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record xmlns http:www.loc.govMARC21slim xmlns:xsi http:www.w3.org2001XMLSchemainstance xsi:schemaLocation http:www.loc.govstandardsmarcxmlschemaMARC21slim.xsd leader nam 2200385Ka 4500 controlfield tag 001 002029635 005 20090918114352.0 007 cr mnuuuuuu 008 090918s2009 flu s 000 0 eng d datafield ind1 8 ind2 024 subfield code a E14SFE0002951 035 (OCoLC)437009317 040 FHM c FHM 049 FHMM 090 TJ145 (Online) 1 100 Garapati, Sri Harsha. 0 245 Analysis of single fiber pushout test of fiber reinforced composite with a nonhomogeneous interphase h [electronic resource] / by Sri Harsha Garapati. 260 [Tampa, Fla] : b University of South Florida, 2009. 500 Title from PDF of title page. Document formatted into pages; contains 69 pages. 502 Thesis (M.S.M.E.)University of South Florida, 2009. 504 Includes bibliographical references. 516 Text (Electronic thesis) in PDF format. 3 520 ABSTRACT: Fiber pushout test models are developed for a fibermatrixcomposite with a nonhomogeneous interphase. Using design of experiments, the effects of geometry, loading and material parameters on critical parameters of the pushout test such as the loaddisplacement curve and maximum interfacial shear and normal stresses are studied. The sensitivity analysis shows that initial load displacement curve is dependent only on the indenter type and not on parameters such as fiber volume fraction, interphase type, thickness of interphase, and boundary conditions. In contrast, interfacial shear stresses are not sensitive to indenter type, while the interfacial radial stresses are mainly sensitive to fiber volume fraction and the boundary conditions. 538 Mode of access: World Wide Web. System requirements: World Wide Web browser and PDF reader. 590 Advisor: Autar Kaw, Ph.D. 653 Pushout test Nonhomogeneous interphase Interfacial stresses ANSYS Design of experiments 690 Dissertations, Academic z USF x Mechanical Engineering Masters. 773 t USF Electronic Theses and Dissertations. 4 856 u http://digital.lib.usf.edu/?e14.2951 PAGE 1 Analysis of Single Fiber Pushout Test of Fiber Reinforced Composite with a Nonhomogeneous Interphase by Sri Harsha Garapati A thesis submitted in partial fulfillment of the requirements for the degree of Master of Science in Mechanical Engineering Department of Mechanical Engineering College of Engineering University of South Florida Major Professor: Autar Kaw, Ph.D. Glen Besterfield, Ph.D. Craig Lusk, Ph.D. Date of Approval: March 24, 2009 Keywords: Pushout Test, Nonhomogeneous Interphase, Interfacial Stresses, ANSYS, Design of Experiments, Composite Copyright 2009, Sri Harsha Garapati 1 PAGE 2 2 DEDICATION This thesis dedicated to my parents, w ho took care with all th eir love, supported and believed in me. To my professor Dr. Autar K. Kaw, who guided, instructed and inspired me in the graduate school. PAGE 3 i ACKNOWLEDGEMENTS I wish to acknowledge the gracious suppor t of many people for their contributions towards this work both directly and indirect ly. Firstly, I thank my advisor Dr. Autar Kaw who patiently guided me through all phases of th is work. He is a true role model, and a best professor I have ever seen. I am deeply indebted to him for financial support, and for the academic resources he provided. The time a nd effort of Dr. Glen Besterfield and Dr. Craig Lusk as committee members is greatly appreciated. I would like to thank my parents, Nagabhushanam and Padmavathi for their support, suggestions and invaluable encourag ement that have always made me a better man and have indirectly prepared me to tack le challenges that I came across. Without my parents support and encour agement, I never would have made it this far. Additionally, I would like to thank all my friends, especially from the research group Luke Snyder and John Daly for having always motivated and accompanied me throughout the challenges of research. Without their help, this thesis would have been much more difficult. This work has been supported in part through the University of South Florida. PAGE 4 TABLE OF CONTENTS TABLE OF CONTENTS .....................................................................................................i LIST OF TABLES ..............................................................................................................v LIST OF FIGURES ...........................................................................................................vi LIST OF EQUATIONS ......................................................................................................x ABSTRACT .................................................................................................................xiv CHAPTER 1 LITERATURE REVIEW...........................................................................1 1.1 Introduction .................................................................................................1 1.2 Analytical Modeling ...................................................................................3 1.2.1 Interphase Layer Model ..................................................................3 1.2.2 Cohesive Zone Model.....................................................................4 1.2.3 Spring Layer Model ........................................................................4 1.3 Shear Lag Analysis .....................................................................................4 1.4 Finite Element Modeling ............................................................................6 1.4.1 3D finite Element Model ...............................................................6 1.4.2 Axisymmetric Model ......................................................................6 1.4.3 Axisymmetric Model with Friction Elements .................................7 i PAGE 5 1.5 Boundary Element Method (BEM) .............................................................9 1.6 Functionally Graded (FG) Coating ...........................................................10 1.7 Nonhomogeneous Interphase ....................................................................10 1.8 Comparison Between Multi and Single Fiber Pushout Test .....................11 1.9 Present Work .............................................................................................12 CHAPTER 2 FORMULATION .....................................................................................14 2.1 Finite Element Modeling ..........................................................................14 2.1.1 Geometry .......................................................................................14 2.2 Meshing the Geometry ..............................................................................15 2.2.1 PLANE182 ....................................................................................16 2.3 Modeling the Bonded Contact in the Composite ......................................17 2.4 Properties ..................................................................................................18 2.4.1 Fiber and Matrix ...........................................................................18 2.4.2 Interphase ......................................................................................19 2.4.3 Composite .....................................................................................21 2.4.3.1 Axial Properties .............................................................21 2.4.3.2 Tangential Properties .....................................................22 2.4.3.3 Radial Properties ............................................................24 2.5 Continuity Conditions ...............................................................................25 2.5.1 FiberInterphase ............................................................................25 2.5.2 Sub Layers of Interphase ..............................................................26 ii PAGE 6 2.5.3 InterphaseMatrix ..........................................................................27 2.5.4 MatrixComposite .........................................................................28 2.6 Boundary Conditions ................................................................................29 2.6.1 Boundary Condition 1 (BC1) .....................................................29 2.6.2 Boundary Condition2 (BC2)......................................................30 2.7 Loading .....................................................................................................31 2.7.1 Spherical Indenter .........................................................................31 2.7.1.1 Radius of Contact ...........................................................32 2.7.2 Uniform Pressure Loading ............................................................34 2.7.3 Flat Indenter ..................................................................................35 2.8 Factors for Sensitivity Analyses ...............................................................36 2.8.1 Type of Indenter ............................................................................36 2.8.2 Fiber Volume Fraction ..................................................................36 2.8.3 Thickness of Interphase to Ra dius of Fiber Ratio (TIRFR) ..........37 2.8.4 Type of Interphase ........................................................................37 2.8.5 Boundary Conditions ....................................................................38 2.9 Responses for Sensitivity Analyses ..........................................................38 2.9.1 Load to Contact Depth Ratio (LCDR) ..........................................38 2.9.2 Normalized Maximum Interfacial Radial Stress (NMIRS) ..........38 2.9.3 Normalized Maximum Interfacial Shear Stress (NMISS) ............39 2.10 Modeling the Contact between the Fiber and the Indenter .......................40 CHAPTER 3 VALIDATION OF MODEL ....................................................................41 iii PAGE 7 3.1 Spherical Indenter .....................................................................................41 3.1.1 Contact Between the Indenter and Fiber .......................................41 3.1.2 Bonded Contact Betw een the Interfaces .......................................43 3.2 Uniform Pressure Indenter ........................................................................44 3.2.1 Contact Between the Indenter and Fiber .......................................44 3.2.2 Bonded Contact Betw een the Interfaces .......................................46 3.3 Flat Indenter ..............................................................................................46 3.3.1 Contact Between the Indenter and Fiber .......................................46 3.3.2 Bonded Contact Betw een the Interfaces .......................................48 3.4 Validation with Huang SLA and Finite Element Model ..........................48 3.5 Validation Using In terfacial Stresses ........................................................50 3.5.1 Validation Using Interf acial Radial Stress ....................................50 3.5.2 Validation Using Interfacial Shear Stress .....................................52 