Large displacements of fgsw beams in thermal environment using a finite element formulation
Abstract. The large displacements of functionally graded sandwich (FGSW) beams in
thermal environment are studied using a finite element formulation. The beams are composed of three layers, a homogeneous core and two functionally graded face sheets with
volume fraction of constituents following a power gradation law. The material properties of the beams are considered to be temperature-dependent. Based on Antman beam
model and the total Lagrange formulation, a two-node nonlinear beam element taking the
effect of temperature rise into account is formulated and employed in the study. The element with explicit expressions for the internal force vector and tangent stiffness matrix is
derived using linear interpolations and reduced integration technique to avoid the shear
locking. Newton-Raphson based iterative algorithm is employed in combination with
the arc-length control method to compute the large displacement response of a cantilever
FGSW beam subjected to end forces. The accuracy of the formulated element is confirmed
through a comparison study. The effects of the material inhomogeneity, temperature rise
and layer thickness ratio on the large deflection response of the beam are examined and
highlighted.
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Tóm tắt nội dung tài liệu: Large displacements of fgsw beams in thermal environment using a finite element formulation
Vietnam Journal of Mechanics, VAST, Vol.42, No. 1 (2020), pp. 43 – 61 DOI: https://doi.org/10.15625/0866-7136/14628 LARGE DISPLACEMENTS OF FGSW BEAMS IN THERMAL ENVIRONMENT USING A FINITE ELEMENT FORMULATION Bui Thi Thu Hoai1,2,∗, Nguyen Dinh Kien1,2, Tran Thi Thu Huong3, Le Thi Ngoc Anh4 1Institute of Mechanics, VAST, Hanoi, Vietnam 2Graduate University of Science and Technology, VAST, Hanoi, Vietnam 3Phenikaa University, Hanoi, Vietnam 4Institute of Applied Mechanics and Informatics, VAST, Ho Chi Minh city, Vietnam E-mail: thuhoaihus@gmail.com Received: 18 December 2019 / Published online: 20 March 2020 Abstract. The large displacements of functionally graded sandwich (FGSW) beams in thermal environment are studied using a finite element formulation. The beams are com- posed of three layers, a homogeneous core and two functionally graded face sheets with volume fraction of constituents following a power gradation law. The material proper- ties of the beams are considered to be temperature-dependent. Based on Antman beam model and the total Lagrange formulation, a two-node nonlinear beam element taking the effect of temperature rise into account is formulated and employed in the study. The ele- ment with explicit expressions for the internal force vector and tangent stiffness matrix is derived using linear interpolations and reduced integration technique to avoid the shear locking. Newton-Raphson based iterative algorithm is employed in combination with the arc-length control method to compute the large displacement response of a cantilever FGSW beam subjected to end forces. The accuracy of the formulated element is confirmed through a comparison study. The effects of the material inhomogeneity, temperature rise and layer thickness ratio on the large deflection response of the beam are examined and highlighted. Keywords: FGSW beam, total Lagrange formulation, reduced integration, thermal environ- ment, large deflection analysis. 1. INTRODUCTION Large displacement analysis of structures has drawn much attention from researchers since the recent invention of new materials allows structures to undergo large deforma- tion during their service. The finite element method, a powerful tool in solving nonlinear problems, is a preferable choice in dealing with this problem. In the context of finite element analysis, two types of nonlinear formulation for analyzing beams undergoing large displacement, namely the co-rotational formulation [1,2] and the total Lagrange c 2020 Vietnam Academy of Science and Technology 44 Bui Thi Thu Hoai, Nguyen Dinh Kien, Tran Thi Thu Huong, Le Thi Ngoc Anh one [3,4], are the most often used. The main difference between these two formulations is the choice of reference frames, which leads to different expressions of the element for- mulation. Functionally graded