CROSS-REFERENCE TO RELATED APPLICATIONS

This application is related to Serial No. 07/365,847 filed June 13, 1989, titled "Interpenetrated Polymer Fibers"; which is a division of Serial No. 07/064,746 filed June 22, 1987, now U.S. Patent 4,845,150 issued July 4, 1989 and titled "Interpenetrated Polymer Films"; which is a CIP of Serial No. 06/780,648 filed September 26, 1985.

It is also related to Serial No. 98,710 filed September 21, 1987; Serial No. 203,329 filed June 7, 1988; Serial No. 206,137 filed June 13, 1988; Serial No. 07/206,484 filed June 13, 1988, titled "Multiaxially Oriented Thermotropic Polymer Films and Method of Preparation"; Serial No. 209,271 filed June 20, 1988; Serial No. 07/209,281 filed Ju". 20, 1988, filed "Multiaxially Oriented Thermotropic Polymer Substrate for printed Wire Boards"; and Serial No. 367,433 filed June 16, 1989.

Also of interest are U.S. Patents 4,533,692; 4,533,693; and 4,533,724, all to Wolfe et al.

The disclosures of these applications and all other cited prior art materials are incorporated herein by reference.

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BACKGROUND OF THE INVENTION

1. Brief Description of the Invention The present invention relates to a new class of structural materials, having the near-zero coefficient of thermal expansion (CTE) and high stiffness-to-weight ratio required for space-based SDI systems. These structures have a CTE of less than 1 ppm/°C, preferably less than 0.3 ppm/°C, and have a specific stiffness more than twice that possible with aluminum.

In addition, they have high- and low- temperature capability (-50 to 150°C) , impact resistance, high structural damping, and survivability to a variety of mission-specific threats. Metallic structures are heavy, and conventionally designed structures made from fiber- reinforced composites cannot meet all the demands placed on space-based systems without severe weight penalties, high cost, and slow fabrication. Microcomposite structures made from self-reinforced ordered polymer films, and possibly secondary materials, have excellent intrinsic and tailorable properties to fulfill ultralightweight SDI structural design requirements and the need for rapid fabrication, Poly-p-phenylene benzobisthiazole (PBZT) and poly-p-phenylene benzobisoxazole (PBO) are liquid- crystalline ordered-polymer materials with specific strength and stiffness, CTE, and other mechanical properties equal to or better than many fiber- reinforced composites. Ordered polymers in thin-film form (0.2 to 2 mils) become highly efficient microcomposites when impregnated with secondary material (epoxy, sol-gel, polyimide).

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As described in Section 2, the excellent properties exhibited by thin-film PBZT can be translated into a new class of thin-walled structures which includes stiff, ultralightweight structures (ULWS) for space-based SDI systems. We have demonstrated that a PBZT honeycomb sandwich structure can achieve near-zero CTE ( at least as low as 0.3 ppm/°C) and high specific stiffness, with potential weight savings of 40 to 50 percent over graphite fiber composites, for applications requiring dimensional control of space-based SDI platforms.

The ULW sandwich structure with a specific shear stiffness of the core greater than 34 x 10 in. (863 x 10 ) , about 30 percent better than aluminum, was designed and fabricated with thin (less than 0.002 in., 0.05 mm), biaxially-oriented PBZT film. In addition, near-zero CTE was achieved through a temperature range of -50°C to +150°C. Tables 1-1 and 1-2 as well as Figure 1 compare these properties to current state-of-the-art graphite fiber reinforced cores as well as commercially available cores. This particular PBZT structure has potential applications especially where minimum deflection and dimensional stability during thermal cycling in space is critical. The advantage of using thin, high-moαulus

PBZT films is illustrated in Figure 2 for several core materials. Current quasi-isotropic graphite-reinforced composite materials show high specific stiffness but are limited by their thickness. For the same shear modulus and core thickness, weight savings of nearly 38 percent can be achieved by using PBZT as the core material instead of the thickness-limited

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graphite/epoxy material. Further reduction in wall thickness is possible by reducing the amount of adhesives, for example, and should bring weight savings to 50 percent or more. These structures have both extremely high flexural stiffness, at least 70,000 psi, combined with extremely low core density, no more than 5 pcf, preferably no more than 3 pcf. The high flexural stiffness arises from the inherent stiffness of the films employed, which can be made thin and accordingly are usable with a cell size of 1/8-inch or preferably less, as well as from the stiffness of the facesheets, which can be made from the same material as the core. The weight savings realized by applying the ultralightweight PBZT core to SDI space-based applications allows significant performance improvements in sandwich structures. For example, thicker facesheets and larger facesheets separation distances are possible without any increase in weight over the baseline graphite honeycomb core sandwich to improve tracking accuracy and dimensional stability. Also, thin-films permit smaller cell sizes (less than 0.15 in.) without any increase in core weight. This reduces facesheet wrinkling and allows for thinner facesheets for antenna and mirror applications.