CHAPTER 4 RESULTS AND CONCLUSIONS ..........................................................55 4.1 Responses for the Sensitivity Analyses ....................................................57 4.1.1 Load to Contact Depth Ratio (LCDR) ..........................................57 4.1.2 Normalized Maximum Interfacial Radial Stress (NMIRS) ..........58 4.1.3 Normalized Maximum Interfacial Shear Stress (NMISS) ............61 4.2 Conclusions ...............................................................................................64 REFERENCES .................................................................................................................66 iv PAGE 8 LIST OF TABLES Table 1 Youngs Modulus and Poisson's Ratio of Fiber and Matrix ........................19 Table 2 Values of Differe nt Levels of the Factors ....................................................56 Table 3 Percentage Cont ribution of Factors to Load to Contact Depth Ratio..........58 Table 4 Percentage Contri bution of Factors to NMIRS ............................................61 Table 5 Percentage Contribution of Factors to Normalized Interfacial Maximum Shear Stress ................................................................................64 v PAGE 9 LIST OF FIGURES Figure 1 Schematic Diagram of a Pushout Test of a Composite. .................................2 Figure 2 Schematic Diagram of the FiberInterphaseMatrixComposite Model ...........................................................................................................15 Figure 3 Meshed Model of Compos ite with Nonhomogeneous Interphase ...............16 Figure 4 Structure of PLANE182 ...............................................................................17 Figure 5 Contact and Target Elements at the Interfaces ............................................18 Figure 6 Composite with BC1 ..................................................................................30 Figure 7 Schematic Diagram of Spherical Indenter Loading .....................................32 Figure 8 Contact between the Fiber and the Indenter ................................................33 Figure 9 Schematic Diagram Illust rating Uniform Pressure Loading ........................35 Figure 10 Schematic Diagram of Flat Indenter Loading ..............................................36 Figure 11 Finite Element Model of Composite with Spherical Indenter.....................40 vi PAGE 10 Figure 12 Typical Distribution of Normalized Axial Stress Along the Normalized Radial Distance from the Center of the Fiber for Spherical Indenter ........................................................................................42 Figure 13 Typical Distribution of Norm alized Axial Displacement Along the Normalized Radial Distance from the Center of the Fiber for Spherical Indenter ........................................................................................42 Figure 14 Typical Distribution of Normalized Axial Stress Along the Normalized Radial Distance from the Center of the Fiber for Uniform Pressure Indenter ...........................................................................44 Figure 15 Typical Distribution of Normalized Axial Displacement Along the Normalized Radial Distance from the Center of the Fiber for Uniform Pressure Indenter ...........................................................................45 Figure 16 Typical Distribution of Normalized Axial Stress Along the Normalized Radial Distance from th e Center of the Fiber for Flat Indenter ........................................................................................................47 Figure 17 Typical Distribution of Normalized Axial Displacement Along the Normalized Radial Distance from th e Center of the Fiber for Flat Indenter ........................................................................................................47 Figure 18 Typical Distribution of Norma lized Interfacial Radial Stress Along the Normalized Length of the Fiber .............................................................51 vii PAGE 11 Figure 19 Typical Distribution of Norma lized Interfacial Radial Displacement Along the Normalized Length of the Fiber ..................................................52 Figure 20 Typical Distribution of Norm alized Interfacial Shear Stress Along the Normalized Length of the Fiber .............................................................53 Figure 21 Typical Distribution of Norma lized Interfacial Axial Displacement Along the Normalized Length of the Fiber ..................................................54 Figure 22 Normalized LCDR as a Function of Type of Indenter. ...............................57 Figure 23 Normalized Maximum Interfacial Radial Stress as a Function of Fiber Volume Fraction for Uniform Pressure Indenter, Linear Type of Interphase, and TIRFR=1/20. ..................................................................59 Figure 24 Normalized Maximum Interfacial Radial Stress as a Function of Fiber Volume Fraction for Spherica l Indenter Loading, Linear Type of Interphase, and BC1 ...............................................................................60 Figure 25 Normalized Maximum Interfacial Radial Stress as a Function of Fiber Volume Fraction for Flat Indenter Loading, TIRFR=1/20, and BC2. ............................................................................................................60 Figure 26 Normalized Maximum Interfacial Shear Stress as a Function of Fiber Volume Fraction for Uniform Indent er, Linear Type of Interphase, and TIRFR=1/20..........................................................................................62 viii PAGE 12 Figure 27 Normalized Maximum Interfacial Shear Stress as a Function of Fiber Volume Fraction for Spherical Inde nter Loading, Linear Type of Interphase, and BC1...................................................................................62 Figure 28 Normalized Maximum Interfacial Shear Stress as a Function of Fiber Volume Fraction for Flat Indent er Loading, TIRFR=1/20, and BC2. ........63 ix PAGE 13 LIST OF EQUATIONS Equation 1 Force Balance Equation to Calculate the Friction Stress at the Interface [1]. ...................................................................................................5 Equation 2 Exponential Variation of Young's Modulus along the Radial Thickness of Interphase ...............................................................................19 Equation 3 Exponential Variation of Po isson's Ratio along the Radial Thickness of Interphase .................................................................................................19 Equation 4 Linear Variation of Y oung's Modulus along the Thickness of the Interphase .....................................................................................................20 Equation 5 Linear Variation of Pois son's Ratio along the Thickness of the Interphase .....................................................................................................20 Equation 6 Poisson's Ratio of the jth layer of Interphase ................................................20 Equation 7 Young's Modulus of the jth Layer of the Interphase.....................................20 Equation 8 Equations for Calculating the Axial Properties of the Composite ...............22 Equation 9 Equations for Calcul ating the Tangential Properties ...................................24 x PAGE 14 Equation 10 Radial Stress Continui ty in FiberInterphase Interface ................................25 Equation 11 Shear Stress Continu ity in FiberInterphase Interface .................................25 Equation 12 Radial Displacement Conti nuity in FiberInterphase Interface ...................25 Equation 13 Axial Displacement Conti nuity in FiberInterphase Interface .....................25 Equation 14 Radial Stress Con tinuity at the Interface of jth and j+1th Sublayer of Interphase .....................................................................................................26 Equation 15 Shear Stress Continuity at the Interface of jth and j+1th Sublayer of Interphase .....................................................................................................26 Equation 16 Radial Displacement Co ntinuity at the Interface of jth and j+1th Sublayer of Interphase .................................................................................26 Equation 17 Axial Displacement Con tinuity at the Interface of jth and j+1th Sublayer of Interphase .................................................................................26 Equation 18 Radial Stress Continui ty at InterphaseMatrix Interface .............................27 Equation 19 Shear Stress Continu ity at InterphaseMatrix Interface ...............................27 Equation 20 Radial Displacement Conti nuity at InterphaseMatrix Interface .................27 Equation 21 Axial Displacement Conti nuity at InterphaseMatrix Interface ...................27 Equation 22 Radial Stress Conti nuity at MatrixComposite Interface .............................28 Equation 23 Shear Stress Continu ity at MatrixComposite Interface ..............................28 xi PAGE 15 Equation 24 Radial Displacement Con tinuity at Matrix Composite Interface ................28 Equation 25 Shear Displacement Conti nuity at MatrixC omposite Interface ..................28 Equation 26 Axisymmetric Condition ..............................................................................29 Equation 27 Matrix Constrained in its Axial Direction at its Bottom End ......................29 Equation 28 Composite Constrained in its Axial Direction at its Bottom End ................29 Equation 29 Radial Stressfree Condition at the Radial Edge of the Composite ..............29 Equation 30 Shear Stressfree Condition at the Radial Edge of the Composite ................30 Equation 31 Radial Displacement Constrained at the Radial Edge of the Matrix ...........30 Equation 32 Axial Displacement Constraine d along the Radial Edge of the Matrix .......30 Equation 33 Pressure Applie d on the Spherical Indenter .................................................31 Equation 34 FischerCripps Equation to Calculate the Contact Radius ...........................33 Equation 35 Uniform Pressure Applied on the Fiber .......................................................34 Equation 36 Fiber Volume Fraction .................................................................................37 Equation 37 Load to Contact Depth Ratio .......................................................................38 Equation 38 Normalized Maximum Radial Stress at the FiberInterphase Interface .......39 Equation 39 Normalized Maximum Shear St ress at the FiberInterphase Interface ........39 xii PAGE 16 Equation 40 Total Load on the Fiber using the Axial Stress Data on the Top of the Fiber .......................................................................................................43 Equation 41 Total Load Applied on the Fiber through Spherical Indenter ......................43 Equation 42 Load Applied on the Fiber through Uniform/Flat indenter .........................45 Equation 43 Loading Condition for