Next Article in Journal
Aging and Curing Temperature Effects on Compressive Strength of Mortar Containing Lime Stone Quarry Dust and Industrial Granite Sludge
Previous Article in Journal
Recovery of Silver Using Adsorption Gels Prepared from Microalgal Residue Immobilized with Functional Groups Containing Sulfur or Nitrogen
 
 
Search for Articles:
Title / Keyword
Author / Affiliation / Email
Journal
Article Type
 
 
Advanced Search
 
Section
Special Issue
Volume
Issue
Number
Page
 
Journals
Materials
Volume 10
Issue 6
10.3390/ma10060638
materials-logo
Submit to this Journal Review for this Journal Propose a Special Issue
► Article Menu

Article Menu

share Share announcement Help format_quote Cite question_answer Discuss in SciProfiles thumb_up
...
Endorse textsms
...
Comment
first_page
settings
Order Article Reprints
Font Type:
Arial Georgia Verdana
Font Size:
Aa Aa Aa
Line Spacing:
Column Width:
Background:
Article

In Situ Imaging during Compression of Plastic Bonded Explosives for Damage Modeling

by
Virginia W. Manner
1,
John D. Yeager
1,*,
Brian M. Patterson
2,
David J. Walters
3,
Jamie A. Stull
1,
Nikolaus L. Cordes
2,
Darby J. Luscher
3,
Kevin C. Henderson
2,
Andrew M. Schmalzer
1 and
Bryce C. Tappan
1
1
Explosive Science and Shock Physics Division, Los Alamos National Laboratory, Los Alamos, NM 87545, USA
2
Materials Science and Technology Division, Los Alamos National Laboratory, Los Alamos, NM 87545, USA
3
Theoretical Division, Los Alamos National Laboratory, Los Alamos, NM 87545, USA
*
Author to whom correspondence should be addressed.
Materials 2017, 10(6), 638; https://doi.org/10.3390/ma10060638
Submission received: 4 May 2017 / Revised: 30 May 2017 / Accepted: 7 June 2017 / Published: 10 June 2017
(This article belongs to the Section Advanced Materials Characterization)
Browse Figures
Versions Notes

Abstract

:
The microstructure of plastic bonded explosives (PBXs) is known to influence behavior during mechanical deformation, but characterizing the microstructure can be challenging. For example, the explosive crystals and binder in formulations such as PBX 9501 do not have sufficient X-ray contrast to obtain three-dimensional data by in situ, absorption contrast imaging. To address this difficulty, we have formulated a series of PBXs using octahydro-1,3,5,7-tetranitro-1,3,5,7-tetrazocine (HMX) crystals and low-density binder systems. The binders were hydroxyl-terminated polybutadiene (HTPB) or glycidyl azide polymer (GAP) cured with a commercial blend of acrylic monomers/oligomers. The binder density is approximately half of the HMX, allowing for excellent contrast using in situ X-ray computed tomography (CT) imaging. The samples were imaged during unaxial compression using micro-scale CT in an interrupted in situ modality. The rigidity of the binder was observed to significantly influence fracture, crystal-binder delamination, and flow. Additionally, 2D slices from the segmented 3D images were meshed for finite element simulation of the mesoscale response. At low stiffness, the binder and crystal do not delaminate and the crystals move with the material flow; at high stiffness, marked delamination is noted between the crystals and the binder, leading to very different mechanical properties. Initial model results exhibit qualitatively similar delamination.

Graphical Abstract

1. Introduction

Octahydro-1,3,5,7-tetranitro-1,3,5,7-tetrazocine (HMX) is a powerful high explosive that is routinely used in a variety of plastic bonded explosive (PBX) formulations such as PBX 9501. Many HMX-based PBXs are highly loaded (10% or less binder) and exhibit bimodal or trimodal particle size distribution in the size range of single to hundreds of micrometers. In addition to safety considerations, PBXs are difficult to characterize from a materials science standpoint because they are relatively fragile and often have low melting points, poor optical or X-ray contrast between the crystals and the binder, and extensive intermixing of constituents. However, the microstructure of PBX materials is known to directly influence fracture behavior [1,2], mechanical properties [3,4], and thermal properties [5,6]. Microstructural behavior is also believed to strongly affect the initiation process, particularly in off-normal scenarios such as cook-off or oblique impact/skid testing [7,8]. For example, microstructure-based effects such as binder thermal expansion and ventilation pathways through the material have been shown to influence time-to-ignition in cook-off of PBX 9501 [9]. Advancing our current understanding of these links between the PBX microstructure and properties is hindered by the difficulty of characterizing the PBX at the mesoscale and would be greatly benefited by systematic, mesoscale experiments coupled with robust model development.
PBX 9501 is widely studied due to its use in a variety of critical applications, and has an extensive amount of historical experimentation data [10,11,12,13]. Mesoscale model development is critical to understanding this treasure trove of data. Currently, models are hindered by a lack of precise microstructural characterization, particularly for in situ measurements during mechanical deformation. Critical information such as crystal-binder adhesion, crystal movement during deformation, and void or crack nucleation and growth are generally only known (if at all) by measurements on bulk specimens [14], by surface-only measurements [15], or by post-test characterization [16]. Three-dimensional microstructural data can be acquired during deformation by in situ imaging such as X-ray computed tomography (CT), but the HMX and the polymer binder have similar density and the X-ray contrast is not sufficient to segment the two phases from each other.
To address this difficulty, we have formulated a series of HMX-based PBXs using lower-density binders which will allow for microCT characterization. Specifically, we have prepared formulations with 88% HMX using hydroxyl-terminated polybutadiene (HTPB) binder in order to form an explosive that is relatively insensitive to mild stimuli, analogous to PBXN-110 [17], differing primarily in the use of dioctyladipate (DOA) as a plasticizer. A particle size distribution of 75% coarse Class 1 HMX and 25% fine Class 2 HMX was used here, which is identical to the distribution found in PBX 9501 [18]. Small changes were made to the mechanical stiffness of the binder system in order to determine how rigidity plays a role in damage of the composite explosive. The HMX content here is much lower than PBX 9501 (95% HMX) and so a direct comparison between the materials must be done with caution, but the characterized microstructure should still provide insight into general PBX damage mechanisms and the relative effects of binder strength and crystal-binder adhesion. Although microCT imaging during compression has been performed in similar non-explosive materials [19,20], this is the first methodical study we are aware of to directly demonstrate the importance of the binder system using explosive samples.

