A numerical study of the influence of Z-pin parameters on the elastic properties of laminates

Abstract

A finite element model with periodic boundary conditions was developed to investigate the influence of different Z-pin parameters including diameter, spacing, and insertion angle of Z-pin on the elastic properties of composite laminates. Benchmark tests were carried out to verify the FE model and a series of parametric analyses were subsequently performed. In general, all the elastic moduli, excluding the through-thickness modulus (E_z), decreased while E_z increased nonlinearly with increasing Z-pin diameter and decreasing spacing. The reduction of E_y (transverse modulus) was approximately 40% of that of E_x (longitudinal modulus), while the reduction of G_xy is similar to that of E_x. Besides, G_xz and G_yz were reduced by approximately half of the reduction of G_xy. Although the impact of insertion angle was obvious on E_z, it was negligible on the other five moduli.

Keywords

Z-pin composite laminate elastic modulus Poisson’s ratio finite element analysis

Introduction

Due to the lack of fibers in the through-thickness direction, the interlaminar mechanical properties of composite laminates are usually poorer than the in-plane properties. In order to enhance the through-thickness properties of composite laminates, Z-pinning has been widely used and proven to be effective in improving the poor impact damage tolerance and bonding properties between two layers.^1-3 Research on Z-pinned composite joints also shows that Z-pin can significantly improve the joint carrying capacities.^4-8 However, the in-plane properties of Z-pinned laminates would be degraded due to the defects induced by the insertion of Z-pin.¹ One of the major defects is the resin-rich region (see Figure 1) resulting from the filling of resin into the region between Z-pin and fibers which are diverted to accommodate the insertion of Z-pin. Comparing to the original laminate material, the resin has much poorer properties. Therefore, the existence of resin-rich region would have a negative influence on the moduli of laminates. Another major defect is the abovementioned diverted fibers, also known as fiber waviness. Obviously, these wavy fibers would affect the mechanical properties of the laminates.¹

Figure 1.

Typical in-plane microstructure of Z-pinned unidirectional laminate.⁹

In order to understand how and to what extent the insertion of Z-pin would influence the performance of composite laminates, an increasing number of studies on mechanical properties of Z-pinned composites have been carried out through experiments^9-20 and the results showed that the insertion of Z-pin would lead to the reduction of the in-plane mechanical properties of the laminate. Chang et al.⁹ investigated the in-plane tensile properties of unidirectional and quasi-isotropic Z-pinned laminates. Test results showed that both longitudinal modulus and tensile strength decreased linearly with pin volume content and pin diameter. Later, Chang et al.¹¹ explored the effect of Z-pin on the flexural properties of carbon/epoxy laminates. Although the Z-pin process would introduce resin-rich zone and fiber distortion damage into the [0°/90°] pattern laminate, the experimental results showed that pins did not affect the flexural modulus probably due to the modulus knockdown resulting from the crimp in the satin weave, while the flexural strength decreased as the density and diameter of Z-pin increased. Mouritz¹² found that the elastic modulus, compressive strength of the unidirectional laminate reduced with increasing volume content (0.5%, 2%, 4%) and diameter (0.28 mm, 0.51 mm) of Z-pin. Hoffmann and Scharr¹³ found that both circular and rectangular Z-pin would lead to the reduction of stiffness and strength of unidirectional and quasi-isotropic laminates while the influence of the circular Z-pin was more obvious. Cui et al.¹⁴ experimentally examined the stiffness of Z-pinned unidirectional laminates under combined transverse compression and shear load. Results showed that the stiffness of Z-pinned laminates decreased significantly in all off-axis angles (different angles representing different mixture ratios of compression and shear load).

