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Composite Structures 293 (2022) 115753 Available online 14 May 2022 0263-8223/© 2022 Elsevier Ltd. All rights reserved. Fatigue behavior of laminated composites with embedded SMA wires A.H. Mirzaei, M.M. Shokrieh *, A. Saeedi Composites Research Laboratory, Center of Excellence in Experimental Solid Mechanics and Dynamics, School of Mechanical Engineering, Iran University of Science and Technology, Tehran 16846-13114, Iran A R T I C L E I N F O Keywords: Laminated composites Shape memory alloy wires Progressive fatigue damage Self-heating Thermomechanical constitutive modeling A B S T R A C T Embedding pre-strained shape memory alloy (SMA) wires within laminated composites can enhance their fatigue performance due to pseudoelastic and shape memory effects. In the present research, an experimental program was conducted to investigate the fatigue behavior of carbon/epoxy laminated composites with/without embedded SMA wires. Moreover, a novel fatigue model was proposed to predict the behavior of laminated composites with embedded SMA wires. The model is an integration of three parts. The first part is the progressive fatigue damage model to simulate the fatigue behavior of composites. The second part is the self-heating model for the prediction of the self-temperature rise in laminated composites subjected to cyclic loading. The third part is the thermomechanical constitutive model of the mechanical behavior of the SMA wire. Effects of the stacking sequence, the applied stress level, and the pre-strain level of SMA on fatigue behavior of laminated composites were studied. Good agreement between theoretical and experimental results revealed the ability of the present model. 1. Introduction The shape memory alloys (SMAs), due to their unique thermo- mechanical properties, i.e., the pseudo-elastic (PS) effect and the shape memory (SM) effect, have been vastly utilized in engineering applica- tions [1,2]. The PS behavior of SMAs is defined by their large recover- able strain upon loading. Unlike the conventional alloys, which show plastic behavior under large deformation after a few cycles of loading, SMAs can preserve their elastic behavior and create a large hysteresis loop under cyclic loadings [3]. Moreover, the pre-strained SMAs can produce a compressive recovery force after activation of the system due to their SM effect [4,5]. The generated compressive force can result in crack closure effect [6,7], resistance against damage propagation [8,9], and postponing the final failure in composite laminates [10–12]. Regarding the great reinforcing potential of the SMA wires, they can also be employed in fiber-reinforced composite laminates to improve the fatigue life of the composite structures. So far, a few experimental in- vestigations were conducted to examine improving the fatigue life of the composite materials by SMA wires. Wang et al. [13] studied the fatigue behavior of glass/epoxy composite laminates with embedded SMA wires. They reported that by using SMA wires, the fatigue life of the composite specimens increased by more than two times. Moreover, they found that for unidirectional plies, the position of the wire did not significantly affect the fatigue life enhancement. In another study, Daghash and Ozbulut [14,15] employed SMA wires as reinforcements in a thermoset polymer matrix and studied the tensile and fatigue behavior of the SMA/epoxy composites. They showed that by using SMA wires, the recoverable strain of their polymer upon unloading was improved, and fatigue life enhancement was observed. Shimamoto et al. [16] studied fatigue crack propagation behavior in epoxy matrix composite reinforced with embedded SMA wires. Their results revealed that the generated recovery compressive force in the SMA wires decreased the matrix crack-tip stress intensity, and as a consequence, led to resistance against fatigue crack propagation. Experimental studies are also per- formed on SMA wires reinforced carbon-fiber-reinforced-polymer (CFRP) patches for enhancement of the fatigue life of the composite samples [17–20]. It was demonstrated that CFRP/SMA hybrid patches can enhance the fatigue life of cracked specimens. In the present research, the fatigue behavior of carbon/epoxy lami- nated composites with/without embedded SMA wires was investigated. To the best knowledge of the present authors, there is no model for simulating the fatigue behavior of laminated composites with embedded SMA wires. By integrating three submodels, a novel fatigue model was developed for the simulation of the fatigue behavior of SMA-embedded reinforced laminated composites. The first submodel is the progressive