2. Materials and Methods

Coarse HMX (Class I) and fine HMX (Class II) were produced by Holston Army Ammunition Plant (HAAP, Kingsport, TN, USA). MDI/Isonate (diphenylmethane diisocyante; Isonate 143-L MDI) and lecithin were obtained from Firefox Enterprises (Pocatello, ID, USA), and dibutyl tin dilaurate from TCI America (Portland, OR, USA). HMX, HTPB, and DOA were dried overnight in a vacuum oven at 60 °C.
Four formulations were prepared and tested in this work. Two formulations were comprised of 88% HMX, 5.4% HTPB, 5.4% DOA, 0.7% lecithin, and trace dibutyltin dilaurate as a catalyst. Figure 1 shows the chemical structures of these formulations. Two different levels of diphenylmethane diisocyanate (isonate) were used to cure the HTPB and form a polyurethane binder system surrounding the HMX crystals. Here, these are simply labeled “L” (low isonate; 0.5%) and “H” (high isonate; 1%).
The other two formulations used HMX bound with various mixtures of glycidyl azide polymer (GAP) cured with a commercial blend of acrylic monomers/oligomers (AMO) capable of cycloaddition with the azide functionality on the GAP. The four formulations are shown in Table 1. Both binder systems are cast-curable, which offers greater flexibility in the preparation of samples than the traditional slurry-formulated materials. This flexibility enabled simple but precise variations in the mechanical properties of the binders in order to study the resulting effects in the composite. However, one drawback is that sample preparation with highly uniform dimensions can be difficult, a result which is discussed in the next section.
To prepare CF75H, fine HMX (1.1 g) was mashed with a Teflon plunger to remove clumps, and mixed well with course HMX (3.3 g). HTPB (0.27 g), DOA (0.27 g), lecithin (0.035 g), MDI/Isonate (0.051 g), and trace dibutyltin dilaurate were mixed together well in an aluminum pan. The HMX was then added to the liquid mixture, and mixed with a spatula and gloved hands to ensure that the formulation was well mixed. The mixture was placed in a small plastic container and alternated through vacuum mixing and a centrifuge. The formulation was allowed to cure overnight. CF75L was prepared using the same method, but with 0.027 g isonate to reduce the rigidity of the binder system. See Table 1 for variations in the amount of isonate and ratio of HMX coarse/fine. After curing, small ~5 mm diameter cylinders were prepared using brass cork borers.
CF75-AMO1 and CF75-AMO2 were hand mixed on a 2 g scale using the quantities listed in Table 1. After mixing, the materials were packed well into 5–7 mm diameter straws, irradiated with UV-light, and allowed to cure overnight before cutting open the straws. They were cut into 7–10 mm lengths using a blade to shave the ends to be as flat as possible.
Uniaxial compression tests were conducted remotely on an Instron 8862 (Instron Corp., Norwood, MA, USA). Individual samples were prepared from the formulations by boring cylinders approximately 7 mm diameter × 8–11 mm height. Tests were conducted in position control and the strain was measured using the displacement of the crossheads of the instrument. All specimens were tested at ambient conditions and the crosshead speed was varied around the 0.1 in/min value according to the actual specimen height to give a strain rate for all tests of 0.0045 in/in/s.
Micro X-ray CT images were collected using an Xradia Carl Zeiss X-ray Microscopy Inc. MicroXCT (Pleasanton, CA, USA). The system uses a microfocused X-ray source with a tungsten anode. The source was operated at 40 kilovolts potential (kVp) and 10 W·A scintillator converts the X-ray photons to visible light photons and is mounted on the front of the 4× magnification objective which then transmitted the optical photons to the 1 k × 1 k piezo electrically cooled charge-coupled device (CCD). With an individual exposure time of 20 s, the 2001 images were collected as the sample was rotated 180°. These conditions produced an isotropic voxel size of 5.2 micrometers at the sample. The images were reconstructed using TXM reconstructor (Carl Zeiss X-ray Microscopy Inc., Pleasanton, CA, USA) and rendered and quantified using Avizo (FEI, Hillsboro, Oregon, USA). The images were smoothed with an edge-preserving filter and segmented based upon the gray-scale values and the crystals, binder, and voids were separated and quantified. In situ CT imaging of the composites during loading was completed using a Deben CT500 500N loadcell (Deben UK LTD., London, UK).

