Deformation of a sandwich plate under CONWEP blast loading

This example shows how to build better structures that resist blast loads by using the blast loading capability in Abaqus/Explicit.

The following Abaqus features are demonstrated:

applying CONWEP blast loading,
comparing computational results using Abaqus/Explicit and experimental measurements of deformation of sandwich structures under blast loads, and
demonstrating a generic example of a nonlinear analysis of a sandwich structure.

This page discusses:

Application description
Abaqus modeling approaches and simulation techniques
Cases 1–3: Solid plate with shell elements
Cases 4–6: Solid plate with 3D continuum elements
Cases 7–9: Sandwich plate structure
Additional cases
Discussion of results and comparison of cases
Input files
References
Tables
Figures

Application description

Modern structural designs can be used to protect various systems that are vulnerable to large blast loads. Sandwich structures are a particular class of modern structures that could be explored for such applications.

Geometry

Two models are used in this example. One model is the sandwich plate structure described by Dharmasena et al. (2008) and shown in Figure 1. The sandwich structure consists of a square honeycomb core with vertical webs welded to top and bottom plates. The dimensions of the overall sandwich plate structure are 610 × 610 × 61 mm. The sandwich structure lies in the X–Y plane, while the blast source is 100 mm vertically above (along the z-direction) the center of the top plate of the sandwich structure. The top and bottom plates are 5 mm thick, and the square honeycomb core webs are 0.76 mm thick. The spacing between the honeycomb webs is 30.5 mm measured from the midplane.

The second model is a solid plate, which was chosen for comparison with Dharmasena et al.

Materials

The top and bottom plates and honeycomb core of the sandwich structure and the solid plate are all made of a high ductility stainless steel alloy (Al-6XN) comprised of 49% Fe, 24% Ni, 21% Cr, and 6% Mo by weight as described by Nahshon et al. (2007).

Initial conditions

All structures are initially at their undeformed state at 273 K temperature.

Boundary conditions and loading

All the edges of the sandwich structure and the solid plate are fixed. One-quarter of the full plate is modeled, assuming symmetry of the solution.

Interactions

In the sandwich structure the honeycomb web is welded to the inner surfaces of the plates.

Abaqus modeling approaches and simulation techniques

This example demonstrates the usage of CONWEP blast loading using Abaqus/Explicit. This example was chosen based on experiments reported by Dharmasena et al. (2008) that discuss the deformation of a particular sandwich structure and an equivalent solid plate subjected to CONWEP blast loads due to 1, 2, and 3 kg of TNT. The solid plate with equivalent material is presented as a simple example. The solid plate is modeled using shell elements and three-dimensional continuum elements. Finally, the main problem of interest, the sandwich structure described by Dharmasena et al., is analyzed. A tonne-millimeter-second-kelvin unit system was chosen for all simulations.

Summary of analysis cases


Case 1	Solid plate modeled with S4R shell elements under 1 kg TNT blast load.
Case 2	Solid plate modeled with S4R shell elements under 2 kg TNT blast load.
Case 3	Solid plate modeled with S4R shell elements under 3 kg TNT blast load.
Case 4	Solid plate modeled with C3D8R continuum elements under 1 kg TNT blast load.
Case 5	Solid plate modeled with C3D8R continuum elements under 2 kg TNT blast load.
Case 6	Solid plate modeled with C3D8R continuum elements under 3 kg TNT blast load.
Case 7	Sandwich structure under 1 kg TNT blast load.
Case 8	Sandwich structure under 2 kg TNT blast load.
Case 9	Sandwich structure under 3 kg TNT blast load.

Analysis types

Dynamic analysis using Abaqus/Explicit is performed for all cases. Solutions are computed up to 1.5 milliseconds, where no further permanent deformation is observed for all load values.

Materials

The mechanical properties of the steel alloy as described in Nahshon et al. (2007) are specified as follows: Young's modulus of 1.61 × 10⁵ MPa, Poisson's ratio of 0.35, density of 7.85 × 10⁻⁹ metric tons/mm³, and coefficient of expansion of 452 × 10⁶ Nmm/metric tons $\cdot$ K.

A Johnson-Cook model is used to model the elastic-plastic behavior with the following coefficients and constants: $A = $ 400 MPa, $B = $ 1500 MPa, $C = $ 0.045, $n = $ 0.4, $m = $ 1.2, and $\dot{ε_{0}} = $ 0.001 s⁻¹. The transition temperature is 293 K, and the melting temperature is 1800 K.