2. Background of Ordered-Polvmer Films This section will give an overview of the ordered-polymer films which are of great interest in connection with this invention. Current graphite/epoxy (Gr/Ep) or thermoplastic (TP) composites have high specific stiffness properties but cannot be processed

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economically as an ultrathin gage (less than 0.010 in., 0.25 mm) structural material. Thin-film PBZT can achieve the high specific stiffness required of SDI space-based designs as ultrathin, biaxially-oriented film. The ability to tailor properties such as stiffness, strength, CTE, and toughness are also important for optimizing such structural designs. Emphasis, then, is placed on applying thin-film PBZT to generic structures that require a maximum stiffness-to- weight ratio.

2.1 Development of Film-Based Ordered Polymers

The assignee of the present invention, Foster-Miller, Inc., has developed film-processing techniques for producing biaxially-oriented ordered polymer films from lyotropic solutions of high- viscosity aromatic heterocyclic polymers. See Serial No. 07/098,710. Figures 3(a) and 3(b) show two such rigid-rod polymers, poly-p-phenylene benzobisthiazole (PBZT) and poly-p-phenylene benzobisoxazole (PBO) . The presence of aromatic groups and ring-shaped stiffening elements (heterocyclic rings containing nitrogen and sulfur) in the backbone of the polymer molecule give rise to its excellent mechanical properties as well as high thermo-oxidative resistance. In addition to film processing, Foster-Miller has developed novel solution processing and treatment to control orientation, microfibrillar structure and texture, and physical properties. See Serial Nos. 07/098,710 and 07/064,746. Generally, the structural materials of the present invention contain polybenzazole (PBZ) polymers selected from the group consisting of polybenzoxazole

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(PBO) , polybenzothiazole (PBT) and polybenzimidazole (PBI) polymers, and random, sequential or block copolymers thereof. Polybenzazole polymers and their synthesis are described at length in numerous references, such as Wolfe et al., Liquid Crystalline

Polymer Compositions, Process and Products, U.S. Patent 4,533,693 issued August 6, 1985, and W.W. Adams et al., The Materials Science and Engineering of Rigid-Rod Polymers (Materials Research Society 1989), which are incorporated herein by reference.

Polybenzazole polymers preferably contain a plurality of mer units that are AB-PBZ mer units, as represented in Formula 1(a), and/or AA/BB-PBZ mer units, as represented in Formula Kb)

1(») AB-PBZ

Kb) AA/BB-PBZ wherein:

Each AR represents an aromatic group. The aromatic group may be heterocyclic, such as a pyridinylene group, but it is preferably carbocyclic. The aromatic group may be a fused or unfused polycyclic system. The aromatic group preferably contains no more than about three six-membered rings, more preferably contains no more than about two six-membered rings and

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most preferably consists essentially of a single six- membered ring. Examples of suitable aromatic groups include phenylene moieties, biphenylene moieties and bisphenylene ether moieties. Each Ar is most prefeably a 1,2,4,5-phenylene moiety.

Each Z is independently an oxygen atom, a sulfur atom or a nitrogen atom bonded to an alkyl group or a hydrogen atom. Each Z is preferably oxygen or sulfur (the polymer is preferably PBO, PBT or a copolymer thereof);

Each DM is independently a bond or a divalent organic moeity that does not interfere with the synthesis, fabrication or use of the polymer. ^! he divalent organic moiety may contain an aliphatic group (preferably C, to C,,), ^ou t the divalent organic moiety is preferably an aromatic group (Ar) as previously described. Each DM is preferably a 1,4-phenylene moiety or a 4,4'-biphenylene moiety, and is most preferably a 1,4-phenylene moiety. The nitrogen atom and the Z moiety in each azole ring are bonded to adjacent carbon atoms in the aromatic group, such that a five-membered azole ring fused with the aromatic group is formed.

The azole rings in AA/BB-PBZ mer units may be in cis- or trans-position with respect to each other, as illustrated in Polybenzothiazoles and Polybenzoxazoles, 11 Ency. Poly. Sci. and Eng. 601, 602 (J. Wiley & Sons 1988), which is incorporated herein by reference. The polybenzazole polymer may be rigid rod, semirigid rod or flexible coil. It is preferably rigid rod in the case of an AA/BB-PBZ polymer or semirigid in

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the case of an AB-PBZ polymer. It more preferably consists essentially of AA/BB-PBZ mer units. Exemplary highly preferred mer units are illustrated in Formulae 2 (a)-(e).

c

The polybenzazole polymer most preferably consists essentially either of the mer units illustrated in Formula 2(a) (cis-PBO) or of the mer units illustrated in Formula 2(c) (trans-PBT).

Each polymer preferably contains on average at least about 25 mer units, more preferably at least about 50 mer units and most preferably at least about 100 mer units. The intrinsic viscosity of cis-PBO or trans-PBT in methanesulfonic acid at 25°C is preferably

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at least about 10 dL/g, more preferably at least about 20 dL/g and most preferably at least about 30 dL/g.

The examples herein relate mainly to PBZT structures, but PBO is also usable as it is often interchangeable with PBZT. PBO is commercially available from the Dow Chemical Company. U.S. Patents 4,772,678; 4,703,103; 4,533,724; 4,533,692; 4,225,700; 4,131,748; and 4,108,835 are of interest in connection with the manufacture of PBO and PBZT. Also usable are thermotropic polymers, including wholly aromatic polyesters such as Vectra (trademark), which is available from Hoechst-Celanese, and is a naphthalene-based aromatic copolyester; or Xydar (trademark), which is available from Amoco Performance Polymers, and is a bisphenol-based aromatic copolyester.