3. Results and Discussion

3.1. Mechanical Testing of HMX Formulations

Stress-strain data was collected for each formulation in the uniaxial compression configuration. The CF75L specimens had an average density of 1.566 ± 0.067 g/cm3, CF75H specimens had a density of 1.572 ± 0.148 g/cm3, the CF75-AMO1 specimens had a density of 1.649 ± 0.086 g/cm3, and the CF75-AMO2 specimens had a density of 1.680 ± 0.086 g/cm3.
Figure 2 shows the compression stress-strain data for all four specimens. In general the CF75L and CF75H specimens have much lower strength than the CF75-AMO specimens. The CF75L specimens exhibited low strength and significant plastic flow during uniaxial compression; only at the very end of the tests did the edges of the material start to tear. The CF75H specimens registered higher strength than the CF75L specimens, which is expected due to the higher isonate content. The CF75H specimens also deformed elastically compared to the CF75L specimens that failed plastically, with little to no recovery observed after the load has been removed. In contrast, the CF75-AMO specimens exhibited very brittle failures that were not observed for the HTPB-bonded formulations. These specimens had much higher compressive strength and more extensive fracture compared to the softer CF75L and CF75H materials during uniaxial compression.
The CF75-AMO samples did not have good reproducibility so additional samples were tested, five samples in total for each. It is clear from Figure 2b that the stronger more brittle CF75-AMO materials are more sensitive to the geometry of the cylinders. Since the samples were not precisely machined, the uneven surfaces lead to larger spread in the compression data. In some cases this leads to point loading on the sample, which is observed as sharp peaks in the data, or what appears to be a change in the modulus. Here it is clear that making conclusive statements about the differences between the AMO samples is not possible due to the range of responses. The general behavior between them is similar.
The maximum or ultimate stresses of the specimens are plotted as a function of density in Figure 3 and compared to PBXN-110 [17]. The error bars represent the standard deviation measured for the density and the ultimate stress reached for each formulation. The compression strength of the CF75L and CF75H materials compare well to PBXN-110 although the density of PBXN-110 is closer to the CF75-AMO specimens.

3.2. In-Situ Tomography during Compression

Samples of each formulation were sequentially 3D imaged using CT with an in situ load stage during compression. Each sample was compressed to identical engineering strain (10% and 20% displacement of the total sample height, or ε = 0.1 and ε = 0.2). They were held for 10−15 min after compression to allow any residual plastic flow to occur, then imaged at this strain [21,22]. Each full 3D measurement required approximately 26 h.
The CF75L sample was found to be quite ductile and to exhibit a strong plastic flow during uniaxial compression, leading to a large Poisson effect but little cracking or separation of the binder from the crystals. However, CF75H was much more rigid and with delamination between the binder and crystals widely seen. The separation between the crystals and binder is not uniform throughout the cylinders. Reconstructed slices out of the full 3D data set for CF75L and CF75H at 0%, 10%, and 20% strains are shown in Figure 4.
The effect of increased curing via increased isonate is evident in the difference in deformation behavior between samples CF75L and CF75H. A selected region from Figure 4 is highlighted across several compression strains in Figure 5 for both materials. Individual crystals can be tracked during compression, showing increased separation from each other as the material deforms. The images were taken at the same location in the experiment reference frame (i.e., same physical x-y-z coordinates inside the instrument) but the material deforms slightly non-uniformly and so individual crystals move in or out of the single reconstructed slice during the compression. However, most of the crystals can be found in the majority of the images and this is sufficient to observe material motion, rotation of crystals, crystal damage, and void and/or crack nucleation and growth. In CF75L no fracture is evident even up to 20% strain, and the only changes in the microstructure are due to material motion. The binder is either soft or adhesive enough to the crystals to flow with them as they respond to the compressive stress. However, CF75H exhibits extensive crack formation at the crystal-binder interfaces. At 20% strain, most of the crystals have at least one surface debonded from the HTPB matrix.
Both of the CF75-AMO binder specimens show increased adhesion between the crystals and the binder. Due to the higher density of the CF75-AMO mixtures compared to HTPB, the contrast between the HMX and the binder is diminished. However, some trends are readily apparent. Figure 6 shows compression of CF75-AMO1 and CF75-AMO2. In CF75-AMO2, an “X” pattern of fracture is apparent in the reconstructed slice, demonstrating a conical failure which is typical of brittle materials. In CF75-AMO1, cracks form and extend primarily along the direction of compression in a transgranular fashion. These observations are more easily concluded via Figure 7, which highlights a selected area of the microstructure within the 20% strain tomogram for each material. The “X” pattern can be seen primarily along ~45° directions relative to the compression direction and is formed by crystals fracturing (transgranular) and delaminating from the binder (intergranular).
One particularly useful observation from the CT is that the microstructural response of the two AMO specimens are completely different, but the overall mechanical properties (cf. Figure 2) are similar. This indicates that changing the ratio of GAP and AMO more strongly affects the interfacial adhesion between HMX and the binder than the stiffness of the binder. Both effects are interlinked but the change from intergranular (CF75-AMO1) to mixed inter- and transgranular (CF75-AMO2) failure demonstrates a clear change in adhesive properties. Further quantification is beyond the scope of the present study but could help explain large differences in sensitivity or explosive properties in other PBXs which otherwise have similar mechanical properties [23].

3.3 Automated Microstructural Description from the CT Data

For CF75L and CF75H, excellent X-ray contrast was seen between the HTPB, the HMX crystal, and voids, allowing for image analysis software to clearly segment each constituent and therefore quantify measurements of each. Table 2 gives the percent volume and mass for the HMX crystals, binder, and voids in each of the samples as calculated by the segmentation routine. Note that the calculated HMX content is slightly below the measured formulation mass percentage. This is likely due to the moderate amount of HMX crystals smaller than 10 microns, which is approximately the resolution of the CT instrument. However, the fact that the majority of the HMX can be automatically segmented is important, as most X-ray tomography studies of PBX materials have given poor contrast between the crystals and binder to date. As a result of this, it is possible to create 3D renderings of the crystals in which each crystal is colored by its equivalent diameter (Figure 8). The equivalent diameter measurement assumes each object is a sphere and calculates its diameter. Additionally, it is possible (not shown) to measure the changes in crystal and void sizes as a function of the strain [24]. The dataset is sufficient to track the debonding behavior of a large single crystal within the matrix as a function of compression. CF75-AMO1 and CF75-AMO2 also give reasonable contrast between the crystals and binder by eye but the absolute contrast was not sufficient for the software routines to segment them. Note that this weaker contrast is why the microstructure in Figure 6 is less apparent than in Figure 4.
The quality of the contrast in the CF75L and CF75H systems is such that digital image correlation (DIC) could be used in future efforts to map the local strain fields, as in Croom et al. [25,26]. This could also be used to track the rotation of the crystals within the binder. Some of the larger crystals visible in Figure 5 appear to be rotating, not just translating, under the applied compressive load. This type of problem has been treated recently by Yang et al. [27] who established a theoretical framework to predict arbitrarily shaped particles rotating within a soft matrix under a remote stress. Such a theoretical approach could be linked with the particle imaging capability shown here to validate simulations of material deformation.