Initial conditions

The temperature is initialized to 273 K for all nodes in each model.

Boundary conditions

Symmetry behavior is assumed. Only one-quarter of the structure is modeled for all cases, with the center of the plate positioned at the origin of the X–Y plane. The boundaries at $X = 305$ mm and $Y = 305$ mm are fixed for all degrees of motion (ENCASTRE). Symmetry conditions about the x-axis (XSYMM) are applied at the plane $X = 0$ . Similarly, symmetry conditions about the y-axis (YSYMM) are applied at the plane $Y = 0$ .

Loads

The CONWEP blast load is applied on the top surface of the plate. The source of the blast is at a standoff distance of 100 mm vertically above the center of the top surface of the plate. The property of the blast load is specified using the incident wave interaction property and the CONWEP charge property at the model level and the incident wave interaction at the step level.

Analysis steps

Each analysis consists of a single dynamic explicit step.

Output requests

Translational degrees of freedom (UT) are requested at the center of the plate.

Results and discussion

The center displacement after 1.5 milliseconds was monitored to compare each case with experimental results. Single and double precision job execution gave similar results for all cases.

The animation of the deformed plate over the entire time period of 1.5 milliseconds shows large deformations at the center. The plate stabilizes after a few oscillations. Comparison of the total work done history (ALLWK) and the total plastic dissipation history (ALLPD) indicates that most of the work done by the blast load is dissipated in plastic deformation.

Cases 1–3: Solid plate with shell elements

The solid plate model is modeled with shell elements and is subjected to CONWEP blast loading using different charge masses.

Mesh design

The plate surface is discretized using 31 × 31 S4R elements with nine integration points through the thickness of each element.

Boundary conditions

All degrees of freedom including the rotational degrees of freedom are fixed at the $X = L$ and $Y = L$ edges boundaries, where $L = 305$ mm. Symmetry boundary conditions (XSYMM) are applied at the $X = 0$ edge, and symmetry boundary conditions (YSYMM) are applied at the $Y = 0$ edge.

Loads

1, 2, and 3 kg TNT loads are used in Cases 1, 2, and 3, respectively. The blast source is kept at a standoff distance of 100 mm from the midsection of the shell elements.

Results and discussion

The artificial energy history (ALLAE) is significantly lower than the total internal energy (ALLIE), indicating that the solution is trustworthy with minimal artificial effects.

Cases 4–6: Solid plate with 3D continuum elements

The solid plate is modeled with three-dimensional continuum elements and is subjected to CONWEP blast loading using different charge masses.

Mesh design

The plate surface is discretized using 31 × 31 C3D8R elements with five layers of elements through the thickness of the plate.

Boundary conditions

All degrees of freedom including the rotational degrees of freedom are fixed at the $X = L$ and $Y = L$ face boundaries, where $L = 305$ mm. X-symmetry boundary conditions are applied at the $X = 0$ face, and Y-symmetry boundary conditions are applied at the $Y = 0$ face.

Loads

1, 2, and 3 kg TNT loads are used in Cases 4, 5, and 6, respectively. The blast source is kept at a standoff distance of 100 mm from the top surface of the plate.

Output requests

History output of the center deflection at the top and the bottom surfaces of the plate is requested at every increment.

Results and discussion

Similar behavior using C3D8R elements was observed as that observed using S4R elements. The top surface center deflection and the bottom surface center deflection were quite close to each other. The mean of the two values was used to compare the midsection deflection of the solid plate.

Cases 7–9: Sandwich plate structure

The sandwich plate structure is modeled using three-dimensional continuum elements for the top and bottom plates and shell elements for the square honeycomb core and is subjected to CONWEP blast loading using different charge masses.

Mesh design

The plate surface is discretized using 31 × 31 C3D8R elements with five layers of elements through the thickness of the plate. The honeycomb core is meshed using 30 layers of S4R shell elements along the height of the core with five integration points through their thickness.

Boundary conditions

Loads

1, 2, and 3 kg TNT loads are used in Cases 7, 8, and 9, respectively. The blast source was kept at a standoff distance of 100 mm from the top surface of the plate.

Constraints

The edges of the shell elements at the top and bottom of the core are attached to the inner surfaces of the top plate and the bottom plate, respectively, using tie constraints. The shell element edges form the node-based secondary surface to the main plate surfaces. The tie constraint is defined without allowing any adjustments and using the node set of the edges to identify the nodes on the secondary surface that will be tied to the main surface.

Interactions

General contact is specified at the step level, including all exterior surface contact interactions.