fatigue damage (PFD) model of laminated composites, developed by * Corresponding author. E-mail address: shokrieh@iust.ac.ir (M.M. Shokrieh). Contents lists available at ScienceDirect Composite Structures journal homepage: www.elsevier.com/locate/compstruct https://doi.org/10.1016/j.compstruct.2022.115753 Received 20 August 2021; Received in revised form 21 March 2022; Accepted 8 May 2022 mailto:shokrieh@iust.ac.ir www.sciencedirect.com/science/journal/02638223 https://www.elsevier.com/locate/compstruct https://doi.org/10.1016/j.compstruct.2022.115753 https://doi.org/10.1016/j.compstruct.2022.115753 https://doi.org/10.1016/j.compstruct.2022.115753 http://crossmark.crossref.org/dialog/?doi=10.1016/j.compstruct.2022.115753&domain=pdf Composite Structures 293 (2022) 115753 2 Shokrieh and Lessard [21]. The second submodel is the self-heating model for the prediction of the self-temperature rise in laminated composites subjected to cyclic loading, recently developed by the pre- sent authors [22]. The third submodel is the thermomechanical consti- tutive model of the mechanical behavior of the SMA wire, developed by Liang and Rogers [23]. The SMA wires are embedded into the host laminated composites to investigate their effect on the static strength. Then, the results of the present model were verified by a set of fatigue experiments on carbon/epoxy laminates with different layups and stress levels. 2. Theoretical model The idea of fatigue life enhancement of the laminated composites by using embedded SMA wires is based on employing both pseudoelastic (PS) effect and shape memory (SM) effect of SMA wires. During cyclic loading, the temperature in the laminate is increased due to the self- heating phenomenon. The temperature elevation activates SMA wires and the SM effect generates the recovery force, leading to crack closure behavior, and consequently fatigue life enhancement of the specimen. Also, the PS effect of SMA wires causes a relatively large energy dissi- pation in the specimen, and fatigue life enhancement can be expected. Fig. 1 schematically depicts the procedure of fatigue life improvement by embedding SMA wires in laminated composites due to the SM and PS effects of SMA wires. In the present study, a theoretical model is developed to simulate the fatigue behavior of polymeric laminated composites with embedded SMA wires. The present model consists of three major submodels as follows: 1. The progressive fatigue damage (PFD) model, developed by Shokrieh and Lessard [21] for predicting the fatigue behavior of the host laminated composites, 2. The self-heating model, called the generated-dissipated energy (GDE) model, developed by Mirzaei and Shokrieh [22], for predic- tion of the self-temperature rise in the host laminated composites during the cyclic loading, 3. The nonlinear thermomechanical constitutive model of the me- chanical behavior of the SMA wire during the cyclic loading, developed by Liang and Rogers [23]. Using the PFD submodel, the cycle-by-cycle fatigue behavior of the host laminated composites with arbitrary geometry and layup under complex fatigue loading conditions with/without stress concentration can be analyzed. The second submodel predicts thetemperature rise in composite specimens during the fatigue loading. In this submodel, viscoelastic energy is calculated as the reason for heat generation in the specimen due to the viscoelastic behavior of the polymeric matrix. Then, by applying the heat transfer equations, energy dissipation due to con- duction and convection mechanisms are calculated. Finally, by applying the first law of thermodynamics to these dissipated energies in each cycle of life, the temperature rise is computed. The third submodel simulates the embedded SMA mechanical behavior in laminated composites. The model is capable of calculating the martensite volume fraction, mechanical properties, and generated recovery force in the wires during cyclic loadings. By integration of these three submodels, the behavior of the SMA reinforced composite specimens subjected to cyclic loading was simu- lated. Fig. 2 shows the flowchart of the present model by the integration of three submodels. In the following sections, each modeling step is Fig. 1. The procedure of fatigue life improvement by embedding SMA wires in laminated composites due to the PS and SM effects. A.H. Mirzaei et al. Composite Structures 293 (2022) 115753 3 described in more detail. 2.1. The progressive fatigue damage model In this section, a short explanation of the PFD model for predicting the fatigue behavior of the host laminated composites is presented. For a more detailed explanation of the PFD model, it is recommended that interested readers refer to Refs. [21,24]. The PFD model contains three subsections as the stress calculation, failure analysis, and material degradation that are explained as follows. 