3.4. Application to Mesoscale Modeling

This type of data is critical to constructing and simulating real three-dimensional microstructures for mesoscale modeling. A primary objective for this mesoscale modeling effort is to simulate quasistatic compression of PBX 9501 specimens, which have even less contrast between the HMX and the binder than the CF75-AMO samples due to the higher density of the binder. However, by substituting in a low-density binder such as HTPB, while retaining an HMX particle size distribution representative of PBX 9501, a realistic, 3D, voxelized microstructure can be measured with microCT and then meshed for a finite element simulation. Additionally, utilizing a close representation of the actual microstructural geometry rather than an idealized statistical representation (i.e., random spheres, circles, etc.) is a critical component in simulating realistic mechanical responses [28]. Ideally, the simulation parameters would be validated by direct comparison to force-displacement data and the well-characterized microstructure, e.g., Figure 4. The simulation could then be applied to PBX 9501 by duplicating the initial microstructure from the HTPB samples while altering the binder properties to match those of the PBX 9501 binder.
While it is recognized that a three-dimensional (3D) description of the material geometry and associated deformation and stress states within the microstructure are critical for accurate quantitative descriptions of damage evolution in explosive materials, there is much utility in two-dimensional (2D) simulations towards that ultimate goal. For example, Arora et al. have conducted 2D and 3D simulations of explosives that explicitly include microstructure geometry [29]. While their 3D simulations employed only an idealized representation of the actual geometry (e.g., spherical particles), their 2D simulations clearly demonstrated the importance of accurately representing the actual crystallite geometry. Barua et al. have developed a cohesive finite element modeling (CFEM) approach based on 2D plane strain simulation of microstructural volume elements of polymer bonded explosives and demonstrated its utility within a framework to investigate the spatiotemporal distribution of hotspot formation during dynamic loading conditions [30,31,32]. While their simulations included an accurate 2D description of microstructure geometry, it did not include anisotropic thermoelastic behavior of the explosive crystals which may be important for capturing local stress distributions that drive the decohesion of the crystal and binder. Hu et al. have used 2D simulations to evaluate the debonding of HTPB binder from ammonium perchlorate (AP) particles and compared them with corresponding experiments to validate a CFEM approach [33]. Gonthier’s group has developed a coupled FEM-discrete element modeling (FEM-DEM) approach to identify energy dissipation and hotspot generation in microstructure simulations that are used to inform macroscale models of explosive response [34,35,36]. The 2D modeling employed in this research is a pre-cursor to guide the judicious development and use of 3D models. By assessing the consistency between qualitative trends from such 2D simulations and the truly 3D experiments, this research will narrow the scope for continued 2D and 3D model development towards predictive capabilities of damage initiation and progression to failure in PBXs.
The full details of such mesoscale modeling approaches are beyond the scope of this paper, but below we provide a brief overview of the treatments applied here. Figure 9 shows a 2D meshed representative volume element (RVE) reconstructed from the segmented microstructures provided by the microCT. Here, the segmented image is sieved to remove segmented particles containing fewer than 5 pixels. Contour detection algorithms based on Python’s OpenCV package [37] were used to convert the segmented HMX grains into a meshable geometry. A finite element mesh of the RVE was generated using Sandia National Laboratories’ CUBIT application [38]. The prescribed meshing routines produce a highly ordered quadrilateral mesh with refined detail around the HMX grain boundaries as seen in Figure 9. A thin layer of cohesive elements placed between regions of HMX and HTPB enable simulation of the progressive debonding and degradation of the binder-to-crystal interfaces.
Without full characterization of the binder properties, hyperelastic parameters for HTPB as reported by Niu et al. [39] are used as a baseline in these simulations. Additionally, preliminary studies by Prakash et al. [40] and ongoing parameterization efforts suggest that a rate dependent plastic behavior is also applicable to the mechanical behavior of HTPB. Delamination behavior between the crystals and binder is modeled using a bi-linear traction-separation law to govern the previously described layer of cohesive elements. The cohesive model progressively softens the interface stiffness to zero stiffness after reaching a critical value of stress. Although Hu et al. modeled HTPB bonded ammonium perchlorate [33], their parameters for the interface model are utilized as a starting point. The 3D orientation of each HMX crystal is randomly selected from a uniform orientation distribution and assigned single crystal anisotropic elastic constants referenced from Hooks et al. [41]. Doubly periodic boundary conditions for the 2D RVE are specified following the approach developed by van der Sluis et al. [42] and the implementation scheme of Luscher et al. [43].
To illustrate our modeling approach, a simulation utilizing a 198 × 182 pixel 2D section of the CF75L sample geometry in Figure 4 was compressed to approximately 20% strain. Figure 10 shows the progression of crystal-binder delamination at 5%, 10%, and 20%. These preliminary results exhibit qualitatively similar behavior to the high isonate formulation experiments with an HTPB binder shown in Figure 4 (CF75H).
Increasing the compliance of the HTPB binder to mimic the material behavior of the CF75L sample yielded familiar qualitative differences in delamination behavior between the CF75H and CF75L experimental samples. Figure 11 below shows a simple comparison of the simulated state of delamination at 5% macroscale strain for the same mesh displayed in Figure 9 and Figure 10, but with material parameters mimicking samples CF75H (Figure 11a) and CF75L (Figure 11b). Delamination at the crystal-binder interfaces are markedly less numerous for the analogous CF75L simulated sample than the CF75H simulated sample using the same mesh: similar to the comparative experimental results shown in Figure 4 and Figure 5.
Ongoing model development seeks to apply more specific characterization of the binder and interface parameters. In addition to altering the compliance of the HTPB binder, parameters which control plastic hardening of the binder and adhesion between the crystals and binder are also parameters which affect both the interface and macro-scale mechanical behavior. Simulations on increasing spatial scales will be useful for determining an appropriate RVE at which macroscale behaviors are adequately approximated. Insights gained from 2D simulation will help streamline parameterization of full 3D models using real geometric representations of PBX materials. Furthermore, accurate simulation of the characterized microstructure of the materials presented here will enable new simulations of quasistatic and dynamic mechanical deformation of PBX 9501 and other relevant materials. This current study is identifying a range of deformation and fracture responses which depend on several thermomechanical properties such as stiffness and crystal-binder adhesion. It is likely that other PBX materials fall into this spectrum of possible responses, enabling us to conduct simulations and validation experiments without needing to perform full microstructural characterization of every single sample.