materials (FGMs), a new type of composites initiated by Japan- ese scientists in mid-1980 [5], are increasing used to fabricate structural elements for use in severe environment. Investigations on nonlinear behaviour of FGM beam structure have been extensively reported in the last two decades. In this line of works, Kang and Li [6,7] derived the large displacement solutions for cantilever FGM beams subjected to a transverse tip load or a tip moment. The position of the neutral axis has been taken into account in the derivation, which eliminates the axial deformation and bending coupling effect. Kocaturk¨ et al. [8] formulated a total Lagrange formulation for studying large displacement behaviour of FGM beams due to distributed load. Also using the total La- grange formulation, Almeida et al. [9] investigated geometrically nonlinear behaviour of FGM beams under mechanical loads. Levyakov [10, 11] adopted the neutral surface as reference plane to derive the elastic solutions for FGM beams under the thermal loading. Based on the third-order shear deformation beam theory, Zhang [12] derived the consti- tutive equations for studying the nonlinear bending of FGM beams. Nguyen et al. [13–17] derived the co-rotational beam elements for large displacement analysis of FGM beams and frames. The effect of plastic deformation on buckling and nonlinear bending of FGM beams is considered using the finite element method [18,19]. A geometrically exact beam model with fully intrinsic formulation is employed by Masjedi et al. [20] to study the large deflection behaviour of functionally graded beams under conservative and non- conservative loading. With the development of advanced manufacturing methods [21], FGMs can now be incorporated into sandwich construction to improve the performance of structures. Func- tionally graded sandwich (FGSW) structures can be designed to have a smooth variation of material properties, and this helps to avoid the interface delaminating problem as often seen in the conventional sandwich structures. Several investigations, mainl ... 25 −0.25 * (a) (2−1−1), n=3, P =3 (b) (1−2−1), n=3, P*=3 −0.5 −0.5 −1.2 −0.8 −0.4 0 0.4 0.8 1 −1.2 −0.8 −0.4 0 0.4 0.8 1.2 σ /109 (N/m) σ /109 (N/m) x x Fig. 7. Effect of temperature rise on thickness distribution of axial stress at clamped section of FGSW cantilever beam corresponding to a transverse tip load P∗ = 3 Large displacements of FGSW beams in thermal environment using a finite element formulation 55 0.5 0.5 (1−0−1) (1−0−1) (2−2−1) (2−2−1) (1−8−1) (1−8−1) 0.25 0.25 0 z/h 0 z/h −0.25 −0.25 * (a) n=3, ∆T=0, P =3 (b) n=3, ∆T=50K, P*=3 −0.5 −0.5 −1.2 −0.8 −0.4 0 0.4 0.8 1.2 −1.2 −0.8 −0.4 0 0.4 0.8 1.2 9 σ /10 (N/m) σ /109 (N/m) x x Fig. 8. Effect of layer thickness ratio on thickness distribution of axial stress at clamped section of FGSW cantilever beam corresponding to a transverse tip load P∗ = 3 5.3. Roll-up of cantilever beam due to a tip moment The roll-up of a cantilever FGSW beam subjected to a tip moment M is studied in this sub-section. In Figs.9 and 10, the equilibrium paths of the beam are respectively depicted for different values of the temperature rise and the layer thickness ratio. The temperature rise and the layer thickness ratio, as seen from the figures, play an important role on the large displacement behaviour of the beam. The effect of the layer thickness ratio on the response of the beam is more significant in the large displacement region than that of 6 6 * * u* w* u w 5 5 4 4 3 3 Normalized moment 2 Normalized moment 2 (a) n=5, ∆T=50K (b) n=5, ∆T=90K ∆ T=0K ∆ T=0K 1 ∆ T=30K 1 ∆ T=30K ∆ T=60K ∆ T=60K ∆ T=90K ∆ T=90K 0 0 −1.5 −1 −0.5 0 0.5 1 −1.5 −1 −0.5 0 0.5 1 Tip displacements Tip displacements Fig. 9. Equilibrium paths of cantilever FGSW beam under a tip moment for different temperature rise 56 Bui Thi Thu Hoai, Nguyen Dinh Kien, Tran Thi Thu Huong, Le Thi Ngoc Anh 6 6 * * u w u* w* 5 5 4 4 3 3 Normalized moment 2 Normalized moment 2 (a) n=5, ∆ T=50K (b) n=5 ∆ T=90K (8−1−8) (8−1−8) 1 (2−2−1) 1 (2−2−1) (1−3−1) (1−3−1) (1−8−1) (1−8−1) 0 0 −1.5 −1 −0.5 0 0.5 1 −1.5 −1 −0.5 0 0.5 1 Tip displacements Tip displacements Fig. 10. Equilibrium paths of cantilever FGSW beam under a tip moment for different layer thickness ratio 0.4 0.4 0.3 0.3 0.2 ∆T=0K 0.2 w* w* (1−0−1) ∆T=50K (2−1−1) ∆T=90K (1−8−1) * 0.1 (a) (2−1−1), n=2, M*=7 0.1 (b) n=5, ∆T=50K, M =7 0 0 −0.2 −0.1 0 0.1 0.2 −0.2 −0.1 0 0.1 0.2 x/L x/L Fig. 11. Deformed configurations of FGSW beam subjected to a tip moment the temperature rise. The significant influence of the layer thickness ratio on the large displacement behaviour of the FGSW beam can be seen more clearly from Fig. 11, where the deformed configurations of the beam are displayed for M∗ = 7 and different values of the temperature rise and layer thickness ratio. At the applied moment M∗ = 7, the (1-8-1) beam has already rolled up to a circle while the (1-0-1) beam has not yet. Noting that due to the snap-back of the equilibrium paths, the arc-length control method must be employed to trace the paths in Figs.9 and 10. Large displacements of FGSW beams in thermal environment using a finite element formulation 57 6. CONCLUSIONS The large displacement behaviour of FGSW beams in thermal environment has been investigated by a finite element formulation. The beams are considered to be composed of three layers, a homogeneous core and two functionally graded skin layers with the temperature-dependent material properties. Based on the Antman beam model, a first- order shear deformable nonlinear beam element taking the effect of temperature rise into account was formulated in the context of the total Lagrange formulation. The element with explicit expressions for the internal force vector and tangent stiffness matrix has been derived using the reduced integration technique to avoid the shear locking. Using the derived beam element, the large displacement response of a cantilever FGSW beam under the end forces has been computed, and the effects of the material inhomogeneity, temperature rise and layer thickness ratio have been examined. The obtained numerical results reveal that, in addition to the material inhomogeneity, the temperature rise and the layer thickness ratio also play an important role on the large displacement behaviour of the beam. It has been shown that the effect of the layer thickness ratio on the behaviour of the FGSW beams in the large displacement region is more significant than that of the temperature rise. It is necessary to note that though the numerical investigation in the present paper has been carried out for the cantilever beam only, the element formulation formulated herein can be used to analyze the FGSW beams with other boundary con- ditions as well. 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Nonlinear analysis of shear deformable FGM beams resting on elastic foundations in thermal environments. International Journal of Mechanical Sciences, 81, (2014), pp. 195–206. https://doi.org/10.1016/j.ijmecsci.2014.02.020. 60 Bui Thi Thu Hoai, Nguyen Dinh Kien, Tran Thi Thu Huong, Le Thi Ngoc Anh APPENDIX This Appendix presents detail expressions for the nodal forces and the tangent stiff- ness matrices in Eq. (19). The following notations are used s = sin θ¯ , c = cos θ¯, 2 a1 = (sε¯ − cγ¯) , a2 = (cε¯ + sγ¯) , a3 = γ¯ − ε¯ (1 + ε¯) , (23) 2 2 a4 = cγ¯ − s (1 + ε¯) , a5 = sγ¯ + c (1 + ε¯) , a6 = (1 + ε¯) − γ¯ . The internal force vector l l T f = A ε¯ −c − s γ¯ c s γ¯ , f = A κ¯{0 0 1 0 0 − 1}T, a 11 2 2 b 22 l l T f = A ε¯{0 0 1 0 0 − 1}T + A κ¯ −c − s γ¯ c s γ¯ , c 12 12 2 2 (24) l l T f = ψA γ¯ s − c − (1 + ε¯) − s c − (1 + ε¯) , s 33 2 2 (w − w ) (w − w ) T f = 0 − 2 1 N 0 0 2 1 N 0 , T l T l T c2 sc s2 sym. 2 l l l a1 − a2 a3 2 2 4 1 l ka = A 2 2 , (25) l 11 −c −sc − a1 c 2 l − − 2 2 sc s a5 sc s 2 l l l2 l l l2 a − a a − a a a 2 1 2 2 4 3 2 1 2 2 4 3 0 0 0 sym. 1 0 0 1 k = A , (26) b l 22 0 0 0 0 0 0 0 0 0 0 0 −1 0 0 1 Large displacements of FGSW beams in thermal environment using a finite element formulation 61 0 0 s 0 0 s 0 0 −c 0 0 c 0 0 −c 0 0 −c 0 0 −s 0 0 s s c l s c l l l − − (1 + ε¯) − (1 + ε¯) 0 0 γ¯ 0 0 − γ¯ 2 2 2 2 2 2 2 2 2 kc = A12κ¯ + A12 , 0 0 −s 0 0 −s l 0 0 c 0 0 −c 0 0 c 0 0 c 0 0 s 0 0 −s 1 1 l 1 1 l l l s − c − (1 + ε¯) − s c (1 + ε¯) 0 0 γ¯ 0 0 − γ¯ 2 2 2 2 2 2 2 2 (27) s2 −sc c2 sym. 2 l l l a4 a5 a6 2 2 4 ψ l ks = A33 2 2 , (28) l −s sc − a4 s 2 l − 2 − − 2 sc c a5 sc c 2 l l l2 l l l2 a a a − a − a a 2 4 2 5 4 6 2 4 2 5 4 6 0 0 1 sym. 0 0 0 NT k = . (29) T l 0 0 0 0 0 −1 0 0 1 0 0 0 0 0 0
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