Output requests

History output of the center deflection at the top and the bottom surfaces of the plate is requested at every increment.

Results and discussion

The analysis demonstrates significant buckling of the honeycomb webs involving self-contact near the center of the plate, as shown in Figure 2 for the three loading cases. Figure 3 shows the internal view for the 1 kg TNT blast charge case, revealing the deformation of the honeycomb core. It also confirms that tie constraints using node-based surfaces capture appropriately the weld between the webs and the inner surfaces of the plates.

Additional cases

Studies of similar structures using different parameters have been documented in the literature. Alternative material models and loading cases are mentioned here to provide examples for additional analyses. Different material models have been used to simulate the material behavior under such loads. The material model for the following atypical strain-rate hardening (Dharmasena et al., 2008) can be used for simulation of the above cases with user subroutine VUHARD:

σ = {\begin{matrix} E ε, & ε \leq \frac{σ_{Y}}{E} (1 + {(\frac{ε_{p}^{\cdot}}{ε_{0}^{\cdot}})}^{m}) \\ σ_{Y} (1 + {(\frac{ε_{p}^{\cdot}}{ε_{​_{0}}^{\cdot}})}^{m}) + E_{t} (ε - \frac{σ_{Y}}{E} (1 + {(\frac{ε_{p}^{\cdot}}{ε_{​_{0}}^{\cdot}})}^{m})), & ε > \frac{σ_{Y}}{E} (1 + {(\frac{ε_{​_{p}}^{\cdot}}{ε_{0}^{\cdot}})}^{m}) \end{matrix}

The material properties used by Dharmasena et al. and Rathbun et al. (2006) are as follows: Young's modulus of $E = $ 2.00 × 10⁵ MPa, Poisson's ratio of $ν = $ 0.30, density of $ρ = $ 7.85 × 10⁻⁹ metric tons/mm³, yield stress of $σ_{Y} = $ 300.0 MPa, tangent modulus of $E_{t} = $ 2.00 × 10³ MPa, $\dot{ε_{0}} = $ 4916 s⁻¹, and $m = $ 0.154.

In addition, the following approximate loading, which was applied on the sandwich structure described by Dharmasena et al., can be implemented with user subroutine VDLOAD:

p (t) = (p_{s} - p_{a}) (\frac{t_{d} - t}{t_{d} - t_{a}}) e^{- (\frac{t - t_{a}}{θ})} e^{- {(\frac{d}{d_{0}})}^{2}},

where $p_{s}$ is the shock wave pressure (360 MPa), $p_{a}$ is the ambient pressure (0), $t_{d}$ is the time when the shock decays to a value close to zero, $t_{a}$ is the shock arrival time, $d$ is the distance from the center of the plate (in this example, also the origin), and $d_{0}$ is a reference distance of 120 mm. All variable values are chosen based on Dharmasena et al.

Discussion of results and comparison of cases

The Abaqus/Explicit results for the solid plate using the Johnson-Cook model for the steel alloy (Cases 1–6) are shown in Table 1. These results compare well with the experimental results reported by Dharmasena et al. (2008), shown in Table 2, for both the shell and continuum elements with CONWEP blast loading. The Abaqus/Explicit results for the sandwich structure compare within reasonable error with the experimental results. The simulation and experimental results are presented graphically in Figure 4. The solution differs significantly for higher loads, which Dharmasena et al. attribute to boundary conditions. At higher loads, it is likely that the edges of the sandwich panel used in the test arrangement were actually more flexible than the clamped condition used in the Abaqus model, causing differences between the numerical and experimental results. Differences in the results could also be due to debonding of the honeycomb core webs from the top and bottom plates in the experimental setup.

The sandwich structure was modeled for the same CONWEP loading with a different material model. An isotropic bilinear model with an atypical strain-rate hardening used user subroutine VUHARD with the material properties as described in “Additional cases” above. The displacements, shown in Table 3, were found to be much higher than the Johnson-Cook model and the experimental results, probably due to lower yield stress values.

In addition, the solid plate and the sandwich structure were modeled with the Johnson-Cook material model with an approximate loading, as described in “Additional cases” above, with user subroutine VDLOAD. The displacements, shown in Table 4, were found to be lower than the CONWEP blast loading and the experimental results, probably because less work was done on the model by the approximate load over the total time.