Huang Model ..........................................................49 Equation 44 LCDR from Huang's Shear Lag Model .......................................................49 Equation 45 Intermediate Parameters to be Calculated for LCDR using Huang's Model ...........................................................................................................49 Equation 46 Force in Radial Direction from the Interfacial Radial Stress .......................51 Equation 47 Axial Force Applied on the Fi ber from the Interfacial Shear Stress ............53 xiii PAGE 17 Analysis of Single Fiber Pushout Test of Fiber Reinforced Composite with a Nonhomogeneous Interphase Sri Harsha Garapati ABSTRACT Fiber pushout test models are developed for a fibermatrixcomposite with a nonhomogeneous interphase. Using design of experiments, the effects of geometry, loading and material parameters on critical parameters of the pushout test such as the loaddisplacement curve and maximum interfacial shear and normal stresses are studied. The sensitivity analysis shows that initial load displacement curve is dependent only on the indenter type and not on parameters such as fiber volume fraction, interphase type, thickness of interphase, and boundary conditions. In contrast, interfacial shear stresses are not sensitive to indenter type, while the in terfacial radial stresse s are mainly sensitive to fiber volume fraction a nd the boundary conditions. xiv PAGE 18 CHAPTER 1 LITERATURE REVIEW 1.1 Introduction In a fibermatrix composite, the material immediately surrounding the fiber called the interphase can be different from the bulk matrix. The interphase is a very thin layer formed between the fiber and matrix due to chemical reaction between them or may be intentionally introduced to improve the prope rties of composite. Interphase properties have a significant effect on the overall structural integrity of the composite. This importance of the interphase has led rese archers to carry numerous experimental characterizations and micro mechanical analysis of the interphase subjected to different loading conditions [2]. The pushout test is one of the experi mental techniques used for finding the interphase properties where the fiber is pushe d with an indenter (spherical/flat/cubical, etc). The indentation process starts by applyi ng the load and graduall y increasing the load to a maximum value. The displacement of the fiber is continuously measured as the load is increased. Similarly, displacement of the fi ber is recorded during the unloading of the specimen. Now by drawing a loading / unloading curve, the interphase properties can be found [2]. The two important interphase prope rties are coefficient of friction of fibermatrix interphase and the residual radial st ress in the interface. Several methods are implemented to extract these two properties of the interphase. 1 PAGE 19 Figure 1 Schematic Diagram of a Pushout Test of a Composite. The pushout specimen is prepared by slicing the composite normal to fiber direction and is placed on platform with a hole (Figure 1 ). The radius of the hole of the platform is slightly larger than the radius of the fiber in the specime n. An indenter is used to apply load on the fiber. The load applied is gradually increased and simultaneously displacements are noted. Usually the indenter radius is abou t 6090% of the fiber radius [1]. Fiber pushout test is regarded as the mo st important widely used experimental technique because of the rela tive simplicity of preparing the specimen and conducting the experiment. But the pushout process has certain limitations and they include the following. 1. The values obtained for shear strength and frictional shear stress are average values. 2. Fiber may damage during the loading. 3. Indenter failure may also occur. 2 PAGE 20 1.2 Analytical Modeling The above limitations of th e fiber pushout test created a demand to model it either analytically or numerically. Kerans and Part hasarathy [3] developed an analytical model which gives the fiberend displacement for an applied stress. Hsueh [4, 5] showed that by averaging interfacial shear stress and Po issons effect along the sliding length, the predictions are surprisingl y accurate. LaraCurzio an d Ferber [6] developed a methodology to determine the interfacial properti es of brittle matrix composites using the models developed by Kerans and Parthasara thy [3] and Hsueh [4, 5]. LaraCurzio and Ferber [6] also discussed data analyses te chniques by comparing the models developed by Kerans and Parthasarathy [3] and Hsueh [4, 5]. The most difficult part of modeling the pushout test is modeling the interface. There are three methods used for modeling the interface. They are 1. Interphase layers model 2. Cohesive zone model 3. Spring layers model 1.2.1 Interphase Layer Model Interphase layer model considers that interphase is a distinct layer with a specified thickness. This layer is placed between the fibe r and the matrix. Interphase layer model is very complicated as it requires numerous parame ters to completely describe the behavior of the interface. Also the failure of the interface is difficult to ascertain [7]. 3 PAGE 21 1.2.2 Cohesive Zone Model In this model the interface is treated as a separate material with its own constitutive relationship. This model is re latively simpler than the interphase layer modeling. This model uses only energy based criterion [7]. 1.2.3 Spring Layer Model This is the simplest of all the mode ls. The interface is modeled using spring elements with certain stiffness. The spring zone model uses both st ressbased and energybased criteria [7]. 1.3 Shear Lag Analysis Shearlag theory was first proposed for m odeling the pushout test by Shetty [8]. His model predicted the exponential decrease of interfacial shear stress along the fiber length. This result is similar to the ones obtai ned from finite element analysis[9]. His theory also provided a basis for determining co efficient of friction and interfacial residual stress. He also proposed fricti onal stress due to sliding coul d be over estimated if the transverse expansion of fibers is not taken into account. Shearlag theory is widely used for anal ytical based mechanics to evaluate fibermatrix interface properties. Acco rding to this theory, the inte rphase is assumed to be a thin layer surrounding the fiber. It is also a ssumed that this thin layer of interface has a constant stiffness [2]. The pushout forcedisplacement plot from th e test is regressed to a theoretical model for determining the coefficient of fric tion and residual radial stress in the fibermatrix interface. By experimentally performing the pushout the force ( ) required to F 4 PAGE 22 pushout the fibers is found. From the force bala nce equation, the friction stress near the interface can be calculated as. Equation 1 Force Balance Equati on to Calculate the Fricti on Stress at the Interface [1] In the Equation 1 is the fiber radius, fr L is the length of the fiber and rz is the shear stress along the fibermatrix interface [1 ]. But this assumption is only valid when the coefficient of friction is very small or the length of the specimen is very small. This assumption is not valid for all the cases because it assumes that the shear stress is uniform through the length. But actually when the fiber is pushed by the indenter, the fiber is in compression and it expands in the transverse direction due to Poissons effect. As the fiber expands in transverse di rection, it exerts force on the interface which increases the normal stress on the interface and in turn the frictional stress at the interface. If the Poissons effect is not taken into account the sliding frictional stress can be overestimated. Due to Poissons effect, the frictional shear stress is nonlinear in nature along the length of embedded fiber [1]. Some of the important assumptions in SLA are 1. Coulomb friction law is assumed at the interface. 2. Residual radial compression due to thermal coefficients mismatch between the fiber and matrix is assumed [1, 7, 1012]. Using these assumptions the experimental data collected is regressed to find the mechanical properties of the interface. Huang et al. [2] verified the accuracy of analytical solution based on shearlag assumptions by a finite element method. The analytical model failed to capture the values at the top surface due to free edge effects, but in the rzfLrF 2 5 PAGE 23 interior region the finite element results and analytical results are very close to each other. 1.4 Finite Element Modeling 1.4.1 3D finite Element Model Mital and Chamis [13] developed a 3D fi nite element model consisting of nine fibers. All the nine fibers were unidirecti onal and were arranged in threebythree unit cell order. Their finite element model consiste d of an interphase between the fiber and the matrix, and the interphase thickness was ta ken as 6.8% of the fiber diameter. The material properties of the interphase were assumed to be same as the matrix properties except for its shear modulus. Very low shear modulus of the interphase was assumed to linearize the simulation up to pus h through load of the fiber. This procedure was used to predict the fiber push through lo ad at any temperature and helped in determining the average interfacial shear strength. 1.4.2 Axisymmetric Model ShiraziAdl [1416] and Forc ione [15] conducted finite element stress analysis of a pushout test using an axisymmetric finite element model with two concentric cylinders with a common interface. The model was mesh ed with bilinear quadrilateral elements. They studied the effects of material pr operties and boundary conditions on interfacial shear stress. The three cases of material properties they used for their study were 1. Harder material inside 2. Identical materials 3. Softer material inside. 