Despite the fact that experimental study is the most reliable method to examine the in-plane properties of Z-pinned laminates, parametric analysis of the influence of different Z-pin parameters including diameter, insertion density, and insertion angle of Z-pin is very time-consuming. It is not practical to measure all the elastic properties of Z-pinned laminates, such as longitudinal modulus (E_x), transverse modulus (E_y), out-of-plane modulus (E_z), shear modulus (G_xy, G_xz, G_yz) and Poisson’s ratio (µ_xy, µ_xz, µ_yz) through experiments. Besides, the scatter of experimental data would sometimes cover the influence of Z-pin parameters. In addition, it is extremely difficult to measure and understand the effect of Z-pin on local stress distribution through experiments. Therefore, numerical simulations are required to estimate the influence of Z-pin parameters on the elastic constants of Z-pinned laminates in depth. Steeves and Fleck¹⁰ used a 2D FE code to investigate the in-plane compressive properties of unidirectional carbon-epoxy laminates. In this model, fiber waviness and resin-rich region were taken into consideration, while the Z-pin was replaced by resin to simplify the model. Besides, the boundary conditions imposed on the unit cell were simplified by applying compressive load symmetrically to the specimen and constraining three degrees of freedom to prevent rigid body translation and rotation. Grassi et al.²¹ built a unit cell model consisting of Z-pin, resin-rich region, and fiber waviness region. Although all the main features of a Z-pinned laminate were included in this model, the boundary condition was similar to that used in Ref.¹⁰ Grassi et al.²¹ numerically explored the influence of Z-pin with a diameter of 0.28 mm and volume content of 2% on the engineering elastic constants of laminates and local stress distribution. This study provided a better understanding of the stress distribution in the Z-pin and how the Z-pin changed the local stress distribution, which was difficult to be studied through experiments. Dickinson²² used a unit cell FE model considering the features of Z-pin, resin-rich region, and fiber waviness to analyze the influence of Z-pin material, volume content, diameter, insertion angle on the engineering elastic constants of laminates with different ply stacking sequences. In Dickinson’s model,²² a known macro-stress was applied to the unit cell boundary to simplify the periodic boundary condition and the unit cell was constrained to deform a certain shape at the boundaries. Recently, Pierreux et al.²³ presented a computational approach to generate a structure of Z-pinned laminate consisting of Z-pin, resin-rich zone, and fiber waviness. Periodic boundary conditions were applied while only the influence of stacking sequence and Z-pin content was examined. It could be seen that the parametric study of the Z-pin parameters including diameter, insertion density, and insertion angle on the elastic properties of laminates through a proper model is still limited.

Therefore, in the present contribution, a proper periodic unit cell model of a Z-pinned unidirectional laminate including the features of fiber waviness, resin-rich region, Z-pin, and the unreinforced region was presented. Besides, periodic boundary conditions were applied. The influence of Z-pin diameter, insertion density (Z-pin spacing in this work), and insertion angle on the elastic properties of unidirectional laminates was examined quantitatively to provide a more reliable and comprehensive understanding on the changing trend of each elastic property against Z-pin parameters.

Finite element model

Selection of the unit cell

Figure 2 illustrates the microstructure of Z-pinned unidirectional laminates that contain 5 × 3 unit cells. After Z-pins with row spacing L and column spacing S are inserted into the laminate, an eye-shape zone would be formed around each inserted Z-pin. When the Z-pin spacing is small enough, i.e. S is smaller than the length of eye-shape region l, resin-rich channel would be formed along the fiber direction of the laminate (see Figure 2 (b)). For both the abovementioned conditions, the whole structure can be formed by copying and translating any one of the 5 × 3 unit cells in Figure 2. Therefore, a repeated unit cell (i.e., RUC) with length S and width L was selected to establish the FE model in this work. In order to study the elastic properties in the thickness direction, a 3D model is required. This means a thickness value should be assigned to the unit cell. Because this work was mainly focused on the unidirectional laminate, any value of thickness can be assigned to ensure periodicity. As an example, the unit cell thickness T was assigned to be equal to the thickness of the prepreg herein. Obviously, the chosen RUC is periodic in 3D space and periodic boundary conditions should be applied.

Figure 2.

Multi-cell models with 5 × 3 repeating unit cells (RUCs): (a) RVEs with eye-shape resin-rich regions; (b) RVEs with resin-rich channels.

Fiber waviness and resin-rich region

In order to alleviate the effect of Z-pin insertion, the in-plane fibers are separated to make space for the Z-pin. The influence of the inserted Z-pin on the fibers around Z-pin is shown in Figure 3. For a Z-pinned laminate with Z-pin diameter D and spacing L × S, the influenced region is restricted in the rectangle with a length of l and width of w. Orientations of the fibers outside this region were not affected by the Z-pin. Obviously, the angle between the deformed fiber and the longitudinal direction reaches the maximum α_max on both the edges of the eye-shape resin-rich region. The orientation of deformed fiber is related to its coordinates. Thus, it can be assumed that the angle α is a function of the in-plane coordinates (x, y) with the following boundary value conditions:

x = 0, α = 0

y = \pm \frac{w}{2}, α = 0

x = - \frac{l}{2}, y = 0, | α | = α_{max}

x = \frac{l}{2}, y = 0, | α | = α_{max}

Figure 3.

Illustration of in-plane fiber waviness.

It could be assumed that the fiber orientation is symmetric about the x-axis. Therefore, angle α can be described as

α = a x (\frac{w}{2} - | y |)

where a is an unknown coefficient.

In Eq. (2), |α| increases when |x| increases or |y| decreases. This is in accordance with the variation of fiber orientation shown in Figure 3. Substituting the boundary value conditions in Eq. (1) into Eq. (2), the following equations can be derived

α = - \frac{4 α_{max}}{l \times w} x (\frac{w}{2} - | y |) y > 0

α = \frac{4 α_{max}}{l \times w} x (\frac{w}{2} - | y |) y < 0

where α_max can be approximately expressed as

α_{max} = {tan}^{- 1} (\frac{D}{l})

Bianchi and Zhang²⁴ reported that the length of fiber region l influenced by Z-pin was usually four to six times of the Z-pin diameter D. Therefore, l was assigned to be 5D in this study. Chang et al.⁹ observed that the width of the fiber region w influenced by Z-pin was approximately 0.8 mm and 1.5 mm for Z-pin with diameters of 0.28 mm and 0.51 mm, respectively. Thus, the corresponding width was considered and utilized in this work.