2.1.1. Stress calculation To model the fatigue behavior of laminated composites, it is neces- sary to calculate the stresses and strains in the composites precisely [25]. In terms of the simple or complex geometry, loading conditions, and boundary conditions of the specimen, the classical lamination theory (CLT) or the finite element method can be used. In the present study, simple laminated composites with simple loading and boundary condi- tions were studied, therefore CLT was used for the stress analysis. The nonlinear shear stress–strain behavior of the unidirectional ply was considered. 2.1.2. Failure analysis Different failure criteria of composite materials can be used for failure analysis. However, failure criteria capable of detecting the failure modes, such as the modified Hashin failure criteria, are recommended to be used in the PFD model [26]. Five different failure modes, including the fiber in tension or compression, the matrix in tension or compres- sion, and the fiber–matrix shearing failure modes are considered. It must be mentioned that the out-of-plane stresses are not taken into account. 2.1.3. Material properties degradation Material property degradation consists of sudden death and gradual degradation rules, which are considered for both stiffness and strength of each lamina within the composite specimens. In the model, based on failure modes detected by the failure criteria, the relevant mechanical properties of the composite ply should be decreased to a very low value but non-zero to prevent numerical errors, as shown in Table 1. More- over, according to the magnitude of the applied stress as well as the stress ratio in each cycle of loading, the material properties are gradually degraded due to repetitive loading. Eqs. (1) and (2) are proposed for Fig. 2. The flowchart of the present model. Table 1 Sudden death rules for stiffnesses and Poisson’s ratio of composite ply. Modes of failure Stiffnesses and Poisson’s ratio Fiber Tension or Compression [Exx, Eyy, Exy, νxy] → [0.001*Exx, 0.001* Eyy, 0.001*Exy, 0.001*νxy] Fiber-Matrix Shearing [Exx, Eyy, Exy, νxy] → [Exx, Eyy, Eyy, 0.001*Exy, 0.001*νxy] Matrix Tension or Compression [Exx, Eyy, Exy, νxy] → [Exx, 0.001* Eyy, Exy, νxy] A.H. Mirzaei et al. Composite Structures 293 (2022) 115753 4 calculating the gradual degradation of stiffness and strength in each cycle of life, respectively [27,28]. E(n, σ, κ) = ⎡ ⎣1 − ( log(n) − log(0.25) log(Nf ) − log(0.25) )λ ⎤ ⎦ 1/γ (Es − σ εf )+ σ εf (1) R(n, σ, κ) = ⎡ ⎣1 − ( log(n) − log(0.25) log(Nf ) − log(0.25) )β ⎤ ⎦ 1/α (Rs − σ)+ σ (2) where E, R, and n are the stiffness, strength, and number of the cycle, respectively. Also, k is the stress ratio, Es is the static stiffness, Rs is the static strength, εf is the static strain to failure, and α, β, λ, and γ are the material constants which are determined using the experiments. More- over, Nf is the predicted life, which is calculated by the life assessment part of the PFD model. 2.2. Self-heating phenomenon Due to the viscoelastic nature of the polymeric matrix, a self- temperature rise occurs in the host laminated composites under fa- tigue loading. In this section, the generated-dissipated energy (GDE) model, developed by the present authors [22], was employed to predict the temperature rise during cyclic loading. The main parts of this model are briefly explained as follows. 2.2.1. Viscoelastic energy The generated energy in laminated composites due to the viscoelastic nature of the polymeric matrix in each cycle of fatigue loading is calculated by Eq. (3) [29]. Egenerated = ε0σ0 πsinδ 4 (3) where σ0, ε0, and δ0 are the applied stress, applied strain, and lag-phase of the polymeric matrix, respectively. It should be mentioned that the magnitude of δ is determined by dynamic mechanical analysis (DMA) testing of the polymer. 2.2.1.1. Dissipated energy through heat transfer mechanisms. To calculate the dissipated heat energy, the convection and conduction heat transfer mechanisms are considered. Eqs. (4) and (5) are employed to calculate the heat convection and conduction for the laminated composites, respectively. Econvection = hA(Ts − T∞) (4) where h is the heat convection coefficient between the air and the laminated composites, A is the summation of the area of the lateral surfaces of the specimen, Ts is the surface temperature of the specimen, and T∞ is the ambient temperate. Econduction = 2kA dT dx (5) where k is the heat conduction coefficient of the laminate composites, A is the cross-section area of the specimen and dT dX is the temperature gradient in the composite specimen. 