4. Conclusions

The ability to characterize the effects of compression and damage in PBXs is integral to understanding explosives systems in general. To our knowledge, this is the first 3D spatially-resolved characterization of a PBX microstructure during deformation. A series of PBXs using HMX and lower-density binder systems which were conducive to X-ray imaging were prepared, including HTPB cured with isonate, and GAP cured with a commercial blend of acrylic monomers/oligomers. Critically, pronounced changes in the stiffness of the HTPB-based binder were found with very small adjustments in the level of isonate (0.53%–1.02%). Correspondingly, a range of deformation and fracture responses that depended on binder properties such as stiffness and crystal-binder adhesion were identified. Using micro-CT imaging during mechanical compression, we observed ductile flow with no fracture, crystal-binder delamination, intergranular cracking (where various delaminations link up to form a crack), and transgranular fracture. Software-based volume rendering of the three-dimensional microstructure was used to create a 2D mesh as a starting point for mesoscale modeling, which exhibited qualitatively similar delamination of the binder and crystals that is observed experimentally. Altering the compliance of the binder in the model to emulate the experiment resulted in void distributions that qualitatively matched the image results. Concurrent work involves tracking individual crystal flow pathways during compression. It is likely that other PBX materials fall into this spectrum of possible responses, enabling us to conduct simulations and validation experiments without needing to perform full microstructural characterization of every single sample. Future work using synchrotron tomography could provide even higher resolution via simultaneous imaging during deformation.

Acknowledgments

The authors thank Darla G. Thompson, Racci DeLuca, and Caitlin Woznick for assistance with the compression experiments. All of the work presented here was supported by the U.S. Department of Energy through the LANL/LDRD Program, including the funding to publish Open Access.

Author Contributions

, John D. Yeager, Virginia W. Manner, and Bryce C. Tappan conceived and designed the experiments; Virginia W. Manner, Brian M. Patterson, Jamie A. Stull, Kevin C. Henderson, Nikolaus L. Cordes, and Andrew M. Schmalzer performed the experiments; John D. Yeager, Brian M. Patterson, Jamie A. Stull, and Virginia W. Manner analyzed the data; Bryce C. Tappan and Andrew M. Schmalzer contributed materials, equipment, and analysis tools; David J. Walters and Darby J. Luscher performed the modeling; Virginia W. Man, John D. Yeager, Jamie A. Stull, Brian M. Patterson., David J. Walters, and Darby J. Luscher wrote the paper.

Conflicts of Interest

The authors declare no conflict of interest. The founding sponsors had no role in the design of the study; in the collection, analyses, or interpretation of data; in the writing of the manuscript, and in the decision to publish the results.