In order to define the orientations of fibers in the FE model, an in-house program was developed and used. Taking the fibers in the first quadrant of Figure 3 as an example, if the radius of the eye-shape arc is R, the following equation can be formed:

R^{2} - {(\frac{l}{2})}^{2} = {(R - \frac{D}{2})}^{2}

in which, l = 5D, thus

R = 6.5 D

Therefore, the eye-shape arc equation can be described as

x^{2} + {(y + 6 D)}^{2} = {(6.5 D)}^{2}

The regions of the first quadrant can be given as follows

0 \leq x \leq \frac{l}{2}

0 \leq y \leq \frac{w}{2}

x^{2} + {(y + 6 D)}^{2} > {(6.5 D)}^{2}

In this way, the orientations of fibers in this quadrant can be defined using Eqs. (3) and (4) in accordance with the nodal coordinates of the elements. The orientations of the fibers in the other three quadrants can be described in a similar way. Thus, the orientation of each element in the ABAQUS model could be assigned a rotation angle according to its coordinates to reflect the influence of the fiber waviness.

Periodic boundary condition

In this study, the periodic boundary condition derived by Xia et al.^25,26 was used. For the cubic unit cell shown in Figure 4, the displacement field on the boundary can be expressed as

Figure 4.

A cube unit cell.

u_{i} = {\bar{ε}}_{i k} x_{k} + u_{i}^{*}

where ${\bar{ε}}_{i k}$ is the average strain of the unit cell, x_k is the coordinate of a point in the unit cell, $u_{i}^{*}$ is an unknown value representing the modification of periodic function from one unit cell to another. The displacements on a pair of opposite boundaries can be written as

u_{i}^{j +} = {\bar{ε}}_{i k} x_{k}^{j +} + u_{i}^{*}

10a

u_{i}^{j -} = {\bar{ε}}_{i k} x_{k}^{j -} + u_{i}^{*}

10b

where “j+” represents the boundary surface of which the exterior normal vector points to the positive axis, “j−” denotes the surface of which the exterior normal vector points to the negative axis. The unknown function $u_{i}^{*}$ can be removed by subtracting Eq. (10b) from Eq. (10a)

u_{i}^{j +} - u_{i}^{j -} = {\bar{ε}}_{i k} (x_{k}^{j +} - x_{k}^{j -})

in which, $(x_{k}^{j +} - x_{k}^{j -})$ is the distance between two opposite boundaries that is a constant value when the unit cell has been selected. Besides, ${\bar{ε}}_{i k}$ can be known once the external load is given.

As such, Eq. (11) can then be applied to the FE model. Herein, an in-house program was developed to achieve the establishment of periodic boundary conditions between each pair of nodes on the boundary. In this work, displacements and rotations of the cubic unit cell in Figure 4 were restricted properly on vertexes A, C, D and H

u_{x} = u_{y} = u_{z} = u r_{x} = u r_{y} = u r_{z} |_{D} = 0

12a

u_{z} = u r_{x} = u r_{y} |_{A} = 0

12b

u_{y} = u_{z} = u r_{x} = u r_{y} = u r_{z} |_{C} = 0

12c

u r_{z} |_{H} = 0

12d

where u_x, u_y and u_z are the displacements along x-, y- and z-axis respectively, ur_x, ur_y and ur_z denote the rotations about x-, y- and z-axis, respectively.

Displacement loads are applied on the corner nodes. The axial load in the x-, y-, and z-axis directions can be formed by applying displacement on vertex A along the positive x-axis direction, displacement on vertex A along the positive y-axis direction, and displacement on vertex H along the positive z-axis, respectively. The shear load can also be formed by applying displacement on a certain vertex of the unit cell. The shear load on the x–y plane, x–z plane, and y–z plane can be imposed by applying displacement on vertex A along the positive x-axis, displacement on vertex H along the positive x-axis, and displacement on vertex H along the positive y-axis, respectively.

Modeling and simulation

Mechanical properties of composite materials

The prepreg used in this study was made of T700/QY8911-IV with ply thickness of 0.2 mm. The resin-rich region was filled with bismaleimide (BMI) resin QY8911- IV, the elastic modulus and Poisson’s ratio of QY8911- IV were 4.50 GPa and 0.37, respectively. Z-pin was made of T300/NHZP-1 that is a kind of BMI resin developed by Nanjing University of Aeronautics and Astronautics for Z-pin use only. The mechanical properties of the raw materials for prepreg and Z-pin are given in Table 1.