2.2.1.2. Temperature rise. After calculating the generated and dissi- pated energies, the variation in the internal energy is calculated by applying the first law of thermodynamics on the laminated composites as follows: ΔU = Egenerated − (Econvection + Econduction) (6) Finally, the temperature rise in each cycle is calculated by Eq. (7): ΔT = ΔU mc = ΔU ρVc (7) where m is the mass, ρ is the density of the material, V is the volume of the laminated composites, and c is the specific heat of the material [22]. 2.3. One-dimensional thermomechanical constitutive equation for SMAs When a mechanically constrained SMA wire with pre-strain is acti- vated by heating, the wire tends to return to its initial shape and consequently generates recovery stress. The recovery stress in the SMA wire is calculated by the following equation, developed by Liang and Rogers [23]: σrec = Y(ξ)Sres 2 { 1 − cos [ aA(T − As) − aA CA σrec ]} (8) aA = π Af − As (9) where Y(ξ), Sres, CA, T, As, and Af are the elastic modulus of the wire, the pre-strain level in the wire, the slope of the stress versus austenitestart temperature phase diagram, the applied temperature, austenite start- and finish-temperatures, respectively. Moreover, the elastic modulus of SMA wires, Y(ξ), is considered as a linear function of the martensitic volume fraction (ξ) according to the following equation. Y(ξ) = EA + ξ(EM − EA) (10) where EA and EM are the elastic moduli of the austenitic and martensitic phases, respectively. Furthermore, the martensite volume fraction of the wires, ξ, for the forward transformation (austenitic to martensitic state) and the reverse transformation (martensitic to austenitic state) are described by Eqs. (10) and (11), respectively. ξ = 1 − ξ0 2 cos [ π Ms − Mf ( T − Mf − σ CM )] + 1 + ξ0 2 (11) ξ = ξ0 2 { cos [ π Af − As ( T − As − σ CA )] + 1 } (12) where martensitic volume fraction at the beginning of the trans- formation, the slope of stress versus martensitic start temperature phase diagram, and the martensitic start and finish temperature are denoted by ξ0, CM, Ms, and Mf, respectively. 2.4. Modeling procedure The in-plane stresses were calculated cycle-by-cycle using the CLT method. According to the proposed model by Hahn and Tsai [30], nonlinear stress–strain behavior for in-plane shear is considered for this analysis. Besides, the bridging micromechanical model [31] is used to calculate stresses and strains in the host laminated composites and SMA wires for calculating the viscoelastic energy and mechanical behavior of SMA wires in each loading cycle. To this end, laminated composite (fiber and matrix) was considered as the first component, and the wire was considered as the second component. Furthermore, the calculated re- covery force of the SMA wires is considered for the next cycle and is subtracted from the total applied load to the SMA-embedded laminated composites. 3. Experiments 3.1. Materials The laminated composite samples were fabricated from carbon fibers (T300 12 K, 200 g/m2) and epoxy resin (ML-506 Bisphenol F) hardened A.H. Mirzaei et al. Composite Structures 293 (2022) 115753 5 by HA-11 (Polyamine) with an 85:15 wt fraction according to the manufacturer datasheet. The embedded SMA wires were NiTi type SMA with a diameter of 0.4 mm supplied by HLMET Co. 3.2. Fabrication of specimens For embedding SMA wires within the laminated composites, a fixture was fabricated. The fixture consists of a base plate and two mobile comb- shaped holders for griping the wires in pre-determined positions. The required pre-strain level was first applied to the SMA wires using a tensile machine. Afterward, the wires were wrapped up between the grips, and the laminated composite plates were fabricated and then placed on the top and bottom of the wires, as demonstrated in Fig. 3. The prepared laminated composite plates were cured at ambient tempera- ture for 7 days. Finally, according to the ASTM D3039 standard, lami- nated composite plates were cut into 250 × 25 mm specimens using a diamond saw. 3.3. Mechanical tests Three categories of experiments were performed in the present research to validate the model: 1. Material characterization tests: The first category of tests consists of both static and fatigue experiments performed for mechanical characterization of composite specimens to obtain material proper- ties of the unidirectional ply. 2. Ultimate tensile strength (UTS) tests: In the second category of tests, laminated composite specimens with/without SMA wires were sub- jected to static tensile tests. 