References

  1. Palmer, S.J.P.; Field, J.E.; Huntley, J.M. Deformation, strengths and strains to failure of polymer bonded explosives. Proc. R. Soc. Lond. Ser. A 1993, 440, 399–419. [Google Scholar] [CrossRef]
  2. Yeager, J.D.; Ramos, K.J.; Singh, S.; Rutherford, M.E.; Majewski, J.; Hooks, D.E. Nanoindentation of explosive polymer composites to simulate deformation and failure. Mater. Sci. Technol. 2012, 28, 1147–1155. [Google Scholar] [CrossRef]
  3. Rae, P.J.; Goldrein, H.T.; Palmer, S.J.P.; Field, J.E.; Lewis, A.L. Quasi-static studies of the deformation and failure of β-HMX based polymer bonded explosives. Proc. R. Soc. A Mathemat. Phys. Eng. Sci. 2002, 458, 743–762. [Google Scholar] [CrossRef]
  4. Skidmore, C.B.; Phillips, D.S.; Howe, P.M.; Mang, J.T.; Romero, J.A. The evolution of microstructural changes in pressed HMX explosives. In Proceedings of the 11th International Detonation Symposium, Snowmass Village, CO, USA, 30 August–4 September 1998. [Google Scholar]
  5. Barua, A.; Zhou, M. Computational analysis of temperature rises in microstructures of HMX-Estane PBXs. Comput. Mech. 2013, 52, 151–159. [Google Scholar] [CrossRef]
  6. Willey, T.M.; Lauderbach, L.; Gagliardi, F.; van Buuren, T.; Glascoe, E.A.; Tringe, J.W.; Lee, J.R.I.; Springer, K.H.; Ilavsky, J. Mesoscale evolution of voids and microstructural changes in HMX-based explosives during heating through the β-δ phase transition. J. Appl. Phys. 2015, 118. [Google Scholar] [CrossRef]
  7. Parker, G.R.; Peterson, P.D.; Asay, B.W.; Dickson, P.M.; Perry, W.L.; Henson, B.F.; Smilowitz, L.; Oldenborg, M.R. Examination of morphological changes that affect gas permeation through thermally damaged explosives. Propellants Explos. Pyrotech. 2004, 29, 274–281. [Google Scholar] [CrossRef]
  8. Howe, P.M. Solid Propellant Chemistry, Combustion, and Motor Interior Ballistics(A 00-36332 09-28); American Institute of Aeronautics and Astronautics, Inc.: Reston, VA, USA, 2000; Volume 185, pp. 141–183. [Google Scholar]
  9. Hobbs, M.L.; Kaneshige, M.J.; Erikson, W.W. Modeling the measured effect of a nitroplasticizer (BDNPA/F) on cookoff of a plastic bonded explosive (PBX 9501). Combust. Flame 2016, 173, 132–150. [Google Scholar] [CrossRef]
  10. Berghout, H.L.; Son, S.F.; Skidmore, C.B.; Idar, D.J.; Asay, B.W. Combustion of damaged PBX 9501 explosive. Thermochim. Acta 2002, 384, 261–277. [Google Scholar] [CrossRef]
  11. Mang, J.T.; Hjelm, R.P. Small-angle neutron scattering and contrast variation measurement of the interfacial surface area in PBX 9501 as a function of pressing intensity. Propellants Explos. Pyrotech. 2011, 36, 439–445. [Google Scholar] [CrossRef]
  12. Salazar, M.R.; Kress, J.D.; Lightfoot, J.M.; Russel, B.G.; Rodin, W.A.; Woods, L. Experimental study of the oxidative degradation of PBX 9501 and its components. Propellants Explos. Pyrotech. 2008, 33, 182–202. [Google Scholar] [CrossRef]
  13. Thompson, D.G.; Deluca, R.; Brown, G.W. Time-temperature analysis, tension and compression in PBXs. J. Energ. Mater. 2012, 30, 299–323. [Google Scholar] [CrossRef]
  14. Tan, H.; Liu, C.; Huang, Y.; Geubelle, P.H. The Cohesive law for the particle/matrix interfaces in high explosives. J. Mech. Phys. Solids 2005, 53, 1892–1917. [Google Scholar] [CrossRef]
  15. Liu, C.; Thompson, D.G. Macroscopic Crack Formation and Extension in Pristine and Artificially Aged PBX 9501. In Proceedings of the 14th International Detonation Symposium, Coeur d'Alene, ID, USA, 11−16 April 2010. [Google Scholar]
  16. Hsu, P.C.; de Haven, M.; McClelland, M.; Tarver, C.; Chidester, S.; Maienschein, J. Characterization of Damaged Materials. In Proceedings of the 13th International Detonation Symposium, Norfolk, VA, USA, 23−28 July 2006. [Google Scholar]
  17. Blumenthal, W.; Thompson, D.; Cady, C.; Gray III, G.T.; Idar, D. Compressive properties of PBXN-110 and its HTPB-based binder as a function of temperature and strain rate. Proceedings the of 12th International Detonation Symposium, San Diego, CA, USA, 11–16 August 2002. [Google Scholar]
  18. Skidmore, C.B.; Phillips, D.S.; Son, S.F.; Asay, B.W. Characterization of HMX Particles in PBX 9501. AIP Conf. Proc. 1998, 429, 579–582. [Google Scholar]
  19. Siviour, C.R.; Laity, P.R.; Proud, W.G.; Field, J.E.; Porter, D.; Church, P.D.; Gould, P.; Huntingdon-Thresher, W. High strain rate properties of a polymer-bonded sugar: Their dependence on applied and internal constraints. Proc. R. Soc. Lond. Ser. A 2008, 464, 1229–1255. [Google Scholar] [CrossRef]
  20. Hu, Z.; Luo, H.; Bardenhagen, S.; Siviour, C.; Armstrong, R.; Lu, H. Internal deformation measurement of polymer bonded sugar in compression by digital volume correlation of in- situ tomography. Exp. Mech. 2015, 55, 289–300. [Google Scholar] [CrossRef]
  21. Patterson, B.M.; Henderson, K.; Smith, Z. Measure of Morphological and performance properties in polymeric silicone foams by X-Ray tomography. J. Mater. Sci. 2013, 48, 1986–1996. [Google Scholar] [CrossRef]
  22. Patterson, B.M.; Henderson, K.; Gilbertson, R.D.; Tornga, S.; Cordes, N.L.; Chavez, M.E.; Smith, Z. Morphological and performance measures of polyurethane foams using X-ray CT and mechanical testing. Microsc. Microanal. 2014, 20, 1284–1293. [Google Scholar] [CrossRef] [PubMed]
  23. Yeager, J.D.; Watkins, E.B.L.; Duque, A.H.; Majewski, J. The Thermal and microstructural effect of plasticizing HMX-nitrocellulose composites. J. Energ. Mater. 2017, 1–16. [Google Scholar] [CrossRef]
  24. Cordes, N.L.; Patterson, B.M.; Henderson, K.; Williams, J.J.; Stannard, T.; Singh, S.S.; Ovejero, A.R.; Xiao, X.H.; Robinson, M.; Chawla, N. In Situ X-Ray Synchrotron tomographic imaging during the compression of hyper-elastic polymeric materials. J. Mater. Sci. 2016, 51, 171–187. [Google Scholar]
  25. Croom, B.P.; Xu, P.; Lahoda, E.J.; Deck, C.P.; Li, X.D. Quantifying the three-dimensional damage and stress redistribution mechanisms of braided SiC/SiC composites by in situ volumetric digital image correlation. Scripta Mater. 2017, 130, 238–241. [Google Scholar] [CrossRef]
  26. Croom, B.; Wang, W.-M.; Li, J.; Li, X. Unveiling 3D deformations in polymer composites by coupled micro x-ray computed tomography and volumetric digital image correlation. Exp. Mech. 2016, 56, 999–1016. [Google Scholar] [CrossRef]
  27. Yang, W.; Liu, Q.; Yue, Z.; Li, X.; Xu, B. Rotation of hard particles in a soft matrix. J. Mech. Phys. Solids 2017, 101, 285–310. [Google Scholar] [CrossRef]
  28. Arora, H.; Charalambides, M.N.; Tarleton, E.; Williamson, D.M.; Leppared, C.L. An image based approach to modelling plastic bonded explosives (PBX) on the micro scale. In Proceedings of the 19th International Conference on Composite Materials, Montreal, Canada, July 28 – August 2, 2013. [Google Scholar]
  29. Arora, H.; Tarleton, E.; Li-Mayer, J.; Charalambides, M.; Lewis, D. Modelling the damage and deformation process in a plastic bonded explosive microstructure under tension using the finite element method. Comput. Mater. Sci. 2015, 110, 91–101. [Google Scholar]
  30. Barua, A.; Horie, Y.; Zhou, M. Energy localization in HMX-Estane polymer-bonded explosives during impact loading. J. Appl. Phys. 2012, 111. [Google Scholar] [CrossRef]
  31. Barua, A.; Kim, S.; Horie, Y.; Zhou, M. Ignition criterion for heterogeneous energetic materials based on hotspot size-temperature threshold. J. Appl. Phys. 2013, 113, 064906–064922. [Google Scholar] [CrossRef]
  32. Barua, A.; Zhou, M. A Lagrangian Framework for Analyzing microstructural level response of polymer-bonded explosives. Modell. Simul. Mater. Sci. Eng. 2011, 19. [Google Scholar] [CrossRef]
  33. Hu, R.; Prakash, C.; Tomar, V.; Harr, M.; Gunduz, I.E.; Oskay, C. Experimentally-validated mesoscale modeling of the coupled mechanical–thermal response of AP–HTPB energetic material under dynamic loading. Int. J. Fract. 2016, 203, 1–22. [Google Scholar] [CrossRef]