Table 1.

Properties of T700/ QY8911-IV and Z-pin.

	Elastic modulus (GPa)			Shear modulus (GPa)			Poison’s ratio
Components	E_x	E_y	E_z	G_xy	G_xz	G_yz	v_xy	v_xz	v_yz
T700/ QY8911-IV	121.000	9.930	9.930	4.750	4.750	3.500	0.321	0.321	0.436
Z-pin	131.700	8.800	8.800	5.310	5.310	4.000	0.315	0.315	0.400

Unit cell model

The Z-pin parameters that were studied in this work include Z-pin diameter, spacing, and angle. Z-pins with diameters of 0.3 mm and 0.5 mm that are widely used in research were considered.¹ It should be mentioned that for convenience the Z-pin density in this work was defined as Z-pin spacing, i.e. row spacing L or column spacing S, rather than Z-pin volume content presented in most of the literature, as the engineers think it is inconvenient for either understanding or manufacturing if the Z-pin inserting density is defined by volume content in practice. Five different spacings (i.e., L/S) including 5 mm, 4 mm, 3 mm, 2 mm, 1.5 mm were studied (see Figure 5 and Figure 6). The first three spacings were the most widely used ones in the research and 1.5 mm was the allowed minimum spacing during the manufacturing process. Although Z-pin was usually designed to be inserted vertically (inserting angle of 90°), the actually achieved angle was often smaller than 90° due to the instability of inserting process.⁸ The average offset angles for big pins (0.51 mm) and small pins (0.28 mm) were 28° and 14°, respectively.⁸ Therefore, the inserting angles of 90°, 75°, 60° with a difference value of 15° were studied herein.

Figure 5.

FE unit cell models of the composite laminates reinforced with Z-pin with diameter of 0.5 mm: (a) L/S = 5 mm; (b) L/S = 4 mm; (c) L/S = 3 mm; (d) L/S = 2 mm; (e) L/S = 1.5 mm.

Figure 6.

FE unit cell models of the composite laminates reinforced with Z-pin with diameter of 0.3 mm: (a) L/S = 5 mm; (b) L/S = 4 mm; (c) L/S = 3 mm; (d) L/S = 2 mm; (e) L/S = 1.5 mm.

A mesh size of 0.04 × 0.04 mm² and the element type of C3D8I (eight-node linear brick element with incompatible modes) were used for meshing, while only one element was placed in the through-thickness direction. The boundary conditions were imposed automatically through the in-house program. Unit cell models with inserting angles of 60° and 75° could be generated by simply transferring the nodes of the model with the vertically inserted Z-pin. This is also the reason why 3D model rather than 2D model is used.

Benchmark tests

In order to verify the FE unit cell model, benchmark tests were carried out to compare the simulation results of a certain Z-pinned unidirectional laminate with the literature data.^21,22 A unidirectional laminate with Z-pin diameter of 0.28 mm, Z-pin content of 2% (i.e., L = 1.45 mm and S = 2.11 mm, the two values were given in Ref.²¹) and inserting angle of 90° as presented in Ref.²¹ was modeled. As abovementioned, a mesh size of 0.04 × 0.04 mm² and the element type of C3D8I in ABAQUS were used for meshing, while only one element was placed in the through-thickness direction.

The obtained stress distributions of the laminate under different uniaxial loadings, i.e. x-axis tensile, y-axis tensile, z-axis tensile and x–y plane shear, x–z plane shear, y–z plane shear, were presented in Figure 7. As periodic boundary conditions were assigned to the unit cell in the model of this study, stress distributions were periodic.

Figure 7.

Periodic stress distributions of the unidirectional laminate: (a) S₁₁; (b) S₂₂; (c) S₃₃; (e) S₁₂; (f) S₁₃; (g) S₂₃.

Table 2 shows the comparison between the simulation results and literature data. Most of the differences were less than 8%. It should be noted that the difference of υ_xz between this work and Ref.²¹ was approximately 20.8%, while the difference of υ_xz between this work and Ref.²² was only −5.00%. The boundary conditions of the models in Refs.^21,22 were different, which indicates that boundary condition would influence the value of υ_xz. The boundary conditions used in Refs.^21,22 were either uniform displacement boundary conditions or uniform traction boundary conditions, while the boundary conditions used in this study were periodic. In addition, the size in the through-thickness direction was much smaller than that in the longitudinal and transverse directions, the difference of υ_xz and υ_yz would be more significant than υ_xy, accordingly. Moreover, the modeled microstructures (fiber waviness and resin-rich region) in this work and those in Refs.^21,22 may not be exactly the same. The above benchmark tests showed that the unit cell model along with periodic boundary condition in this work can be used to predict the influence of Z-pin on the elastic properties of unidirectional laminates properly. Additionally, the use of periodic boundary conditions would provide more reliable results.