3. Fatigue tests: In the third category of the experiments, laminated composite specimens were subjected to fatigue tests. The static tensile and fatigue tests were performed by the SANTAM SAF-50 machine, equipped with hydraulic grips. All fatigue tests were accomplished at a frequency of 5 Hz under tension–tension mode with a stress ratio of 0.1. Each condition was tested with three times repetition. Moreover, FLIR C2 infrared thermography camera with a temperature range of − 10 ◦C to 150 ◦C, a resolution of 65 × 85 pixels, a sensitivity/ NEDT (noise equivalent differential temperature) of 0.1 ◦C, and accu- racy of ±2% was used to record the surface temperature of the speci- mens during the experiments. Fig. 4 shows the employed experimental setup for fatigue test and temperature monitoring. The static and fatigue tests were performed on carbon/epoxy lami- nated composites with/without SMA wires to validate the results of the proposed model. Effects of different parameters including, layups, stress levels, volume fraction (VF) of SMA wires, and the magnitude of pre- strain in SMA wires on the fatigue behavior of laminated composites are considered. Table 2 presents the test matrix of the conducted experiments. Fig. 3. The fixture for embedding SMA wires in laminated composites (a) alignment of wires (b) laminated composites with embedded wires. Fig. 4. Experimental setup for fatigue test and temperature-rise monitoring. Table 2 The test matrix of the performed experiments. Test Category Type of experiment Specimens Stress level SMA volume fraction Pre- strain level 1 SMA characterization SMA wire, tensile test – – 0 SMA wire, DSC test – – 0 Polymer characterization ML-506 resin, DMA test – 0 – Composites characterization (static) Longitudinal tensile [04] – 0 – Transverse tensile [908] – 0 – Composites characterization (fatigue) Longitudinal tensile [04] 0.60, 0.70, 0.80 0 – Transverse tensile [908] 0.60, 0.70, 0.80 0 – 2 Static Tests [0/907/ SMA]s – 0 – [0/907/ SMA]s – 1% 6% [02/906/ SMA]s – 0 – [02/906/ SMA]s – 1% 6% 3 Fatigue Tests [0/907/ SMA]s 0.65, 0.75, 0.85 0 – [0/907/ SMA]s 0.65, 0.75, 0.85 1% 0 [0/907/ SMA]s 0.65, 0.75, 0.85 1% 6% [02/906/ SMA]s 0.65, 0.75, 0.85 0 – [02/906/ SMA]s 0.65, 0.75, 0.85 1% 6% A.H. Mirzaei et al. Composite Structures 293 (2022) 115753 6 4. Result and discussion 4.1. Result of material characterization tests The characterization experiments were performed based on the test matrix, shown in Table 2, and the results were presented in the following. 4.1.1. Characterization of SMA wires To characterize the transformation temperatures of the SMA wires, the DSC experiment was performed according to the ASTM F2004 standard. The differential scanning calorimetry (DSC) test was con- ducted at a rate of 10 ◦C/min (Mettler-Toledo, LLC, Switzerland) be- tween − 20 ◦C and 120 ◦C. Moreover, mechanical tensile tests on SMA wires were also performed according to ASTM F2516 standard with a 0.3 mm/min rate. The results of the DSC and tensile tests on SMA wires are presented in Table 3. 4.1.2. Characterization of polymer The dynamic mechanical analysis (DMA) experiment was conducted according to the ASTM E1640 standard for the host polymer (ML-506) at the frequency of 5 Hz. The test was operated in tensile mode, specimen size was 20 × 10 × 3 mm, and the temperature range was 20 to 110 ◦C. Fig. 5 depicts the variation of the storage modulus (E’) and loss factor (E“) for the polymer as a function of the applied temperature. 4.1.3. Characterization of unidirectional composites Longitudinal tensile, transverse tensile, and shear experiments were performed on the composite specimens to obtain their strengths and moduli. Table 4 presents the mechanical properties of composite specimens. Moreover, according to the test matrix, shown in Table2, fatigue characterization experiments were also performed on composite speci- mens. Fig. 6 presents the fatigue life (S-N diagram) for composite specimens in the longitude direction, transverse direction, and in-plane shear loading. The gradual stiffness degradation parameters (λ and γ in Eq. (1)) and strength degradation parameters (α and β in Eq. (2)) for the longitudinal Table 3 The SMA wires properties. Elastic properties (GPa) Transformation temperatures (℃) Transformation constants (MPa/℃) EM = 20.78 Mf = 16, Ms = 23 CM = 21.74 EA = 42.00 As = 28, Af = 45 CA = 29.00 Fig. 5. Storage (E’) and loss (E“) moduli of ML-506 at a frequency 5 Hz [22]. Table 4 Mechanical characterization of T300/ML-506 [22]. Magnitudes Denoted by Parameter 82 GPa Ex Tensile modulus 4.9 GPa Ey Transverse modulus 6.2 GPa Exy In-plane shear modulus 0.3 νxy Poisson’s ratio 860 MPa Xt Tensile strength 18.2 MPa Yt Transverse strength 64 MPa Sxy In-plane shear strength 1.204E-8 MPa− 3 α Nonlinearity coefficient 0.25 mm tply Ply thickness 65% vf Fiber volume fraction Fig. 6. The S-N curve of T300/ML-506 with an R-ratio of 0.1 [22]. Table 5 The stiffness and strength degradation constants for T300/ML-506 [22]. Loading λ γ α β Longitudinal 1.611 0.757 5.615e-05 669.3 Transverse 1.561 0.6547 9.6287 0.1255 A.H. Mirzaei et al. Composite Structures 293 (2022) 115753 7 direction and transverse directions are presented in Table 5. 