). The properties of the composite constituents are collected in Table 1. Moreover the stress-strain curve representing matrix material elastic-plastic behavior is shown in Fig. 5.

[FIGURE 4 OMITTED]

The results of the analyses carried out by using different approaches are collected in Table 2. Additionally, Table 3 shows percent relative error between material parameters determined by numerical methods [E.sup.NUM] and experimental data [E.sup.EXP] defined as follows:

[[chi].sup.E] = [absolute value of ([E.sup.EXP] - [E.sup.NUM])]/[E.sup.NUM] x 100% (11)

The investigation of the composite behavior after plasticizing of matrix material is conducted by enforcing uniaxial strain on the RVE presented in Fig. 2. Three analyses, for different strains, are performed: [[[epsilon].sub.11].sup.(1)] = 0.01, [[[epsilon].sub.22].sup.(2)] = 0.01, [[[epsilon].sub.33].sup.(2)] (3) = 0.01.

The results of these analyses are presented in the form of stress-strain curves shown in Fig. 5, additionally curve that represents matrix material behavior is attached. The differences between the curves caused by non-homogenous orientation of the reinforcement can be noticed. Moreover, anisotropic plasticity of metal matrix may have a significant impact on the result. Generally, in the extruded aluminum alloy parts there are differences between yield stress in the extrusion direction and the transverse directions [16]. However, during this research, the plastic behaviour of matrix material is simplified and treated as isotropic so Fig. 5 accounts only for the distribution of particles effects on the material response. In addition micro-fields of equivalent plastic strain (Fig. 6) and maximum principal stress in the extrusion plane (Fig. 7) are presented. In the case of Fig. 7 micro-field is shown in randomly chosen section view. High stress values exceeding even the ultimate stress of the reinforcement material can be noticed, however this phenomenon occurs only locally. It indicates the areas of probable damage or crack initiation. During this study material failure is not considered, it should be investigated in the further, detailed analysis.

[FIGURE 5 OMITTED]

[FIGURE 6 OMITTED]

[FIGURE 7 OMITTED]

The distribution of probability density of maximum principal stress values in the reinforcement and matrix phases in case of prescribed uniaxial strain [[[epsilon].sub.11].sup.(1)]=0.01 is presented in Fig. 8.

[FIGURE 8 OMITTED]

5. Conclusions

This work presents methodology of determining effective material properties of particle reinforced composites with non-homogenous distribution of orientation of the particles. Three different approaches are presented: homogenization based on analysis of RVE that reflects simplified material microstructure, orientation averaging procedure and two step homogenization method. All presented methods give acceptable results when compared with the experimental data. The first method needs complex geometry preparation which requires the creation of huge discrete models. Therefore, this method is very expensive from the computational point of view. The orientation averaging procedure requires the determination of the effective properties of composite with perfectly aligned inclusions and the second-order orientation tensor. Nevertheless, it also requires an application of closure approximation to compute the fourth-order orientation tensor. The third method, based on two step homogenization, involves determining effective properties of crated sub domains separately in the first step and homogenization of the sub domains in the second step. From the numerical point of view, the orientation averaging and the two step homogenization procedures are more complex than the first method, but on the other hand they are fast and flexible. For example, different orientation distributions can be analyzed by considering the same, previously determined unidirectional material properties. Neglecting the consideration of the actual orientation distribution of the particles and considering the material as orthotropic (unidirectional composite) can lead to unacceptable errors in determining the effective material properties. In particular, the biggest error, amounting to 11.4%, is connected with overestimation of young modulus in the extrusion direction. Although the investigation of composite behavior after plasticizing of matrix material is conducted, improvements-involving the consideration of anisotropic plasticity of matrix material and the damage should be considered in further work.

http://dx.doi.org/10.5755/j01.mech.2L2.10276

Acknowledgement

The results presented in the paper are partially financed from BKM-504/RMT-4/2014.

References

[1.] Chawla, N.; Shen, Y-L. 2001. Mechanical behavior of particle reinforced metal matrix composites, Advanced Engineering Materials 3(6): 357-370. http://dx.doi.org/10.1002/1527-2648(200106)3:6<357: AID-ADEM357>3.0.CO;2-I.