6 PAGE 24 They used four different boundary conditions for their study 1. Outer cylinder is constraine d axially at the bottom 2. Outer cylinder is fixed at the bottom 3. Outer surface area of outer cylinder is constrained radially 4. Outer cylinder is fixed in all directions. They considered both axial compression a nd axial torque loads for this study, and observed that the shear stress at the interface is almost constant for material property of type1 and boundary conditions 3 and 4. For th e same material property type and the boundary conditions 1 and 2, the interfacial shear stress varied along the length and the maximum value is found at the bottom. Interfacial radial stresses for material property of type1 and boundary condition 4 were of ve ry small magnitude and compressive. For boundary conditions 1 and 3, the interfacial radial stress was found to have very large values of tensile stress at the bottom and at the top. 1.4.3 Axisymmetric Model with Friction Elements Yuan et al. [7] modeled the single fi ber pushout test as an axisymmetric cylindrical model. The SiC fiber and titanium matrix were modeled using isoparametric 4noded quadrilateral elements. The interface between the fiber and matrix was modeled using contactfriction and spring elements. Th e interface was modeled using the spring elements because the analyses was carried based on the stress based criterion [7]. The procedure was modulated into two steps as given below. First, cooling the matrix from high temperature to room temperature was modeled in finite element analyses by using a thermal load. Residual stresses were induced due to the mismatch in the coefficient of thermal expansion. Also, we should note that we 7 PAGE 25 should have same displacement in the matrix and fiber at the interface through out the length of the specimen. The radial displ acement at the center of fiber is zero. In the second step, pushing the fiber out of the specimen with a flat indenter was simulated. In numerical analyses, prescribed displacement was added to the punch until the fiber was completely pushed out from the specimen. The boundary condition of axial displacement being zero along the supported end was applied. Duplicate nodes were created on both fiber and matrix ends. With th e use of these duplicate nodes, fiber matrix bonding was simulated by connecting the duplicat e nodes with spring elements. In this analysis, the interface failure was based upon shear stress cr iterion, that is, when the interfacial shear stress was larger than the critical shear stress value, debonding was assumed to initiate. When the interface debonde d completely, frictional sliding could be observed. Coulombs law was applied for mo deling the frictional sliding. Property variation with temperature was included in the analyses. The results obtained from the numerical analyses [7] were that the residual stresses are symmetric and the shear stresses are asymmetric relative to the center of the specimen. The shear stress vs. length of the specimen was plotted. From the plot it was observed that shear stress was pos itive (as per the coordinate system used in his study) at the loading end, and then slowly decreases a nd changes to negative stress as we go towards the compressive end. When a compressive load is applied on the loading end, the load induces compressive stress in the specimen. Thus by superimposing the shear stress due to compressive loading on the shear stress due to cooling, we observe the shear stress 8 PAGE 26 decrease at the loading end and increase at the supporting end and reach the critical shear stress value. This provides the support for fiber debondin g starting from the supported ends. Load displacement curves were plotted. The load displacement curve was linear up to maximum load after which the load decreased dramatically. This was due to complete debonding of the fiber from the matrix. The shear stress obtained from the peak lo ad in the pushout test in not the exact actual shear stress but it provides a reference value. In this way, numerical analyses are helpful in evaluating the in terfacial shear strength. 1.5 Boundary Element Method (BEM) Ye and Kaw [1] modeled the pushout test us ing an axisymmetric model with fiber as a solid cylinder a nd the matrix is modeled as a hol low cylinder. The study concluded the following. Maximum pushout force is independent of indenter radius, type of indenter and radius of hole. The interfacial stresses remain constant along the length of the specimen except at the top and bottom surfaces. This conclusion from BEM was in agreement with the shearlag model proposed by Shetty [8]). The coefficient of friction extracted fr om BEM differed by 15% from the value that was obtained from shearlag model of Shetty [8]. 9 PAGE 27 1.6 Functionally Graded (FG) Coating Functionally graded coatings offer an im provement of 35 % after heat treatment and 70% before heat treatment on composite fracture [17]. He nce FG coatings are widely used in variety of fields where composite materials are used. SiC monofilaments in Ti based matrix are widely used in aerospace applications. Haque and Choy [17] coated SiC monofilaments with a FG TiC based coating (SiCf/C/ (Ti,C)/Ti) using a close field unbalanced magnetron sputtering. The coated fibers were placed in Ti matrix using isostatic pressing [17]. Carbon layer w ithin the graded system was weakly bonded to the fiber before the heat treatment. This was the re ason for easy debonding of the fiber from the matrix. After heat treatment, the interfacial shear strength was observed to have increased. The percentage of increase depe nded up on the fiber/matrix and FG type of coating. For the above mentioned SiC fiber and Ti matrix, the increase in interfacial strength was around 146%. This increase in interf acial shear strength was due to the formation of brittle titanium silicide or a ternary compound of SiC/C interface, which resulted in better bonding. For the FG coated layers, a reaction la yer was found adhered to the fiber during the pushout test after heat treatment. The remaining layers were found adhered to the matrix itself. The pushout te sts were analyzed with scanning electron microscopy (SEM) which was equipped with bo th secondary and back scattered electron analysis mode, which helped in identifying the region of failure. 1.7 Nonhomogeneous Interphase The interphase region might have multiple regions of chemically distinct region [18]. Interphase is important in mechanic s of composites. Jayaram et al. [19, 20] reviewed the elastic and ther mal effects of interphases, while Chamis [21] and Argon 10 PAGE 28 [22] studied the effects of fracture toughness of composites with interphase. Fracture mechanics models with nonhomogeneous interphases have been developed by Delale and Erdogan [23], Erdogan [24], Kaw [25]. In th ese studies, the elastic moduli of the interphase was assumed to vary exponentially along the radi al thickness. Bechel and Kaw [26] modeled the interphase, with elastic moduli varying as an aribitary piecewise continuous function along its radial thickness. Indentation model for thin layersubstrate geometry with an interphase were developed by Chalasani et al. [27]. The interphase was modeled either as a nonhomogeneous layer or as a homogeneous la yer. The analysis based on design of experiments (DOE) [28] was carried and it wa s found that contact depth is not sensitive to the type of interphase. Critical interfacial stresses differed significantly for film to substrate elastic moduli ratios greater than 25. It was also found that interphase thickness and film to substrate Youngs moduli ratio had the most impact on th e critical interfacial stresses. The variation of elastic moduli in the interphase and indenter radius had the least impact [27]. This study was carried on thin (film) layersubstrate geometry and in this study nonhomogeneous interphase was modeled between the film and the substrate. This study laid the foundation for the present work, single fiber pushout test with a nonhomogeneous interphase. In the present study the nonhomoge neous interphase is modeled between the fiber and the matrix. 1.8 Comparison Between Multi and Single Fiber Pushout Test Till now we confined the total discussion to single fiber pushout test only. Let us now discuss the multifiber pushout test and comp are it with the single fiber push out test. 11 PAGE 29 Single and multifiber pushout tests were carried out on Nicalon/glass (Corning 1723) composite to examine the interfacial properties by Jero et al. [3]. A m 10 flat probe was used in single fiber pushout test to push the fi ber out of the matrix where as in multifiber pushout test m 100 flat probe was used [3]. Th e loading and unloading curve was obtained in both the cases. The experimental obs ervation of various fibers with the above mentioned two processes resulted in the following conclusions [3]. 1. It was only possible to push fibers from thinnest of the multifiber specimens (0.53 mm). In thicker samples (0.95 and 1.70), fibers were crushed before complete debonding. 2. Single fiber pushout tests were easy to conduct where as mu ltifiber tests were difficult. 3. The data obtained from the multifiber te st was more scattered when compared to single fiber. 4. Multifiber pushout test effectively ma gnified fiber/matrix roughness mismatch and compressive stress due to Poissons expansion. 1.9 Present Work In this study, I am studying the pushout test differently from the previous studies as follows. First, most studies neglect the presence of a separate interface layer called the interphase. These separate layers may be either created due to the normal processing of a composite or by intention to develop a co mposite with better properties. Haque and Choy [17] proved experimentally that SiC/Ti composites with interphases offer an improvement on composite fracture of 3570% and an increase in the interfacial strength 12 PAGE 30 of around 146%. Since the charac terization of the fibermatrix interface is dependent on the results obtained from a pushout test, we ha ve developed a model for the test that not only incorporates the interphase but also one which can be nonhomogeneous. Second, I wanted to study the effect of various parameters on the results of the test. I wanted to quantitatively answer th e question of how do the type of indenter, boundary conditions of the specimen, fiber volume fraction, thickness of interphase to fiber radius ratio, and type of interphase m odel effect the loaddisplacement curve and the critical interfacial stresses as these are the parameters that characterize the most of the intrinsic mechanical properties of the fibermatri x interface. I accomplish these two objectives by first developing a finite element analysis model that is capable of incorporating thes e parameters, and then using a design of experiments (DOE) study to develop clear conclusions from a parametric study. 13 PAGE 31 CHAPTER 2 FORMULATION 2.1 Finite Element Modeling The finite element program of AN SYS 11.0 [9] was used for conducting simulations in this study. ANSYS [9] is chos en because it has the capability of solving nonlinear contact problems. For this study axisymmetric half space of the indentation model is developed instead of 3D indentation model because axis ymmetric model takes relatively much less time than the 3D model. Chudoba et al. [29], conducted a study using spherical indentation of both 3D model and the axisy mmetric model and the results deviated by less than 0.1% from Hertzian theory (ANSYS [9]) for a homogeneous half space. 