Table 2.

Comparison of FE simulation results in the study with those in Refs.^21,22

Mechanical properties	FE simulation results
Mechanical properties	This study	Ref.²¹	Difference (%)	Ref.²²	Difference (%)
E_x (GPa)	120.34	121.80	−1.20	123.10	−2.24
E_y (GPa)	8.84	8.60	2.80	8.85	−0.11
E_z (GPa)	11.33	11.92	−4.95	11.17	1.43
G_xy (GPa)	5.47	5.81	−5.85	5.80	−5.69
G_xz (GPa)	5.57	5.67	−1.76	5.70	−2.28
G_yz (GPa)	3.09	3.13	−1.28	3.17	−2.52
υ_xy	0.32	0.33	−3.03	0.31	3.22
υ_xz	0.19	0.24	−20.83	0.20	−5.00
υ_yz	0.29	0.27	7.41	0.31	−6.45

Simulation results and discussion

Influence of Z-pin parameters on E_x, E_y, E_z

Figure 8 (a) shows the simulation results of the influence of Z-pin diameter, spacing, and insertion angle on E_x of the composite laminate. Both the insertion of Z-pin with diameters of 0.3 mm (netlike column in Figure 8 (a)) and 0.5 mm (solid column) would lead to an obvious decrease in E_x and the drop is more significant for Z-pin with a larger diameter. The insertion of Z-pin with a larger diameter would increase the defects (i.e., resin-rich region and fiber waviness) introduced into the laminate. The changing trend in E_x against Z-pin spacing is similar for both types of Z-pin as E_x decreases with decreasing Z-pin spacing regardless of Z-pin diameters. When the spacing is 4 mm, the decrease of E_x is less than 10%, e.g. 7.09% and 2.78% for Z-pin with a diameter of 0.3 mm and 0.5 mm, respectively. However, the reduction becomes significant when Z-pin spacing is less than 3 mm. The reason for this is that as the spacing decreases the volume content of resin with poorer properties than original laminate material increases nonlinearly. The eye-shape resin-rich regions are connected and resin-rich channels are formed when Z-pin spacing is smaller than 3 mm for big Z-pin (see Figure 5). Between the two defects, the effect of the resin-rich region should be more significant because the mechanical properties of the resin are much lower than those of the slightly curved fiber. The increasing of the resin-rich region also means the reduction of the fiber volume fraction of the laminate, which would obviously decrease the in-plane mechanical properties of the laminate. In addition, the property of Z-pin along the longitudinal direction of the laminate is also poorer than the laminate. Thus, the decreasing rate of E_x becomes greater and the difference of E_x between the laminates with different Z-pin diameters is getting more and more noticeable as the spacing decreases.

Figure 8.

Influence of Z-pin parameters on E_x, E_y, E_z: (a) E_x; (b) E_y; (c) E_z.

As seen in Figure 8 (a), the insertion angle has a negligible influence on E_x regardless of Z-pin diameter and spacing. This could be attributed to the fact that the volume content of the resin-rich region is the same for laminates with different Z-pin insertion angles. Furthermore, the insertion angle would not change the volume content of fiber waviness region. Although the modulus of Z-pin in the longitudinal direction increases with the decrease of insertion angle, this influence is weak since the volume content of Z-pin is much smaller than that of the resin-rich region with low modulus. When Z-pins with a spacing of 1.5 mm and insertion angle of 90° are embedded into the laminate, E_x would be decreased by 15.68% and 29.32% for small and large Z-pins, respectively.

The influence of Z-pin diameter, spacing, and insertion angle on E_y is shown in Figure 8 (b). The transverse modulus is decreased due to the insertion of Z-pin. The larger pins would lead to a more significant drop in E_y, which is similar to the influence of Z-pin diameter on E_x. The decreasing rate becomes noticeable as the spacing of Z-pin reduces. An obvious reduction of E_y can be found when the spacing is smaller than 3 mm. This changing trend is similar to the influence of Z-pin spacing on E_x. However, unlike the significant drop of E_x, the reduction of E_y is mostly smaller than 10%.

The influence of the insertion angle on E_y is different from that on E_x. The transverse modulus decreases as the insertion angle decreases. The inserted Z-pin with large through-thickness modulus (E_z) would restrict the deformation of the unit cell in the out-of-plane direction. This restriction would cause resistance to the applied load and result in an effective increase in the stiffness along the transverse direction.²² Obviously, the restriction reaches the maximum when Z-pin is inserted vertically. When Z-pins with a spacing of 1.5 mm and insertion angle of 60° are embedded into the laminate, E_y would be decreased by 6.26% and 11.36% for small and large Z-pins respectively, which are approximately 40% and 39% of the decrease of E_x.