4.2. Results of static tensile tests According to the test matrix shown in Table 2, the effect of the embedded SMA wires on the UTS of laminated composites was studied. The obtained results of the conducted static tests on composite speci- mens with standard deviation (STD) are shown in Table 6. It can be declared that because of the low volume fraction of the embedded SMA wires in the present study, embedding SMA wires in laminated com- posites has neither a strengthening nor weakening effect on the UTS of laminated composites. Table 6 The static strength of laminated composites with/without embedded SMA wires. Layup Tensile strength (MPa) (STD) [01/907]s 116.33 (7) [01/907]s with 1% VF SMA 117.66 (6) [02/906]s 216.66 (11) [02/906]s with 1% VF SMA 213.00 (13) Fig. 7. S-N curves for [01/907]s layup (a) laminated composites without SMA (b) laminated composites with SMA wires (VF = 0.01), without pre-strain (c) laminated composites with SMA wires (VF = 0.01), with 0.06 pre-strain, (d) experimental data. A.H. Mirzaei et al. Composite Structures 293 (2022) 115753 8 4.3. Assessment of the present model and case studies 4.3.1. Model assessment To examine the validity of the present model, a series of fatigue tests were conducted on laminated composites with [01/907]s Fig. 7 com- pares the results of the present model and experimental data for [01/ 907]s laminated composites with/without embedded SMA wires. As shown in this figure, good agreement between the experimental and theoretical results is obtained. For a better comparison, the results of the present model and ex- periments for [01/907]s composites were summarized in Table 7. Both the experimental data and results of the present model confirm that embedding the SMA wires in the host laminated composites increases the fatigue life of [01/907]s composite specimens at the three stress levels. It should be noted that by embedding non-pre-strained wires in laminated composites, according to Eq. (8), no recovery force is gener- ated. Therefore, only the PS effect of wires, which cause dissipating energy, improves the fatigue life. While, for the cases with 0.06 pre- strain, as well as the dissipating energy, a compressive force is also generated that decreases the damage propagation rate of the host laminated composites and consequently increases the fatigue life. As shown in Table 7, it is clear that employing the pre-strained wires, due to the simultaneous existence of the PS and SM effects, a better improve- ment in fatigue life was observed in the comparison of that of the non- pre-strained wires that just present the PS effect. 4.3.2. Recovery force in SMA wires Using the present model, a detailed study on the recovery force in SMA wires embedded in [01/907]s laminated composites was per- formed. Fig. 8 shows the generated recovery force by SMA wires in laminated composites at stress levels of 0.65 and 0.85. As shown in this figure, the evolution trend of the generated recovery force at a stress level of 0.85 (red curve) proceeds in a two-step behavior. At the first few cycles of life, the magnitude of the generated recovery force by SMA wires shows a fast decrease, and then it increases fast for the remaining part of the life. However, the generated recovery force in SMA wires at a stress level of 0.65 (blue curve) has a five-step behavior. At the first few cycles of life, the magnitude of the generated recovery force by SMA wires shows a very slow decrease, followed by a fast increase, then a sharp fall, again followed by a sharp increase, and after that a slow in- crease for the remaining part of the life. The above-mentioned trends can be justified by using the present model and evaluating the stiffness degradation of the host laminated Table 7 The results of the present model and experiments for [01/907]s composites. Stress level Mean value of experimental fatigue life (STD) Predicted fatigue life by the model Improved fatigue life by experiments (%) Improved fatigue life predicted by the model (%) Without SMA 0.65 91,070 (28840) 85,140 – – 0.75 15,320 (7770) 13,710 – – 0.85 1470 (260) 1310 – – With SMA wires (VF = 0.01), without pre-strain 0.65 124,700 (59260) 120,880 36 41 0.75 19,310 (8530) 18,240 26 33 0.85 1730 (770) 1700 19 28 With SMA wires (VF = 0.01), with 0.06 pre-strain 0.65 148,400 (65060) 133,690 62 57 0.75 22,530 (8120) 19,610 47 43 0.85 1990 (910) 1750 35 33 Fig. 8. The generated recovery force of SMA wires in [01/907]s lami- nated composites. Fig. 9. Fatigue behavior of [01/907]s laminated composites at the stress level of 0.85 (a) stiffness degradation (b) self-heating phenomenon. A.H. Mirzaei et al. Composite Structures 293 (2022) 115753 9 composites (that changes the applied stress on SMA wires) and the self- temperature rise phenomenon. For instance, the results of the model show that at the same number of cycles of the sharp fall (blue color curve), the 90-degree layers failed. Therefore, the sharp fall is due to the failure of 90-degree layers. The other trends can also be justified by the model, but to avoid the lengthening are not mentioned here. 4.3.3. Stiffness degradation and self-heating phenomenon Fig. 9a and b show the longitudinal stiffness degradation and self- heating phenomenon for [01/907]s laminated composites at a stress level of 0.85, respectively. As shown in Fig. 9a, a fast longitudinal stiffness degradation occurs during the first cycles. This fast degradation increases the applied stress on SMA wires. According to Eq. (8), it results in a decrease in the amount of the generated recovery force. While, at the same time, the temperature of the laminate is rising due to the viscoelastic behavior of the polymeric matrix (see Fig. 9b). This self-temperature rise, according to Eq. (8), increases the generated recov- ery force by the wires. By increasing the fatigue cycles, the stiffness degradation rate decreases significantly (the slope of the curves in Fig. 9a), and the effect of the self-temperature rise increases the magnitude of the generated recovery force. It should be noted that ac- cording to Ref. [32], SMA wires do not exhibit considerable self-heating behavior during cyclic loading. Hence, the viscoelastic nature of the polymeric matrix is the major reason for the temperature variation in laminated composites with embedded SMA wires. The idea of using self- heating temperature rise of laminated composites to activate SMA wires is practical in laboratory-controlled conditions. However, in real cases for operational structures, wires can be activated by using external sources, such as electrical or thermal excitations. Fig. 10a and b show the longitudinal stiffness degradation and self- heating phenomenon [01/907]s laminated composites at a stress level of 0.65. In comparison with the case of the stress level of 0.85 (Fig. 9b), for the case of the stress level of 0.65 (Fig. 10b), the self-heating Fig. 10. Fatigue behavior of [01/907]s laminated composites at the stress level of 0.65 (a) stiffness degradation (b) self-heating phenomenon. Fig. 11. The applied stress on SMA wires embedded in [01/907]s lami- nated composites. Fig. 12. S-N curves for [02/906]s laminated composites (a) without SMA (b) with SMA wires (VF = 0.01), and 0.06 pre-strain. A.H. Mirzaei et al. Composite Structures 293 (2022) 115753 10 phenomenon starts faster. Therefore, more enhancement in the fatigue life of [01/907]s laminated composites, in comparison with that of [02/ 906]s laminated composites were obtained. 4.3.4. Applied stress on SMA wires Fig. 11 shows the applied stress on SMA wires in [01/907]s laminated composites. As illustrated in this figure, under cyclic loading, the applied stress to SMA wires was increased as a result of the stiffness degradation of the composites. Also, a jump on the curve of the cases with the stress level of 0.65 happened, which is due to the 90-degree plies failure. Fig. 11 shows the good capability of the present model in revealing the detailed mechanisms of failure which cannot be easily observed by experiments. 4.3.5. Effect of the layup of laminated composites The fatigue behavior of [01/907]s laminated composites was studied in detail in the previous section. In here, for considering the effect of the layup of the host laminated composites on the results, [02/906]s lami- nated composites were subjected to fatigue tests at three different stress levels. Fig. 12a and b present the experimental and theoretical results of the specimens with and without embedded SMA wires. Table 8 sum- marizes the results of the present model and experimental data of [02/ 906]s laminated composites. By comparing the results obtained for [01/ 907]s and [02/906]s laminated composites, it can be concluded that embedding SMA wires in [01/907]s laminated composites leads to better enhancement in fatigue life at both stress levels of 0.65 and 0.85. The magnitude of stiffness of [02/906]s laminated composites is higher than that of [01/907]s laminated composites. Therefore, the ratio of the stiffness of SMA wires to the stiffness of [01/907]s laminated composites is higher. It means that SMA wires are more effective in improvement of the fatigue life of laminated composites with lower stiffness. 