2.1.1 Geometry An axisymmetric finite element mode l of homogeneous fiber surrounded by a homogeneous matrix separated by a nonhomoge neous interphase and the whole fiberinterphasematrix surrounded by a composite is modeled. The geometry of the problem is shown in Figure 2 The model consists of homogeneous fiber, nonhomogeneous interphase, homogeneous matrix and composite of infinite length and finite radius of and respectively. Youngs modulus and Po issons ratio vary arbitrarily along the width of nonhomogeneous interphase where as, they are constant in the homogeneous fiber, matrix and composite part of the model. mifrrr ,,cr 14 PAGE 32 F I M C fr ir mr cr Figure 2 Schematic Diagram of the Fibe rInterphaseMatri xComposite Model 2.2 Meshing the Geometry An axisymmetric model is developed in ANSYS [9] with homogeneous fibermatrix and composite properties. The nonh omogeneous interphase is modeled with nonhomogeneous properties between the fibe r and the matrix. The nonhomogeneous interphase is modeled as series of sub homogeneous layers. The model is meshed with 4 node isoparametric elements (PLANE182). The mesh on the top surface of the fiber (region of indentation) and at the interf aces of the fiber, interphase, matrix, and composite is refined several times to catch the stresses and displacements on the top of the fiber when load is applied and to simu late the perfect bonded contact between the n 15 PAGE 33 fiber, interphase, matrix and composite. The meshed finite element model is shown in Figure 3 Figure 3 Meshed Model of Composite with Nonhomogeneous Interphase 2.2.1 PLANE182 PLANE182 is a 2D structural element in ANSYS [9] element library. It could be used for plane stress, plane strain and axisym metric problems. It is defined by four nodes having two degrees of freedom at each node (translation in X and Y directions). The element has plasticity, hyperelasticity, stress s tiffening, large deflecti on, and large strain capabilities. It also has mi xed formulation capability fo r simulating deformations of nearly incompressible elastoplastic materi als, and fully incompressible hyperelastic materials. 16 PAGE 34 Figure 4 Structure of PLANE182 2.3 Modeling the Bonded Contact in the Composite The contact between the fiber and interpha se, sublayers of inte rphase, interphase and matrix and matrix, and composite is modeled as a bonded contact using contact elements (CONTA 171 and TARGET 169) in AN SYS [9] element library. The interfaces in the finite element model are to be mode led as bonded contact to satisy the continuity equation mentioned in Section 2.5. 17 PAGE 35 Figure 5 Contact and Target Elements at the Interfaces In Figure 5 the violet pink color elements are the contact elements and the elements shown in yellow color are the targ et elements at various interfaces in the composite model. 2.4 Properties 2.4.1 Fiber and Matrix For this study, a glass/epoxy composite is chosen. The Youngs modulus and Poissons ratio for the glass fiber and epoxy ma trix are taken from the data available in the literature. The Youngs modulus and Pois sons ratio of the glass fiber and epoxy matrix are given in Table 1 18 PAGE 36 Table 1 Youngs Modulus and Poisso n's Ratio of Fiber and Matrix Material Elastic modulus (GPa) Poissons ratio Glass fiber 72.6 0.2 Epoxy matrix 2.4 0.3 2.4.2 Interphase The properties of the interphase are calculated assuming the elastic moduli are varying exponentially or lin early through the radial thic kness. If the properties are varying exponentially, then along the radial thickness of the interphase Youngs modulus and Poissons ratio are given by i f brrrraerE ,)( Equation 2 Exponential Variation of Young' s Modulus along the Radial Thickness of Interphase i f drrrrcer ,)( Equation 3 Exponential Variation of Pois son's Ratio along the Radial Thickness of Interphase where , and are found using the Youngs modulus and Poissons ratios at the edges of the layer abcd ifrrrr ,. If the properties are varying linearly, then along the radial thickness of the interphase Youngs modulus and Poissons ratio are given by 19 PAGE 37 i frrrbrarE ,)( Equation 4 Linear Variation of Youn g 's Modulus alon g the Thickness of the Interphase i frrrdrcr ,)( Equation 5 Linear Variation of Poisson's Ra tio along the Thickness of the Interphase where, , and are found using the Youngs modulus and Poissons ratios at the edges of the layer abcd ifrrrr ,. Poissons ratio and the Youngs modulus at the edges of sublayers are given by )()1( )()( )1()(jiji r r jirr drrji ji Equation 6 Poisson's Ratio of the jth layer of Interphase )()1( )()( )1()(jiji r r jirr dxrE Eji ji Equation 7 Young's Modulus of the jthLa y er of the Interphase Where, )( ji =Poissons ratio of sublayer of the interphase, =Youngs modulus of sublayer of the interphase, thj)( jiEthjnnj ,1,...,2,1 subscript for the interphase. iNote that when 1 jfjirr )1(. Also when n j ijirr )1( 20 PAGE 38 2.4.3 Composite The properties of the composite were obtained by applying Sutcus recursive concentric cylinder model [30]. 2.4.3.1 Axial Properties The equations used to calculate the axial properties of composite by using recursive cylinder model are given below. In the equations, in the subscript represent the number of the concentric cylinder (example: N 1 N represent innermost cylinder, that is, fiber), e in the superscript represent the effective property and A in the superscript represent the axial direction (example: represent Youngs modulus, Poisons ratio and shear modulus, respec tively in axial dire ction considering concentric cylinders and represent the Youngs m odulus, Poisons ratio and shear modulus, respectively in axial direction of the cylinder). Ae N Ae N Ae NGvE ,,NA N A N A NGvE ,,thN 2 1 N N Nr r f A N A N A N NEG G k 32 A Nn Ae NNAEfEfE )1(1 N T NN N T N e N N T NN e NN T N e NN e NfGkfGk fGkkfGkk k )()1)( ( )()1)( (1 1 1 T N N N e N N N N A N Ae N A Ae NG k f k f ffvv EE 1 1 )1()(41 2 1 21 PAGE 39 T N N N e N N N N e N N A i Ae N N Ae NN A N Ae NG k f k f ff k k vv fvfvv 1 1 1 11 )1(1 1 1 1 N A N Ae NN A N Ae Nf GGf GG 1 )(2 Equation 8 Equations for Calculating the Axial Properties of the Composite Where, 3,2,1 NWhen only the fiber is considered. All the properties such as will be equal to the properties of the fiber, that is, , When the effective properties will be due to the combination fiber and the interphase. When 1 NAe N Ae N Ae NGvE ,,f A N Ae NEEE f A N Ae Nvvv f A N Ae NGGG 2 N 3 N, the effective properties will be due to the combination of fiber, interphase and matrix. Thus at the end of the effective properties of the composite in axial direction are obtained. 3 N2.4.3.2 Tangential Properties The equations required for the extraction of properties in tangential direction are given below. The nomenclature is same as the above equations and T in the superscript represents the tange ntial direction. T NNGGb 2 2 1 N N Nr r VF Te NNGGFTT1 22 PAGE 40 2 2 1 2 N NN Nr rr Vb NNkkb T NNvvb Te NNvvFTT N N NGb GFTT N Nvb b 43 1 1 N NvFTT b 43 1 2 NN NNN Nb b b a 21 2 1 1 1 1 2 N NN Nb a N N N N N N NGb Vb Gb GFTT VFGb MG 2 1 2 22 3 22 31 3 2 11 1 3 12 11 2NNN N NN N NNN N NNN N N NbVbVFVFaVFa bVbVFVFbaVFa GbPG 2 22N N Te NPGMG G Ae N Ae N e N NE vk M2 *4 1 Te NN e N Te N e N Te NGMk Gk E *4 23 PAGE 41 Te NN e N Te NN e N Te NGMk GMk v * Equation 9 Equations for Calculating the Tangential Properties where 3,2,1 N. When only fiber is considered. All the properties such as will be equal to the properties of the fiber, that is, , 1 NTe N Te N Te NGvE ,,f T N Te NEEE f T N Te Nvvv f T N Te NGGG Note that when 1 N 01 N, then all the values of the terms with 1 N in subscript are zero. When the effective properties will be due to the combination fiber and the interphase. When the effective properties will be due to the combin ation of fiber, interphase and matrix. Thus at the end of 2 N 3 N 3 N, the effective properties of the composite in tangential direction are obtained. 2.4.3.3 Radial Properties As the composite material used for this study is assumed to be transversely isotropic, the propertie s of the composite are same in tangential and radial directions. Hence, the properties of the composite in the polar coordinate system are obtained. 24 PAGE 42 2.5 Continuity Conditions 2.5.1 FiberInterphase The continuity conditions at interface between fiber and interphase for bonded contact are given by [27]. lzzrzrf i r f f r 0),,(),( Equation 10 Radial Stress Continuity in FiberInterphase Interface lzzrzrf i rz f f rz 0),,(),( Equation 11 Shear Stress Continuity in FiberInterphase Interface lzzruzruf i r f f r 0),,(),( Equation 12 Radial Displacement Cont inuity in FiberInterphase Interface lzzruzruf i z f f z 0),,(),( Equation 13 Axial Displacement Continuity in FiberInterphase Interface where, = radial stress at the interface of fiber and interphase in the fiber, = radial stress at the in terface of fiber and interphase in the interphase, = shear stress at the in terface of fiber and interphase in the fiber, = shear stress at the interf ace of fiber and interphase in the interphase, = radial displacement at the interface of fibe r and interphase in the fiber, = radial displacement at the interf ace of fiber and interphase in the interphase, = axial ),( zrf f r),( zrf i r),( zrf f rz),( zrf i rz),( zruf f r),( zruf i r),( zruf f z 25 PAGE 43 displacement at the interface of fibe r and interphase in the fiber, = axial displacement at the interface of fiber and interphase in the interphase. ),( zruf i z2.5.2 Sub Layers of Interphase The continuity conditions at sublayer interfaces of interphase (ijijhr or where 0)1( jir1,2,...,3,2,1 nn j) are given by lzzrzrji ji r ji ji r 0),,(),()1( )1( )( )( Equation 14 Radial Stress Cont inuity at the Interface of jth and j+1th Sublayer of Interphase lzzrzrji ji rz ji ji rz 0),,(),()1( )1( )( )( Equation 15 Shear Stress Contin uity at the Interface of jth and j+1th Sublayer of Interphase lzzruzruji ji r ji ji r 0),,(),()1( )1( )( )( Equation 16 Radial Displacement Co ntinuity at the Interface of jth and j+1th Sublayer of Interphase lzzruzruji ji z ji ji z 0),,(),()1( )1( )( )( Equation 17 Axial Displacement Co ntinuity at the Interface of jth and j+1th Sublayer of Interphase where, = radial stress at the interface of sublayer in the interphase, = shear stress at the interface of sublayer in the interphase, = radial displacement at the interface of sublayer in the interphase, = axial displacement at the interface of sublayer in the interphase. ),()( )(zrji ji rthj),()( )(zrji ji rzthj),()( )(zruji ji rthj),()( )(zruji ji zthj 26 PAGE 44 2.5.3 InterphaseMatrix The continuity conditions at interface be tween interphase and matrix are given by lzzrzri m r i i r 0),,(),( Equation 18 Radial Stress Cont inuity at InterphaseMatrix Interface lzzrzri m rz i i rz 0),,(),( Equation 19 Shear Stress Continuity at InterphaseMatrix Interface lzzruzrui m r i i r 0),,(),( Equation 20 Radial Disp lacement Continuity at Inte rphaseMatrix Interface lzzruzrui m z i i z 0),,(),( Equation 21 Axial Displacement Continuity at InterphaseMatrix Interface where, = radial stress at the interface of interphase and matrix in the interphase, = radial stress at the interface of interphase and matrix in the matrix, = shear stress interface of interpha se and matrix in the interphase, = shear stress at the interface of in terphase and matrix in the matrix, radial displacement at the interface of interphase and matrix in the interphase, = radial displacement at the interface of interphase and matrix in the matrix, = axial displacement at the interface of interphase and matrix in the interphase, = axial displacement at th e interface of interphase a nd matrix in the matrix. ),( zri i r),( zri m r),( zri i rz),( zrm m rz ),( zrui i r),( zrui m r),( zrui i z),( zrui m z 27 PAGE 45 2.5.4 MatrixComposite The continuity conditions at interface be tween matrix and composite are given by lzzrzrm c r m m r 0),,(),( Equation 22 Radial Stress Cont inuity at MatrixComposite Interface lzzrzrm c rz m m rz 0),,(),( Equation 23 Shear Stress Continuity at MatrixComposite Interface lzzruzrum c r m m r 0),,(),( Equation 24 Radial Displacement Cont inuity at MatrixComposite Interface lzzruzrum c z m m z 0),,(),( Equation 25 Shear Displacement Cont inuity at MatrixComposite Interface where, = radial stress at th e interface of matrix and composite in the matrix, = radial stress at the interface of matrix and composite in the composite, = shear stress at the interface of matrix and composite in the matrix, = shear stress at the interface of matrix and composite in the composite, = radial displacement at the inte rface of matrix and composite in the matrix, = radial displacement at the interface of matrix and composite in the composite, = axial displacement at the interface of matrix and composite in the matrix, = axial displacement at the interf ace of matrix and composite in the composite. ),( zrm m r),( zrm c r),( zrm m rz),( zrm c rz),( zrum m r),( zrum c r),( zrum m z),( zrum c z 28 PAGE 46 2.6 Boundary Conditions Because of axisymmetry, the center line of fiber, 0 r is constrained along the radial direction. lzluf r 0,0),0 ( Equation 26 Axisymmetric Condition The specimen is constrained at the bottom in axial direction ( ) as follows. lz m i m zrrrlru ,0),( Equation 27 Matrix Constrained in its Axial Direction at its Bottom End c m c zrrrlru ,0),( Equation 28 Composite Constrained in its Axial Direction at its Bottom End This condition represents a hole in the pushout test. From th e previous studies [31] we know that the radius of the hole has negligible impact on the indentation results. In this study two types of boundary c onditions (BC1 and BC2) are applied. 