Figure 8 (c) shows the changing trend of the through-thickness modulus (E_z) of the laminate. Through-thickness modulus is greatly improved by the insertion of Z-pin, especially for laminate with larger pins. The laminates with larger pins show a relatively higher E_z. The difference of E_z between laminates with small pins and large pins becomes more obvious as Z-pin spacing decreases. This can be ascribed to the fact that the volume content of Z-pin with relatively higher modulus in the through-thickness direction increases nonlinearly with increasing Z-pin diameters. Besides, the modulus of the resin-rich region is not obviously lower than E_z of the original laminate material.

The changing trend of the through-thickness modulus against Z-pin spacing is similar for both types of Z-pin. As the spacing decreases, E_z increases nonlinearly. This can be ascribed to the fact that the volume content of Z-pin with high modulus in the through-thickness direction increases nonlinearly with the decreasing of Z-pin spacing. The increase of E_z tends to be significant when the spacing is lower than 3 mm, which is the same point when E_x and E_y encounter a sharp drop. In addition, the insertion angle would have a potent influence on E_z as the through-thickness modulus of Z-pin decreases when the Z-pin is offset from the vertical direction. When Z-pins with a spacing of 1.5 mm and insertion angle of 90° are embedded into the laminate, E_z would be dramatically increased by 33.43% and 97.18% for small and large Z-pins, respectively.

Influence of Z-pin parameters on G_xy, G_xz, G_yz

The impact of Z-pin diameter, spacing and insertion angle on G_xy is illustrated in Figure 9 (a). Due to the poor shear modulus of the resin, the insertion of both types of Z-pin with a diameter of 0.3 mm and 0.5 mm would lead to the decrease of G_xy and the influence of large pins would be more significant. The change in G_xy with Z-pin spacing is similar for both types of Z-pin and follows a similar tendency of that for E_x against Z-pin spacing. The decreasing rate becomes more noticeable as the spacing of Z-pin reduces. The drop of G_xy seems to be significant when the spacing is less than 3 mm that is consistent with the influence of Z-pin parameters on E_x and can be explained in the same way. Moreover, the impact of the insertion angle on G_xy can be ignored, which is also similar to its influence on E_x. When Z-pins with a spacing of 1.5 mm and insertion angle of 90° are embedded into the laminate, G_xy is decreased by 12.79% and 26.74% for small and large Z-pins that are about 82% and 91% of the reduction of E_x with the same reinforcement for small and large Z-pins, respectively. Therefore, the reduction of G_xy is similar to that of E_x.

Figure 9.

Influence of Z-pin parameters on G_xy, G_xz, G_yz: (a) G_xy; (b) G_xz; (c) G_yz.

Figure 9 (b) depicts the influence of Z-pin parameters on G_xz. Due to the addition of resin-rich region, G_xz is decreased and the reduction is more obvious for G_xz of the laminate reinforced with large pins. Similar to the influence of Z-pin diameter on the above-discussed elastic properties, the difference of G_xz gets more significant with the decrease of Z-pin spacing. In addition, the reduction of G_xz is smaller than that of G_xy. This can be explained by the fact that the inserted Z-pin would improve the shear modulus of the laminate in the x–z plane as the z-direction modulus is significantly improved by the Z-pin. Although the influence of the insertion angle is small, this influence is slightly greater than that on G_xy. This is because Z-pin with an inclined angle would provide less restriction to the shear deformation as Z-pin is defined to be offset from the positive z-axis to the positive x-axis in the x–z plane and the shear load is formed by applying a displacement at vertex H along the positive x-axis. If the load is applied along the negative x-axis, the restriction would be greater. This is the reason why G_xz decreases as the insertion angle reduces. However, as the separated resin-rich regions would connect to form resin-rich channels for laminate reinforced with large Z-pins in a spacing smaller than 3 mm, the stress distribution would change. Therefore, the changing trend of G_xz against insertion angle is inconstant. While resin-rich channel could not be formed in all the laminates reinforced with small pins, the changing trend of G_xz against insertion angle is constant. When Z-pins with a spacing of 1.5 mm and insertion angle of 90° are embedded into the laminate, G_xz would be decreased by 7.68% and 15.4% for small and big Z-pins, respectively. The reduction is about 60% of that of G_xy.

The influence of Z-pin parameters on G_yz is shown in Figure 9 (c), which is decreased due to the presence of resin-rich region. Additionally, the reduction of G_yz is smaller than that of G_xy and is consistent with the reduction of G_xz. This can be explained by similar reasons for G_xz. As Z-pin is offset from the vertical direction in the x–z plane rather than the y–z plane, there is nearly no influence of insertion angle on G_yz_. When Z-pins with a spacing of 1.5 mm and insertion angle of 90° are embedded into the laminate, G_yz would be decreased by 7.31% and 12.57% for small and large Z-pins, respectively. The reduction is comparable to that of G_xz.