4.3.6. Effect of some other parameters In this section, the effects of SMA pre-strain, modulus, and volume fraction (Vf) of SMA wires on the fatigue life of [01/907]s layup are evaluated. Table 9 exhibits the modeling results for the aforementioned factors. The studied cases were consisted of decreasing the magnitude of pre-strain from 0.06 to 0.02, increasing the VF of SMA wires from 0.01 to 0.04, and increasing the SMA wires modulus by 1.5 times. It is deter- mined that variation in Vf of SMA wires has a significant effect on the fatigue life improvement so that by embedding more SMA wires, fatigue life improvement increases dramatically for both load levels considering in this study. For this case, for example, by increasing the Vf of SMA wires to 0.04, at the loading level of 0.65 and 0.85 UTS, the life improvement increases by 372% and 168%, respectively. 5. Summary and conclusion In the present research, an experimental program was conducted to study the fatigue behavior of the carbon/epoxy laminated composites with/without embedded SMA wires. Also, a novel model was developed to simulate the fatigue behavior of laminated composites with embedded SMA wires. The present model was developed by integrating three submodels a) the PFD model for predicting the fatigue behavior of the host laminated composites, b) the GDE model to simulate the self- temperature rise in laminated composites, and c) the Liang and Rogers nonlinear thermomechanical constitutive model for prediction of the mechanical behavior of SMA wires. Then, the present model was verified by conducting an experimental program on carbon/epoxy composites with/without SMA wire for [01/ 907]s and [02/908]s layups at different fatigue stress levels (0.65, 0.75, and 0.85), 0.01 vol fraction of SMA wires, and 0.06 pre-strain induced in SMA wires. The results show that: • The ratio of the stiffness of SMA wires to the stiffness of the host laminated composites plays a critical role in the fatigue life improvement of laminated composites. By increasing this ratio, both PS and SM effects (dissipating a part of the applied energy and generating a recovery force) of embedded SMA wires are enhanced. • By embedding the SMA wires in [01/907]s laminated composites with 0.01 VF of SMA, and 0.06 pre-strain, at stress levels of 0.65 and 0.85, the fatigue life was improved by 62% and 35%, respectively. • By embedding the SMA wires in [02/906]s laminated composites with 0.01 VF of SMA, and 0.06 pre-strain, at stress levels of 0.65 and 0.85, the fatigue life was improved by 23% and 12%, respectively. • Embedding of SMA wires in laminated composites with lower stiff- ness and strength causes a greater improvement in fatigue life. It means that the magnitude of generated recovery force by the embedded wires becomes more effective. • A good agreement between theoretical and experimental results revealed the ability of the present model in predicting the fatigue behavior of laminated composites with embedded SMA wires. Declaration of Competing Interest The authors declare that they have no known competing financial interests or personal relationships that could have appeared to influence the work reported in this paper. Acknowledgments The authors would like to thank the Iran National Science Founda- tion (INSF) for the Grant numbers 97024007 and 98005981. Table 8 The results of the present model and experiments for [02/906]s composites. Stress level Mean value of experimental fatigue life (STD) Predicted fatigue life by the model Improved fatigue life by experiments (%) Improved fatigue life by the model (%) Without SMA 0.65 209,100 (67520) 253,340 – – 0.75 32,530 (9260) 31,730 – – 0.85 3520 (1580) 3940 – – With SMA wires (VF = 0.01), with 0.06 pre-strain 0.65 256,900 (64260) 298,700 23 18 0.75 37,980 (17030) 36,030 17 13 0.85 4010 (1720) 4270 12 9 Table 9 Influence of the SMA wire pre-strain, Vf of SMA wire, and modulus on fatigue life of [01/907]s layup. Stress level (UTS( Life (cycles) Life by decreasing SMA wire pre-strain (from 0.06 to 0.02) Life by increasing VF of SMA wire (from 0.01 to 0.04) Lifeby increasing SMA wire modulus (SMA modulus £ 1.5) 0.65 133,690 132,010 623,940 189,060 085 1750 1730 4630 2240 A.H. Mirzaei et al. Composite Structures 293 (2022) 115753 11 References [1] Jani JM, Leary M, Subic A, Gibson MA. A review of shape memory alloy research, applications and opportunities. 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