2.6.1 Boundary Condition 1 (BC1) In the first type (BC1) the composite is stress free at its radial edge (crr ). The equations which represent the BC1 are given below. lzzrc r 0,0),( Equation 29 Radial Stressfree Conditi on at the Radial Edge of the Composite 29 PAGE 47 lzzrc rz 0,0),( Equation 30 Shear Stressfree Condition at the Radial Edge of the Composite Figure 6 Composite with BC1 2.6.2 Boundary Condition2 (BC2) In the second type of boundary condition ( BC2), the matrix is constrained at its radial edge ( ) [2]. mrr lzzrum m r 0,0),( Equation 31 Radial Displacement Constrained at the Radial Ed g e of the Matrix lzzrum m z 0,0),( Equation 32 Axial Displacement Constrained along the Radial Edge of the Matrix This boundary condition is modeled by assuming the composite as a rigid body by assigning the Youngs modulus of composite as 100 times the Youngs modulus of the fiber and the Poissons ratio as 0.48. 30 PAGE 48 2.7 Loading Three types of indenter loads are applied load due to a spherical indenter, a flat indenter and a uniform pressure. 2.7.1 Spherical Indenter The spherical indenter is modeled as a quarter (model is axisymmetric) rigid sphere by assigning its Youngs modulus as 100 times that of the fiber and its Poissons ratio as 0.48. A constant load, is applied to the fiber via pressure, on the top plane of the spherical indenter (see Psp Figure 7 ), 2 R P ps Equation 33 Pressure Applied on the Spherical Indenter where, R radius of the spherical indenter. 31 PAGE 49 F I M C sP R Figure 7 Schematic Diagram of Spherical Indenter Loading 2.7.1.1 Radius of Contact Many initial trial runs in ANSYS [9] using spherical indenter loading with various combinations of the factors (boundary conditio ns of the specimen, fiber volume fraction, thickness of interphase to fiber radius ratio, a nd type of interphase model) show that the contact area does not vary by more than 1%. The contact radius is found by checking the contact status of the contact and target elements on the top surface of the fiber near the contact area. 32 PAGE 50 Figure 8 Contact between th e Fiber and the Indenter Hence, the contact area between the inde nter and fiber depends only on the elastic moduli of the fiber and the indenter. It was also noted that the radius, a of the contact area between the fiber and the spherical indent er was within 1% of what FischerCripps, et al. [32] calculated us ing the following formulas. 3/13 4 fE KPR a )1()1( 16 92 2 in in f fE E K Equation 34 FischerCripps Equation to Calculate the Contact Radius 33 PAGE 51 Where, = Youngs modulus of fiber, fEf = Poissons ratio of fiber, = Youngs modulus of indenter, inEin = Poissons ratio of indenter. Note that the above equations are for the case of a spherical indentor loaded on a homogeneous halfplane. 2.7.2 Uniform Pressure Loading The case of the uniform pressure indenter is only a hypothetical indenter and is considered in this study only because some st udies [2] model the indentation as a uniform pressure. The uniform pressure loading is applied on the fi ber over a finite length. The value of the length over which this uniform pre ssure is applied is equal to the value of contact radius, a found from the spherical indenter loading case. The uniform pressure ( ) is calculated using the formula given below. up 2a P pu Equation 35 Uniform Pressure Applied on the Fiber 34 PAGE 52 F I M CuP a Figure 9 Schematic Diagram Illust rating Uniform Pressure Loading 2.7.3 Flat Indenter The flat indenter is modeled as a cylinder with a circular cro sssection of radius, on the fiber. Like the spheri cal indenter, the flat indenter is treated as rigid and its elastic moduli are chosen to be same as that of the spherical indenter A uniform pressure is applied on the top plane of the flat indenter. aup 35 PAGE 53 Figure 10 Schematic Diagram of Flat Indenter Loading This allows the contact area and total load to be the same, but permits different distributions of load due to the three indenters. 2.8 Factors for Sensitivity Analyses 2.8.1 Type of Indenter Type of indenter plays an important role in fiber pushout test. It determines the amount of load that can be applied on the fibe r. For example, for th e load applied through flat indenter may take the fiber beyond the yield point but, for the same load applied through spherical indenter may not yield the fiber. In this study, three loading conditions are applied. These loading conditions are Uniform Pressure, Spherical I ndenter, and Flat Indenter. 2.8.2 Fiber Volume Fraction The fiber volume fraction is defined as th e ratio of volume of fiber to the volume of composite. 36 PAGE 54 2 2 m fr r FVF Equation 36 Fiber Volume Fraction Fiber volume fraction plays an important ro le in determining the elastic moduli of the composite [33]. 2.8.3 Thickness of Interphase to Radius of Fiber Ratio (TIRFR) It is the ratio of thickness of the interpha se layer present betw een fiber and matrix to radius of the fiber. Functionally graded coatings offer an improvement of 35 % after heat treatment and 70% before heat treatment on composite fracture [17]. The increase in interfacial toughness is dependent on type of fiber/matr ix, type of coating, and the thickness of coating (thickness of interphase). This is the reason for considering this as a factor in this study. For this study, we use TIRFR values of 1/10, 1/15 and 1/20. 2.8.4 Type of Interphase As discussed in the Section 2.8.3, coatings improve the interfacial toughness to large extent. The extent of increase of the interfacial toughness depends on the type of coating. The coatings may be homogeneous or nonhomogeneous. Also the extent of nonhomogenity (variation of elastic moduli) depends up on the type of coating. The type of interphase is in this st udy defined by how the elastic moduli vary along the radial thickness of the interphase. The nonhomogenity is described either by a linear or exponential vari ation of the Youngs modulus and Poissons ratio. 37 PAGE 55 2.8.5 Boundary Conditions Boundary conditions influence the interf acial stresses. Galbraith et al. [10] carried the pushout test and f ound that the interfaci al stresses can be reduced to great extent by keeping a layer on the back face of the specimen. Two kinds of boundary conditions are applied in our study. One considers the composite as stressfree at its radial edge ( BC1), and other one constrains the matrix at its radial edge (BC2). 2.9 Responses for Sensitivity Analyses 2.9.1 Load to Contact Depth Ratio (LCDR) We used load to contact depth ratio (LCDR) as a response for this study because the LCDR is the measure of interphase properties such as shear modulus [2]. The equation for LCDR is given by Equation 37 Note that it is not a nondimensional number. P LCDR Equation 37Load to Contact Depth Ratio Where, P = Load applied, = Displacement at the top (contact depth). 2.9.2 Normalized Maximum Interfac ial Radial Stress (NMIRS) The NMIRS is defined as the nondimensional ratio of the maximum tensile interfacial radial stress ( max),( zrf i r) to the average stress app lied over the contact area, that is, 38 PAGE 56 lz a P zr NMIRSf i r 0, ),(2 max Equation 38 Normalized Maximum Radial Stress at the FiberInterphase Interface NMIRS is taken as a response for this st udy because when the fiber is loaded, the crack initiation is observed at the back face of the specimen when the interfacial tensile radial stress exceeds the bond strength [10, 3437]. In this study, the maximum interfacial tensile radial stress is taken as the interfacial tensile radial stresses cause fiber debonding from the matrix. 2.9.3 Normalized Maximum Interfacial Shear Stress (NMISS) The NMISS is defined as the nondimensiona l ratio of the magnitude of maximum interfacial shear stress ( max),( zrf i rz) to the average stress a pplied over the contact area, that is, lz a P zr NMISSf i rz 0, ),(2 max Equation 39 Normalized Maximu m Shear Stress at the FiberInterphase Interface In this study, the absolute value of the maximum interfacial shear stress is taken because positive or negative direction of the sh ear stress is completely dependent on the coordinate axes chosen. 39 PAGE 57 2.10 Modeling the Contact between the Fiber and the Indenter The regions, near the top surface of th e fiber and the bottom surface of the indenter are meshed very densely. The top surface of the fiber is meshed with target elements (TARGET 169) and the bottom face of the indenter, which comes in contact with the fiber when load is applied, is meshed with contact elements (CONTA 171). Figure 11 Finite Element Model of Co mposite with Spherical Indenter Figure 11 shows the finite element model of composite with a spherical indenter modeled. The spherical indenter is modele d as a quarter sphere as the model is axisymmetric. 40 PAGE 58 CHAPTER 3 VALIDATION OF MODEL Initially a homogeneous half space meshed with PLANE182 elements and loaded by an axisymmetric pressure loading is examined. The stresses and displacements in the fi nite element model show good agreement with the classical Terezawas [38] solution for a semiinfinite medium of homogeneous half space with an axisymmetric arbitrary pressure loading. Before starting the ANSYS [9] runs for al l the combinations of factors, several checks are performed to ensure the accuracy of the model. Accuracy of the model is checked for each indenter loading case as follows. 