Influence of Z-pin parameters on υ_xy, υ_xz and υ_yz

Figure 10 (a) illustrates the influence of Z-pin parameters on υ_xy, which is increased due to the insertion of Z-pin. The transverse deformation of Z-pinned laminate under x-axis loading is increased due to the addition of the soft resin-rich region. However, the deformation restriction would offset the softening, as discussed in Section “Influence of Z-pin parameters on Ex, Ey, Ez”. This restriction increases with the increase of the insertion angle. In addition, Z-pins offset from the vertical direction would contribute to the extra longitudinal modulus of laminate, which would reduce the deformation of the unit cell under x-axis loading and the reduction would become larger as the insertion angle decreases. Obviously, the abovementioned two restrictions have opposite reactions to the change of insertion angle. It can be observed from Figure 10 (a) that υ_xy decreases with the decrease of insertion angle. Therefore, the second restriction shows a dominant influence. When the Z-pin diameter increases and Z-pin spacing decreases, the volume content of Z-pin increases and the difference between the two restrictions would be more significant. This could be used to explain why the difference of υ_xy of the laminates with different insertion angles would become more and more obvious. The dominant effect of the second restriction can also explain why there existed an obvious drop when the spacing is smaller than 3 mm and insertion angle was smaller than 90° for large Z-pin. The restriction from the inclined Z-pin is large enough to offset the increase of υ_xy due to the added resin when the Z-pin spacing decreases from 3 mm to 2 mm. Besides, the transformation from separated resin-rich regions to connected resin-rich channel may also make the changing trend of υ_xy become inconstant. Unlike the changing trend of υ_xy of laminates reinforced with big pins, the change of υ_xy is more consistent for laminate reinforced with small pins.

Figure 10.

Influence of Z-pin parameters on υ_xy, υ_xz, υ_yz: (a) υ_xy; (b) υ_xz; (c) υ_yz.

The influence of Z-pin diameter, spacing, and insertion angle on υ_xz is shown in Figure 10 (b), which decreases with increasing Z-pin diameter and decreasing Z-pin spacing. This can be ascribed to the restraining effect of Z-pin with high through-thickness modulus on the out-of-plane deformation. With the increasing of insertion angle, υ_xz decreases, since the vertically inserted Z-pin could provide larger through-thickness modulus than the inclined Z-pin and thus the deformation restriction is enhanced. The influence of Z-pin parameters on υ_yz is depicted in Figure 10 (c), which showed that the changing tendency is similar to that of υ_xz following the identical mechanism.

Conclusions

In this work, the influence of Z-pin parameters including Z-pin diameter, spacing, and insertion angle on the elastic properties of unidirectional laminates was investigated in a quantitative manner using 3D finite element method. Unit cell models with different Z-pin parameters and periodic boundary conditions were built and used. A series of parametric analyses were performed to estimate the influence of each Z-pin parameter. Based on the findings of this study, the following conclusions could be drawn:

The diameter and spacing of Z-pin have influences on all the elastic properties. In general, with increasing Z-pin diameter and reducing Z-pin spacing, E_x, E_y, G_xy, G_xz, G_yz, υ_xz, and υ_yz decrease while E_z and υ_xy increase nonlinearly.

When the Z-pin spacing is lower than 3 mm, the decrease of E_x, E_y, G_xy, G_xz, and G_yz becomes significant. Therefore, a minimum spacing of 3 mm is suggested to maintain the stability of the elastic properties of the laminate.

Comparing to Z-pin diameter and spacing, the influence of Z-pin insertion angle is relatively smaller. While, the insertion angle has an obvious impact on E_z.

For small and large Z-pins with a spacing of 1.5 mm, E_x can be decreased by up to 15.68% and 29.32%, respectively. The reduction of E_y is approximately 40% of that of E_x, while the increase of E_z could be up to 33.43% and 97.18% for small and large Z-pins, respectively. The reduction of G_xy is similar to that of E_x, while G_xz and G_yz are both reduced by approximately half of the reduction of G_xy.

Footnotes

Declaration of conflicting interests

The author(s) declared no potential conflicts of interest with respect to the research, authorship, and/or publication of this article.

Funding

The author(s) disclosed receipt of the following financial support for the research, authorship, and/or publication of this article: The financial support from the National Natural Science Foundation of China (12002315) and the Natural Science Foundation of Zhejiang Province (LQ20A020003) is gratefully acknowledged.

ORCID iD

Mengjia Li

References

Mouritz

. Review of z-pinned composite laminates. Compos Part A 2007; 38(12): 2383–2397.

Hoffmann

Scharr

. Mode I delamination fatigue resistance of unidirectional and quasi-isotropic composite laminates reinforced with rectangular z-pins. Compos Part A 2018; 115: 228–235.

M’membe

Yasaee

Hallett

, et al. Effective use of metallic Z-pins for composites’ through-thickness reinforcement. Compos Sci Technol 2019; 175: 77–84.