Input files

Cases 1–3 Solid plate with shell elements

exa_aco_conwep_sol_1kg.inp: Solid plate model with S4R elements and 1 kg TNT blast load.
exa_aco_conwep_sol_2kg.inp: Solid plate model with S4R elements and 2 kg TNT blast load.
exa_aco_conwep_sol_3kg.inp: Solid plate model with S4R elements and 3 kg TNT blast load.

Cases 4–6 Solid plate with continuum elements

exa_aco_conwep_spl_1kg.inp: Solid plate model with C3D8R elements and 1 kg TNT blast load.
exa_aco_conwep_spl_2kg.inp: Solid plate model with C3D8R elements and 2 kg TNT blast load.
exa_aco_conwep_spl_3kg.inp: Solid plate model with C3D8R elements and 3 kg TNT blast load.

Cases 7–9 Sandwich structure

exa_aco_conwep_snd_1kg.inp: Sandwich structure model with 1 kg TNT blast load.
exa_aco_conwep_snd_2kg.inp: Sandwich structure model with 2 kg TNT blast load.
exa_aco_conwep_snd_3kg.inp: Sandwich structure model with 3 kg TNT blast load.

Additional cases

exa_aco_conwep_snd_vuhard_1kg.inp: Sandwich structure model with user-defined material model and 1 kg TNT blast load.
exa_blast_vuhard.f: User subroutine VUHARD with user-defined strain-rate hardening model.
exa_aco_conwep_sol_vdload_1kg.inp: Solid plate model with user-defined approximate loading equivalent to 1 kg TNT blast.
exa_aco_conwep_snd_vdload_1kg.inp: Sandwich structure model with user-defined approximate loading equivalent to 1 kg TNT blast.
exa_blast_vdload.f: User subroutine VDLOAD with the approximate loading equivalent to 1 kg TNTCONWEP blast load.

References

Dharmasena, K. P., H. N. G. Wadley, Z. Xue, and J. W. Hutchinson, “Mechanical Response of Metallic Honeycomb Sandwich Panel Structures to High-Intensity Dynamic Loading,” Journal of Impact Engineering, vol. 35, pp. 1063–1074, 2008.
Nahshon, K., M. G. Pontin, A. G. Evans, J. W. Hutchinson, and F. W. Zok, “Dynamic Shear Rupture of Steel Plates,” Journal of Mechanics of Materials and Structures, vol. 2–10, pp. 2049–2066, December 2007.
Rathbun, H. J., D. D. Radford, Z. Xue, M. Y. Hu, J. Yang, V. Deshpande, N. A. Fleck, J. W. Hutchinson, F. W. Zok, and A. G. Evans, “Dynamic Shear Rupture of Steel Plates,” International Journal of Solids and Structures, vol. 43, pp. 1746–1763, 2006.

Tables

Table 1. Center deflection computed by Abaqus/Explicit for Cases 1–9.
Model	Charge mass	Center deflection (mm)
Model	Charge mass	Top surface	Midsection	Bottom surface
Solid plate (S4R)	1 kg TNT	–	48.54	–
	2 kg TNT	–	88.38	–
	3 kg TNT	–	109.75	–
Solid plate (C3D8R)	1 kg TNT	–	47.09	–
	2 kg TNT	–	85.72	–
	3 kg TNT	–	108.38	–
Sandwich structure	1 kg TNT	69.15	–	26.15
	2 kg TNT	110.68	–	66.14
	3 kg TNT	141.37	–	96.63

Table 2. Center deflection measurements from experiments.
Model	Charge mass	Center deflection (mm)
Model	Charge mass	Top surface	Midsection	Bottom surface
Solid plate	1 kg TNT	–	37.65	–
	2 kg TNT	–	71.37	–
	3 kg TNT	–	132.94	–
Sandwich structure	1 kg TNT	47.06	–	15.29
	2 kg TNT	98.82	–	53.73
	3 kg TNT	158.04	–	127.45

Table 3. Center deflection computed by Abaqus/Explicit with user subroutine VUHARD.
Model	Charge mass	Center deflection of top surface (mm)	Center deflection of bottom surface (mm)
Sandwich structure with VUHARD	1 kg TNT	96.18	50.74
	2 kg TNT	156.76	114.79
	3 kg TNT	200.03	155.08

Table 4. Center deflection computed by Abaqus/Explicit with user subroutine VDLOAD.
Model	Charge mass	Center deflection (mm)
Model	Charge mass	Top surface	Midsection	Bottom surface
Solid plate (S4R) with VDLOAD	1 kg TNT	–	32.10	–
Sandwich structure with VDLOAD	1 kg TNT	36.31	–	18.89

Figures