3.1 Spherical Indenter Spherical indenter loading is applie d on the fiber by applying a pressure, on the top plane of the spherical indenter (see sp Figure 7 ). Radius of contact, is obtained by checking the contact status of the contact elements in ANSYS [9]. a3.1.1 Contact Between the Indenter and Fiber Using an APDL code, all the nodal in formation of the nodes (node number, location of node, displacements, all stress comp onents, and all elastic strains) on the top surface of the fiber and whose x coordinate (radial distance from the center of the fiber) is less than 1.5 times the contac t radius are written to a te xt file. Now using a MATLAB 41 PAGE 59 [39] program, this file is analyzed, and each and every nodal data is read into an array inside MATLAB. Axial displacement and axial st resses are cubic spline interpolated with respect to the radial distance from the center of the fiber. After the spline interpolation, the axial stress and displacements are plotted against the radial distance from the center of the fiber. (Note: All the nodes are taken on the top surface, so the coordinate would be zero for all the nodes). y Figure 12 Typical Distribution of Normalized Axial Stress Along the Normalized Radial Distance from the Center of the Fiber for Spherical Indenter Figure 13 Typical Distribution of Normalized Axial Disp lacement Along the Normalized Radial Distance from the Center of the Fiber for Spherical Indenter Figure 12 and Figure 13 both the axes are normalized. The axial stress is normalized with the pressure applied fo r the uniform pressure indenter (see Equation 35). The radial distance and the axial displacemen ts are normalized with the contact radius. 42 PAGE 60 From Figure 12 it can be clearly seen that the axial stress is distributed parabolically in the contact area. The axial stress suddenly becomes nearz ero value afte r passing the contact radius. It is also observed that the contact radius found in ANSYS [9] by checking the contact status of the contact elemen ts is equal to the contact radius extracted from MATLAB program. Also the load ap plied on the fiber is calculated using MATLAB program from the axial stress data available. a z matlabrdr P02 Equation 40 Total Load on the Fiber using th e Axial Stress Data on the Top of the Fiber Total load applied on the spherical indenter is calculated using )()(2RpPs Equation 41 Total Load Applied on the Fiber through Spherical Indenter It is observed that the loads, P and differ by less than 1%. This verifies our contact between the fiber and i ndenter as the load applied is obtained back by integrating the axial stresses over the contact area. matlabP 3.1.2 Bonded Contact Between the Interfaces Using an APDL code, displacement, shear stress in radialaxial plane, and the radial stresses of the nodes at the interf aces of the fiberinterphase, sublayers of interphase, interphasematrix and matrixcomposite are written to text files. By analyzing the text files using a MATLAB program, it is f ound that the displacements and stresses of the nodes of either side of the interface differ by less than 1%. This validates the bonded contact between the inte rfaces in the model. 43 PAGE 61 3.2 Uniform Pressure Indenter Uniform pressure indenter loading is appl ied on the fiber by applying a uniform pressure, on the top plane of the fiber (see up Figure 9 ). 3.2.1 Contact Between the Indenter and Fiber Using an APDL code, all the nodal in formation of the nodes (node number, location of node, displacements, all stress comp onents, and all elastic strains) on the top surface of the fiber and whose x coordinate (radial distance from the center of the fiber) is less than 1.5 times the contact radius ar e written to a text file. Now using MATLAB program, this file is analyzed and each and ev ery nodal data is read into an array inside MATLAB. Now axial displacement and axial st resses are cubic spline interpolated with respect to radial distance from the center of the fiber. After the spli ne interpolation, the axial stress and displacements are plotted against the radial distance from the center of the fiber. Figure 14 Typical Distribution of Normalized Axial Stress Along the Normalized Radial Distance from the Center of the Fiber for Uniform Pressure Indenter 44 PAGE 62 Figure 15 Typical Distribution of Normalized Axial Disp lacement Along the Normalized Radial Distance from the Center of th e Fiber for Uniform Pressure Indenter Figure 14 and Figure 15 both the axes are normalized. The axial stress is normalized with the pressure applied over th e uniform pressure indenter. The radial distance and the axial displacements are normalized with the contact radius. From the Figure 14 it can be clearly seen that the axial st ress is uniform in the contact area and is equal to and decreases immediately to a very lo w value after the contact radius. It is also observed that the contact radius found in ANSYS [9] by checking the contact status of the contact elements is equal to the cont act radius extracted from MATLAB. Also the load applied on the fiber is calculated using MATLAB program from the axial stress data available using up Equation 40 Total load applied on the fibe r using uniform pressure i ndenter is calculated using the following formula. )()(2apPu Equation 42 Load Applied on the Fiber through Unif orm/Flat indenter 45 PAGE 63 It is observed that the loads, and differ by less than 1%. This verifies our contact between the fiber and i ndenter as the load applied is obtained back by integrating the axial stresses over the contact area. PmatlabP 3.2.2 Bonded Contact Between the Interfaces Using an APDL code, displacement, shear stress in radialaxial plane, and the radial stresses of the nodes at the interf aces of the fiberinterphase, sublayers of interphase, interphasematrix and matrixcomposite are written to text files. By analyzing the text files using a MATLAB program, it is f ound that the displacements and stresses of the nodes of either side of the interface differ by less than 1%. This validates the bonded contact between the inte rfaces in the model. 3.3 Flat Indenter Flat indenter loading is applied on the fiber by applying a pressure, on the top plane of the flat indenter (see up Figure 10 ). 3.3.1 Contact Between the Indenter and Fiber Using an APDL code, all the nodal in formation of the nodes (node number, location of node, displacements, all stress comp onents, and all elastic strains) on the top surface of the fiber and whose x coordinate (radial distance from the center of the fiber) is less than 1.5 times the contact radius ar e written to a text file. Now using MATLAB program, this file is analyzed and each and ev ery nodal data is read into an array inside MATLAB. Now axial displacement and axial stresses are cubic spline interpolated with respect to radial distance from the center of the fiber. After the spli ne interpolation, the 46 PAGE 64 axial stress and displacements are plotted against the radial distance from the center of the fiber. Figure 16 Typical Distribution of Normalized Axial Stress Along the Normalized Radial Distance from the Center of the Fiber for Flat Indenter Figure 17 Typical Distribution of Normalized Axial Disp lacement Along the Normalized Radial Distance from the Center of the Fiber for Flat Indenter Figure 16 and Figure 17 both the axes are normalized. The axial stress is normalized with the pressure applied over th e uniform pressure indenter. The radial distance and the axial displacements are nor malized with the contact radius. From Figure 17, the axial displacement is clearly unif orm in the contact area and decreases 47 PAGE 65 immediately after the radi us of contact. Also from Figure 16 it can be clearly observed that the axial stress increases through the contact radius, a nd reaches a maximum value at the contact radius. Beyond the contact radius, it drops to a very low value. It is also observed the contact radius found in ANSYS [9] by checking the contact status of the contact elements is equal to the contact radius extracted from MATLAB. Also the load applied on the fiber is calculated using the MATLAB program from the axial stress data available using Equation 40. Total load applied on the fiber using the flat indenter is calculated using Equation 42. It is observed that the loads, and differ by less than 1%. This verifies our contact between the fiber and i ndenter as the load applied is obtained back by integrating the axial stresses over the contact area. PmatlabP 3.3.2 Bonded Contact Between the Interfaces Using an APDL code, displacement, shear stress in radialaxial plane, and the radial stresses of the nodes at the interf aces of the fiberinterphase, sublayers of interphase, interphasematrix and matrixcomposite are written to text files. By analyzing the text files using MATLAB program, it is found that the displacements and stresses of the nodes of either side of the interface differ by less than 1%. This validates the bonded contact between the inte rfaces in the model. 3.4 Validation with Huang SLA and Finite Element Model Huang et al. [2] verified the accuracy of an analytical solution based on shearlag assumptions by a finite element method model, and concluded that their shearlag model 48 PAGE 66 results are with in 1% of the finite element results. In their model, they used the boundary condition, BC2 and applied a uniform pressure, applied on the top of the entire fiber, as given by huangp f f huangrrz r P p 0,0,2 Equation 43 Loading Condition for Huang Model Shearlag model relates the shear modulus of the inter phase to LCDR as given below [2]. D G LCDRi Equation 44 LCDR from Huang's Shear Lag Model f fiir BrraraL D2 )1)(/ln()coth( )/ln( )/ln( 1 ))/ln(/(22 fim mii fiffirrG rrG rrrEG a )/ln( )/ln(fim miirrG rrG B Equation 45 Intermediate Parameters to be Calculated for LCDR using Huang's Model where, iG = Shear modulus of interphase, mG = Shear modulus of the matrix. 49 PAGE 67 Huang et al. [2] found that the values obtained by the Equation 44 are within 1% of the finite element model. We verified this with our own finite element model by applying the same boundary condi tions and load as Huang, et al. [2]. The results were within 2% of Huangs [2] model. However, Huangs [2] FEM model makes many assumptions such as 1. Uniform loading over the fiber radius (when actually load is only applied only over a small area). 2. Homogeneous interphase (when actually interphase may be nonhomogeneous). 3. Constrained matrix along the radial e dge (when actually it is surrounded by a cylinder with composite properties). Only the first of the above three assumptions is quantitatively critical. Loading by spherical indenters occurs only over a very small area of the fiber. Approximating this loading as distributed throughout the fiber can underestimate the shear modulus of the interphase by the order as much as 1000. 3.5 Validation Using Interfacial Stresses In this validation, interfacial stresse s are observed when load is applied. 3.5.1 Validation Using Interfacial Radial Stress The interfacial radial stress is very large and compressive at the top end, decreases, and almost stays c onstant (near zero va lue) along the length of the fiber and changes to a positive value (tensile) as it r eaches the bottom end of the composite. This distribution of interfacial radial stress is in agreement with the BEM [1]. 