Kadlec

Růzek

Belský

. Concurrent use of Z-pins for crack arrest and structural health monitoring in adhesive-bonded composite lap joints. Compos Sci Technol 2020; 188 (Available online):107967.

Vazquez

Castanié

Barrau

, et al. Multi-level analysis of low-cost Z-pinned composite joints: Part 2: Joint behavior. Compos Part A 2011; 42(12): 2082–2092.

Park

Lee

Kweon

, et al. The strength of composite bonded T-joints transversely reinforced by carbon pins. Compos Struct 2012; 94(2): 625–634.

Koh

Feih

Mouritz

. Experimental determination of the structural properties and strengthening mechanisms of z-pinned composite T-joints. Compos Struct 2011; 93(9): 2222–2230.

Guo

Giannopoulos

, et al. Strength enhancement of bonded composite laminate joints reinforced by composite pins. Compos Part A 2020; 236 (Available online): 111916.

Chang

Mouritz

Cox

. Properties and failure mechanisms of z-pinned laminates in monotonic and cyclic tension. Compos Part A 2006; 37(10): 1501–1513.

10.

Steeves

Fleck

. In-plane properties of composite laminates with through-thickness pin reinforcement. Int J Solids Struct 2006; 43(10): 3197–3212.

11.

Chang

Mouritz

Cox

. Flexural properties of z-pinned laminates. Compos Part A 2007; 38(2): 244–451.

12.

Mouritz

. Compression properties of z-pinned composite laminates. Compos Sci Technol 2007; 67(15–16): 3110–3120.

13.

Hoffmann

Scharr

. Mechanical properties of composite laminates reinforced with rectangular z-pins in monotonic and cyclic tension. Compos Part A 2018; 109: 163–170.

14.

Cui

Melro

Yasaee

. Inter-fibre failure of through-thickness reinforced laminates in combined transverse compression and shear load. Compos Sci Technol 2018; 165: 48–57.

15.

Freitas

Magee

Dardzinski

, et al. Fiber insertion process for improved damage tolerance in aircraft laminates. J Adv Mater 1994; 25: 36–43.

16.

Mouritz

Chang

. Tension fatigue of fibre-dominated and matrix-dominated laminates reinforced with z-pins. Int J Fatigue 2010; 32(4): 650–658.

17.

Mouritz

. Tensile fatigue properties of 3D composites with through-thickness reinforcement. Compos Sci Technol 2008; 68(12): 2503–2510.

18.

Sun

, et al. Tensile Properties of Z-pins Reinforced Laminates. Polym Polym Compos 2011; 19(4): 251–258.

19.

Yan

Wang

, et al. Study on compressive properties of z-pinned laminates in RTD and hygrothermal environment. Chin J Aeronaut 2012; 25: 64–70.

20.

Knopp

Düsterhöft

Reichel

, et al. Flexural properties of z-pinned composite laminates in seawater environment. J Mater Sci 2014; 49(24): 8343–8354.

21.

Grassi

Zhang

Meo

. Prediction of stiffness and stresses in z-fibre reinforced composite laminates. Compos Part A 2002; 33(12): 1653–1664.

22.

Dickinson

. Prediction of effective three-dimensional elastic constants of translaminar reinforced composites. J Compos Mater 1999; 33: 1002–1028.

23.

Pierreux

Hemelrijck

, et al. Evaluation of microdamage initiation in Z-pinned laminates by means of automated RVE computations. Compos Struct 2018; 206: 104–115.

24.

Bianchi

Zhang

. Predicting mode-II delamination suppression in z-pinned laminates. Compos Sci Technol 2012; 72(8): 924–932.

25.

Xia

Zhang

Ellyin

. A unified periodical boundary conditions for representative volume elements of composites and applications. Int J Solids Struct 2003; 40(8): 1907–1921.

26.

Xia

Zhou

Yong

, et al. On selection of repeated unit cell model and application of unified periodic boundary conditions in micro-mechanical analysis of composites. Int J Solids Struct 2006; 43(2): 266–278.

A numerical study of the influence of Z-pin parameters on the elastic properties of laminates

Abstract

Keywords

Introduction

Finite element model

Selection of the unit cell

Fiber waviness and resin-rich region

Periodic boundary condition

Modeling and simulation

Mechanical properties of composite materials

Unit cell model

Benchmark tests

Simulation results and discussion

Influence of Z-pin parameters on Ex, Ey, Ez

Influence of Z-pin parameters on Gxy, Gxz, Gyz

Influence of Z-pin parameters on υxy, υxz and υyz

Conclusions

Footnotes

Declaration of conflicting interests

Funding

ORCID iD

References

Influence of Z-pin parameters on E_x, E_y, E_z

Influence of Z-pin parameters on G_xy, G_xz, G_yz

Influence of Z-pin parameters on υ_xy, υ_xz and υ_yz