  34. Gilbert, J.; Chakravarthy, S.; Gonthier, K.A. Computational analysis of hot-spot formation by quasi-steady deformation waves in porous explosive. J. Appl. Phys. 2013, 113. [Google Scholar] [CrossRef]
  35. Chakravarthy, S.; Gonthier, K.A. Analysis of Microstructure-dependent shock dissipation and hot-spot formation in granular metalized explosive. J. Appl. Phys. 2016, 120. [Google Scholar] [CrossRef]
  36. Rao, P.T.; Gonthier, K.A.; Chakravarthy, S. Compaction shock dissipation in low density granular explosive. J. Appl. Phys. 2016, 119, 224904. [Google Scholar] [CrossRef]
  37. Bradski, G.; Kaehler, A. Dr. Dobb’s Journal of Software Tools 2000. Available online: http://mirror.sysu.edu.cn/wiki.ros.org/attachments/Events(2f)ICRA2010Tutorial/ICRA_2010_OpenCV_Tutorial.pdf (accessed on 13 November 2016).
  38. Blacker, T.D.; Bohnhoff, W.J.; Edwards, T.L. CUBIT Mesh Generation Environment; Sandia National Labs: Albuquerque, NM USA, 1994. [Google Scholar]
  39. Niu, R.M.; Zhou, Q.C.; Chen, X.; Ju, Y.T.; Wei, Z.; Zheng, J. Experimental and numerical analysis of mode II fracture between propellant and insulation. Int. J. Adhes. Adhes. 2014, 52, 1–10. [Google Scholar] [CrossRef]
  40. Prakash, C.; Verma, D.; Exner, M.; Gunduz, E.; Tomar, V. Strain rate dependent failure of interfaces examined via nanoimpact experiments. Chall. Mech. Time Depend. Mater. 2017, 2, 93–102. [Google Scholar]
  41. Hooks, D.E.; Ramos, K.J.; Bolme, C.A.; Cawkwell, M.J. Elasticity of crystalline molecular explosives. Propellants Ex. Pyrotech. 2015, 40, 333–350. [Google Scholar] [CrossRef]
  42. Van der Sluis, O.; Schreurs, P.J.G.; Brekelmans, W.A.M.; Meijer, H.E.H. Overall behaviour of heterogeneous elastoviscoplastic materials: effect of microstructural modelling. Mech. Mater. 2000, 32, 449–462. [Google Scholar] [CrossRef]
  43. Luscher, D.; McDowell, D.; Bronkhorst, C. Essential features of fine scale boundary conditions for second gradient multiscale homogenization of statistical volume elements. Int. J. Multiscale Comput. Eng. 2012, 10, 461–486. [Google Scholar] [CrossRef]
Materials 10 00638 g001 550
Figure 1. Chemical components of the HMX/HTPB formulation, where HTPB cures with isonate to form the polyurethane binder system surrounding the HMX crystals and DOA performs as a plasticizer.
Figure 1. Chemical components of the HMX/HTPB formulation, where HTPB cures with isonate to form the polyurethane binder system surrounding the HMX crystals and DOA performs as a plasticizer.
Materials 10 00638 g001
Materials 10 00638 g002 550
Figure 2. Unaxial compression stress-strain curves for the HTPB binder formulations CF75L and CF75H (a) and the CF75-AMO formulations (b). Note the different scales—the HTPB samples in (a) are more compliant. Compression tests were performed at ambient temperature and a strain rate of 0.0045 in/in/s.
Figure 2. Unaxial compression stress-strain curves for the HTPB binder formulations CF75L and CF75H (a) and the CF75-AMO formulations (b). Note the different scales—the HTPB samples in (a) are more compliant. Compression tests were performed at ambient temperature and a strain rate of 0.0045 in/in/s.
Materials 10 00638 g002
Materials 10 00638 g003 550
Figure 3. Ultimate compressive stress as a function of density for the four formulations, compared to PBX 9501 and PBXN-110.
Figure 3. Ultimate compressive stress as a function of density for the four formulations, compared to PBX 9501 and PBXN-110.
Materials 10 00638 g003
Materials 10 00638 g004 550
Figure 4. CT images of CF75L and CF75H samples under uniaxial compression. Note that CF75L does not show cracking, but mostly flow. CF75H shows a separation of the binder from the crystals.
Figure 4. CT images of CF75L and CF75H samples under uniaxial compression. Note that CF75L does not show cracking, but mostly flow. CF75H shows a separation of the binder from the crystals.
Materials 10 00638 g004
Materials 10 00638 g005 550
Figure 5. Selected regions of CF75L and CF75H from Figure 4.
Figure 5. Selected regions of CF75L and CF75H from Figure 4.
Materials 10 00638 g005
Materials 10 00638 g006 550
Figure 6. Comparison of CF75-AMO1 and CF75-AMO2 at increasing compressions. Both samples show extensive cracking by 20% compression, with CF75-AMO2 exhibiting the most damage.
Figure 6. Comparison of CF75-AMO1 and CF75-AMO2 at increasing compressions. Both samples show extensive cracking by 20% compression, with CF75-AMO2 exhibiting the most damage.
Materials 10 00638 g006
Materials 10 00638 g007 550
Figure 7. Selected regions of compressed CF75-AMO1 (a) and CF75-AMO2 (b) at 20% strain.
Figure 7. Selected regions of compressed CF75-AMO1 (a) and CF75-AMO2 (b) at 20% strain.
Materials 10 00638 g007
Materials 10 00638 g008 550
Figure 8. Volume rendering of CF75L (a) and CF75H (b), showing the HMX crystals colored by equivalent diameters. Larger crystals are lighter in color.
Figure 8. Volume rendering of CF75L (a) and CF75H (b), showing the HMX crystals colored by equivalent diameters. Larger crystals are lighter in color.
Materials 10 00638 g008
Materials 10 00638 g009 550
Figure 9. Binary image of CF75L with inset detail of the element mesh used in preliminary simulations.
Figure 9. Binary image of CF75L with inset detail of the element mesh used in preliminary simulations.
Materials 10 00638 g009
Materials 10 00638 g010 550
Figure 10. Maximum principal strain during macroscale compression of the meshed sample in Figure 9, following the general delamination behavior observed with the experimental sample CF75H. Failure of the crystal/binder interfaces occurs in isolated regions at first (5% strain). More surfaces are apparent at 10% strain with continued void growth at 20% strain.
Figure 10. Maximum principal strain during macroscale compression of the meshed sample in Figure 9, following the general delamination behavior observed with the experimental sample CF75H. Failure of the crystal/binder interfaces occurs in isolated regions at first (5% strain). More surfaces are apparent at 10% strain with continued void growth at 20% strain.
Materials 10 00638 g010
Materials 10 00638 g011 550
Figure 11. Void growth patterns at 5% macroscale strain using a polycrystalline mesh identical to those depicted in Figure 9 and Figure 10 for material parameters mimicking (a) sample CF75H and (b) sample CF75L. The red fill indicates the region of void growth associated with crystal-binder delamination.
Figure 11. Void growth patterns at 5% macroscale strain using a polycrystalline mesh identical to those depicted in Figure 9 and Figure 10 for material parameters mimicking (a) sample CF75H and (b) sample CF75L. The red fill indicates the region of void growth associated with crystal-binder delamination.
Materials 10 00638 g011
Table
Table 1. HMX formulations prepared and tested.
Table 1. HMX formulations prepared and tested.
Formulation% HMX 1% HTPB/DOA/Isonate 2% GAP/AMODescription
CF75L88.05.40/5.40/0.530/0Low Isonate, Spongy consistency
CF75H87.65.37/5.37/1.020/0High Isonate, Hard cure
CF75-AMO188.00/0/03.0/9.0Cured with acrylic monomers/oligomers, Hard cure
CF75-AMO288.00/0/06.0/6.0Cured with acrylic monomers/oligomers, Hard cure
1 HMX crystals are a mixture of 75/25 coarse/fine. 2 HMX, HTPB, and DOA were dried in a vacuum oven overnight before use.
Table
Table 2. Volume and mass percent for HMX-HTPB samples taken from the microCT images. 1
Table 2. Volume and mass percent for HMX-HTPB samples taken from the microCT images. 1
Formulation% HMX Volume% Binder Volume% Void Volume% HMX Mass% Binder Mass
CF75L57.941.60.574.425.6
CF75H55.943.60.57327.0
1 Mass calculations assume a crystal and binder density of 1.905 g/cm3 and 0.910 g/cm3, respectively.