50 PAGE 68 Figure 18 Typical Distribution of Normalized Interfacial Radial Stress Along the Normalized Length of the Fiber In the Figure 18 the interfacial radial stress is normalized with the pressure applied on uniform indenter. The length of the fiber is normalized with the fiber radius. Integrating the radial stress along the radial surface area of the fiber gives the force applied on the fiber in radial direction. As ther e is no force applied in the radial direction the value comes out to be zero. 0 20L i rfdzr Equation 46 Force in Radial Direction from the Interfacial Radial Stress 51 PAGE 69 Figure 19 Typical Distribution of Normalized Interfacial Radial Displa cement Along the Normalized Length of the Fiber In Figure 19 the interfacial radial displacement is highly negative at the top face (loading end), then along the length of the fiber increases gradua lly and changes to a positive value. It becomes a near zero value at the back face of the fiber. 3.5.2 Validation Using Interfacial Shear Stress It is also observed the interfacial shear stress is very small (near zero) at the top face of the fiber and increases to certain length of the fibe r and again gradually decreases along the length of the fiber and reaches a near zero value at the bottom end of the fiber. 52 PAGE 70 Figure 20 Typical Distribution of Normalized Interfacial Shear Stress Along the Normalized Length of the Fiber In the Figure 20 the interfacial shear stress is normalized with the pressure applied on the uniform indenter. The length of the fiber is normalized with the fiber radius. Integrating the shear stress along the ra dial surface area of the fiber gives the axial load applied on the fiber. L i rzfdzrP02 Equation 47 Axial Force Applied on the Fiber from the Interfacial Shear Stress 53 PAGE 71 Figure 21 Typical Distribution of Normalized Interfacial Axial Displacement Along the Normalized Length of the Fiber In Figure 21 the interfacial axial displacement is highly negative at the top face (loading end), and then along the length of the fiber increases gradually. The maximum negative axial displacement is found at th e top face (loading end) and the minimum is found at the back face. The in terfacial axial displacement is negative throughout the fiber length. 54 PAGE 72 CHAPTER 4 RESULTS AND CONCLUSIONS This study uses a formal Design of Experi ments (DOE) [27] analysis to quantify the effects on parameters 1. LCDR, 2. NMIRS, 3. NMISS, due to the parameters 1. Type of indenter, 2. Fiber volume fraction, 3. Thickness of interphase, 4. Type of interphase, and 5. Boundary conditions. For this purpose we designed experiments using mixed level full factorial design. The five factors chosen for the mixed level full factorial desi gn and their le vels are shown in Table 2 55 PAGE 73 Table 2 Values of Different Levels of the Factors Factor Symbol Level 1 Level 2 Level 3 Type of Indenter A Uniform Pressure Indenter Spherical Indenter Flat Indenter Fiber Volume Fraction B 0.5 0.6 0.7 Thickness of Interphase to Fiber Radius Ratio C 1/20 1/15 1/10 Type of Interphase D Linear Exponential Boundary Conditions E BC1 BC2 An APDL code is developed and the results are obtained for all the test runs. The APDL code is developed such that the values of LCDR is written to a text file consisting of the values of the factors in that run as its file name at the end of each run. Also the interfacial stresses are also written to a different text file at the end of each run. Now using MATLAB [39] program, the data from th e each file is read into an array, spline interpolated (cubic spline interpolation) and the value of NMIRS and NMISS are determined in each run. These values are written into a different excel file and DOE analysis is carried using Minitab [40] to qua ntify the effect of the above factors on the responses. 56 PAGE 74 4.1 Responses for the Sensitivity Analyses 4.1.1 Load to Contact Depth Ratio (LCDR) Figure 22 shows the normalized load to contact depth ratio for different indenters. The normalization is done with respect to the load to contact depth ratio of the spherical indenter. Figure 22 show that, the flat indenter gives the higher LCDR value for the same load. This also shows that the LCDR can di ffer by as much as 20 to 50% between the types of indenter. 0.8 1 1.2 1.4 1.6 uniform spherical flat Type of IndenterNormalized Load to contact depth ratio Figure 22 Normalized LCDR as a Function of Type of Indenter. Table 3 shows that only the type of indenter has the significant effect on LCDR. All other factors have nea rzero effect on load to c ontact depth ratio (LCDR). 57 PAGE 75 Table 3 Percentage Contribu tion of Factors to Load to Contact Depth Ratio SOURCE PERCENTAGE CONTRIBUTION A 99.9 (A= Type of Indenter, B= Fiber Volume Fraction, C= Thickness of Interphase to Fiber Radius Ratio, D= Type of Interphase, E=Boundary Conditions) 4.1.2 Normalized Maximum Interfac ial Radial Stress (NMIRS) When indenter load is applied on the fiber, interfacial radial stre ss at the top face is found to be compressive and it is found to be tensile at the back face of the specimen (see Figure 18 ). The NMIRS used in this study is the maximum tensile interfacial radial stress obtained from the back face of the specimen. Figure 23 Figure 24 and Figure 25 show typical parametric curves for the normalized maximum interfacial radial stress as a function of the fiber volume fraction for different boundary conditions, interphase thickness, and type of interphase respectively. 58 PAGE 76 Figure 23 Normalized Maximum Interfacial Radial Stress as a Function of Fiber Volume Fraction for Uniform Pressure Indenter, Line ar Type of Interphase, and TIRFR=1/20. In the pushout test, both in terfacial radial and hoop st resses are dependent on the specimen configuration. Figure 23 shows that, the value of NMIRS for BC1 is higher than that for BC2. For the boundary condition, BC2, the radial edge of matrix is totally constrained, and hence the bulging that occurs when the load is applied on the fiber is reduced greatly as compared to the boundary condition, BC1, where the radial edge of the composite is free [10]. This resulte d in the lower valu e of NMIRS for BC2. Figure 23 show that, the NMIRS differ as much as by 48% with boundary conditions for higher fiber volume fraction and differ as much as by 115% for lower fiber volume fraction. 59 PAGE 77 Figure 24 Normalized Maximum Interfacial Radial Stress as a Function of Fiber Volume Fraction for Spherical Indenter Loading, Linear Type of Interphase, and BC1 Figure 24 shows NMIRS for different interphase thickness as a function of fiber volume fraction. Figure 24 show that, the NMIRS differ as much as by 39% with type of interphase for higher fiber volume fraction a nd differ as much as by 22% for lower fiber volume fraction. The value of NMIRS decreases with the increase in thickness of the interphase. Figure 25 Normalized Maximum Interfacial Radial Stress as a Function of Fiber Volume Fraction for Flat Indenter Loading, TIRFR=1/20, and BC2. Figure 25 shows NMIRS for different types of interphase as a function of fiber volume fraction. Figure 25 show that, the NMIRS differ as much as by 9% with type of 60 PAGE 78 interphase for higher fiber volume fraction a nd differ as much as by 11% for lower fiber volume fraction. Table 4 shows that the normalized maximum interfacial radial stress is sensitive to boundary conditions (57%), fiber volume fr action (20%), combined effect of fiber volume fraction and boundary conditions (15%), thickness of interphase (3%), and type of interphase (1%). What is more evident is that the normalized maximum radial stress at the interface is not sensitive to the type of indenter. Table 4 Percentage Contributi on of Factors to NMIRS SOURCE PERCENTAGE CONTRIBUTION B 19.88 C 3.23 D 1.21 E 57.45 B*E 14.73 C*E 1.20 (A= Type of Indenter, B= Fiber Volume Fraction, C= Thickness of Interphase to Fiber Radius Ratio, D= Type of Interphase, E=Boundary Conditions) 4.1.3 Normalized Maximum Interfacial Shear Stress (NMISS) Figure 26 shows typical parametric curves for the normalized maximum interfacial shear stress as a function of the fiber volume fr action for the two different boundary conditions. Figure 26 also shows that the valu e of NMISS increases with increase of fiber volume fraction. 61 PAGE 79 Figure 26 Normalized Maximum Interfacial She ar Stress as a Function of Fiber Volume Fraction for Uniform Indenter, Linear Type of Interphase, and TIRFR=1/20 Figure 26 show that, the NMISS differs as much as by 12% with type of interphase for higher fiber volume fraction, and differs as much as by 14% for lower fiber volume fraction. Figure 27 Normalized Maximum Interfacial She ar Stress as a Function of Fiber Volume Fraction for Spherical Indenter Loading, Linear Type of Interphase, and BC1 Figure 27 show that the NMISS differs by as much as 16% with type of interphase for higher fiber volume fraction and differs as much as by 20% for lower fiber volume fraction. The NMISS value increases with the thickness of the interphase. 62 PAGE 80 Figure 28 Normalized Maximum Interfacial She ar Stress as a Function of Fiber Volume Fraction for Flat Indenter Loading, TIRFR=1/20, and BC2. Figure 28 shows NMISS for different types of interphase as a function of fiber volume fraction. Figure 28 show that the NMISS differs as much as by 8% with type of interphase for higher fiber volume fraction and differs as much as by 9% for lower fiber volume fraction. Table 5 shows that the normalized maximum interfacial shear stress is mainly sensitive to fiber volume fraction (30%), boundary conditions (27%), thickness of interphase (23%), and the type of interphase (18%). What is more evident is that the normalized maximum shear stress at the interf ace is also not sensitive to the type of indenter. 63 PAGE 81 Table 5 Percentage Contribution of Factors to Normalized In terfacial Maximum Shear Stress SOURCE PERCENTAGE CONTRIBUTION B 30 C 23.25 D 18.28 E 26.91 (A= Type of Indenter, B= Fiber Volume Fraction, C= Thickness of Interphase to Fiber Radius Ratio, D= Type of Interphase, E=Boundary Conditions) 4.2 Conclusions The objective of this study was to study the effect of various geometrical, loading and material parameters in the pushout test where the interphase is modeled as a nonhomogeneous interphase. Since the loadd isplacement curve an d the interfacial stresses dictate the characteriz ation of the fibermatrix in terface, these parameters are used as the response variables in a design of experiments study. Shearlag models approximate the distribut ed loading on the entire fiber, but this assumption can underestimate the shear modulus of the interphase by the order as much as 1000. The quantitative analysis showed that flat indenter gives higher LCDR value than spherical and uniform pressure indenters. Th e LCDR value can change from 20 to 50% depending upon the type of inde nter used for pushout test. Depending upon the boundary conditions the NMIRS value can change from 50 to 115%. Thickness of interphase changes the value of NMIRS from 22 to 39%. The 64 PAGE 82 interfacial radial stress d ecreases with the increase in thickness. Also the type of interphase can change the NMIRS value from 9 to 11%. NMISS value can change up to 14% depending upon the boundary conditions. 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