[2.] Ogierman, W.; Kokot, G. 2014. Particle shape influence on elastic-plastic behavior of particle-reinforced composites, Archives of Material Science and Engineering 67(2): 70-76.

[3.] Ramesh, C.S.; Hirianiach, A.; Harishanad, K.S.; Noronha, N.P. 2012. A review on hot extrusion of metal matrix composites (MMC'S), International Journal of Engineering and Science 1(10): 30-35.

[4.] Adamiak, M. 2012. The effect of TiAl and [Ti.sub.3]Al reinforcement on microstructure changes and properties of aluminum matrix composites, Archives of Materials Science and Engineering 58(2): 55-79.

[5.] Ganesh, V.V.; Chawla, N. 2005. Effect of particle orientation anisotropy on the tensile behaviour of metal matrix composites: experiments and microstructure-based simulation, Materials Science and Engineering A, 391: 342-353. http://dx.doi.org/10.1016/j.msea.2004.09.017.

[6.] Jeong, H.; Hsu. D.K.; Shannon, R.E.; Liaw, P.K. 1991. Effect of particle orientation on the elastic anisotropy pf Al/SiC Metal Matrix Composites, Review of Progress in Quantitive Nondestructive Evaluation, 10b: 1461-1468.

[7.] Doghri, I.; Tinel, L. 2005. Micromechanical modeling and computation of elasto-plastic materials reinforced with distributed-orientation fibers, International Journal of Plasticity, 21(10): 1919-1940. http://dx.doi.org/10.1016/jijplas.2004.09.003.

[8.] Advani, S.G.; Tucker III, C.L. 1987. The use of tensors to describe and predict fibre orientation in short fibre composites, Journal of Rheology 31(8): 751-784. http://dx.doi.org/10.1122/1.549945.

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W. Ogierman *, G. Kokot **

* Silesian University of Technology, ul. Konarskiego 18A, 44-100 Gliwice, Poland, E-mail: witold.ogierman@polsl.pl

** Silesian University of Technology, ul. Konarskiego 18A, 44-100 Gliwice, Poland, E-mail: grzegorz.kokot@polsl.pl

Received March 10, 2015

Accepted April 02, 2015

Table 1 Properties of composite constituents Matrix Particles Young modulus, GPa 73 410 Poisson ratio 0.34 0.19 Volume fraction 0.7 0.3 Aspect ratio -- 2.68 Table 2 Effective elastic material properties: E-Young modulus, G- shear modulus Material parameters, GPa E11 E22 E33 Experiment [9] 124.0 112.3 120.4 Microstructure based 128.30 118.80 121.75 Orientation averaging 123.78 119.15 121.02 Two step homogenization 126.76 116.17 119.06 Unidirectional composite 138.13 115.57 116.45 Material parameters, GPa G12 G13 G23 Experiment [9] 44.6 47.6 45.3 Microstructure based 46.31 46.98 45.67 Orientation averaging 45.25 45.19 45.09 Two step homogenization 46.21 46.72 45.19 Unidirectional composite 45.27 44.80 42.63 Table 3 Percent relative error between material parameters evaluated by numerical methods and experimental data [[chi] [[chi] [[chi] [[chi] .sup. .sup. .sup. .sup. E11] E22] E33] E12] Microstructure based 3.47 5.79 1.12 3.84 Orientation averaging 2.23 3.45 1.11 3.61 Two step homogenization 1.75 3.94 1.31 3.82 Unidirectional composite 11.4 2.91 3.28 1.49 [[chi] [[chi] Average .sup. .sup. percentage E13] E23] error Microstructure based 1.3 0.82 2.72 Orientation averaging 3.19 0.07 2.28 Two step homogenization 1.85 0.71 2.3 Unidirectional composite 5.87 5.89 5.14

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Author: | Ogierman, W.; Kokot, G. |
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Publication: | Mechanika |

Date: | Mar 1, 2015 |

Words: | 3026 |

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