Share and Cite

MDPI and ACS Style

Manner, V.W.; Yeager, J.D.; Patterson, B.M.; Walters, D.J.; Stull, J.A.; Cordes, N.L.; Luscher, D.J.; Henderson, K.C.; Schmalzer, A.M.; Tappan, B.C. In Situ Imaging during Compression of Plastic Bonded Explosives for Damage Modeling. Materials 2017, 10, 638. https://doi.org/10.3390/ma10060638

AMA Style

Manner VW, Yeager JD, Patterson BM, Walters DJ, Stull JA, Cordes NL, Luscher DJ, Henderson KC, Schmalzer AM, Tappan BC. In Situ Imaging during Compression of Plastic Bonded Explosives for Damage Modeling. Materials. 2017; 10(6):638. https://doi.org/10.3390/ma10060638

Chicago/Turabian Style

Manner, Virginia W., John D. Yeager, Brian M. Patterson, David J. Walters, Jamie A. Stull, Nikolaus L. Cordes, Darby J. Luscher, Kevin C. Henderson, Andrew M. Schmalzer, and Bryce C. Tappan. 2017. "In Situ Imaging during Compression of Plastic Bonded Explosives for Damage Modeling" Materials 10, no. 6: 638. https://doi.org/10.3390/ma10060638

Note that from the first issue of 2016, this journal uses article numbers instead of page numbers. See further details here.

Article Metrics

Back to TopTop