Biaxially-oriented PBZT films exhibit properties of high strength and stiffness (as high as 250 Ksi (1.72 GPa) tensile strength, and 25 Msi (172 GPa) tensile modulus). They have controllable CTE (from -10 to +20 ppm/ ^β C) , and outstanding thermal- oxidative resistance of over 400°C. PBO is believed to have even higher specific modulus than PBZT, based on preliminary data from Dow Chemical on their PBO fibers. The control over properties and characteristics of PBZT films as thin as 0.0015 in. (0.04 mm) is accomplished through engineering at a microcomposite level of about 10 to 100 times smaller than fibers or fabrics; resulting in high-performance, ultrathin structures. Orientation can vary from highly uniaxial (±10 deg.) to quasi-isotropic (+45 deg.), depending on the performance requirements of the SDI space-based

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structures. Table 2-1, listing the properties of PBO and PBZT film along with graphite/epoxy unidirectional composite, reflects the outstanding specific stiffness (modulus divided by density) of these ultrathin, ordered-polymer films.

The rod-like morphology of PBZT films is the key to both their excellent properties and their ability to be engineered into ultrathin composites and laminates. The rigid-rod molecules in the form of biaxially-extruded film consist of an interconnected microfibrillar network, similar to unidirectional plies stacked together as a single film, as shown schematically in Figures 4(a) and 4(b). The dimensions of this polymer network are on the order of 50 to 100A in size, and during processing it can be infiltrated by a secondary material such as a dissolved or uncured polymer, or can be completely consolidated into 100% PBZT or PBO. The secondary or matrix material, if used, encapsulates the PBZT microfibriIs and acts in concert with the network to form a microcomposite having volume percentages of 5% to 70% secondary material, for example. See also Serial No. 07/064,746, regarding these microcomposites. These microcomposites are known as "prepregs" in that the polymer network is pre-impregnated with the matrix material.

The properties of the PBZT microcomposite are tailorable, depending on the matrix material used. See Serial No. 07/064,746. Efforts conducted at Foster-Miller have shown that a variety of matrix materials can form different types of microcomposites, including polyimide, epoxy and silica glass processed by the sol-gel method. The impregnation process can

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also be used to bond adjacent PBZT/matrix plies together to build up a laminate with quasi-isotropic properties. A thin coating of high-temperature resins, such as polyimide on the surface of the PBZT film, can serve as adherent for bonding PBZT film. This is useful for node bonds in honeycomb cores or joints on stiffened panels.

2.2 Application of Ordered Polymer

Films to Ultraliσhtweiqht Structures One of the major advantages of using film- based PBZT for structural application is the film's ability to achieve high specific stiffness at a thickness of less than 0.002 in. (0.05 mm). Thin- walled structures such as tubes, ribbed panels and honeycomb sandwich structures fail at the elastic buckling stress of the structure (also called shell buckling). This buckling stress is directly related to the modulus and in general is much lower than the material's compressive stress. Thus, high-modulus, low-density thin materials such as PBZT films are required for space-based satellite structures.

When using an isotropically balanced eight- ply composite laminate for SDI structures, ultrathin plies are needed for high-stiffness, moderate-strength, minimum-gage applications, with a minimum gage being 0.040 in. (1.0 mm). However, future requirements for space structures will call for a gage of less than 0.010 in. (0.25 mm) for similarly balanced six- or eight-ply laminates (JL). Production costs are extremely high for these fiber-reinforced sheets because it is difficult to spread and handle high modulus tows or yarns. PBZT films have the ability to

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g exceed specific stiffness of 3.2 x 10 in. as an ultrathin, quasi-isotropic material that is eight times thinner (less than 0.005 in., 0.127 mm) than current graphite-fiber prepregs. This will permit thin, dimensionally stable, high-stiffness structures to be fabricated.

High strength and high modulus carbon- fiber-reinforced composites (epoxy and thermoplastics) will play important roles in SDI space-based systems, but innovative new designs will also be needed. Some of these new structures are shown in Figures 5(a)-5(g).

Emphasis of SDI requirements for space- based systems has shifted from space-based interceptors (SBI) to space surveillance and tracking systems (SSTS). These large, boxlike structures and platforms must be of low mass and high dimensional stability. New innovative structural designs can be realized only by using high modulus, thin-film PBZT as the primary structural material. Metals are too heavy and fiber composites are too thick.

In Section 3, we describe the design and fabrication of a thin-walled, ultralightweight honeycomb core using PBZT as the core material. The core provides high shear stiffness (98 Ksi at 5 pcf core density) and low CTE (0.3 ppm/ ^β C) to meet the requirements of space surveillance and tracking systems. Furthermore, ULW PBZT honeycomb sandwich structures have the potential for producibility at an affordable rate, since films can be produced more rapidly than thin fiber-reinforced/epoxy prepregs.

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BRIEF DESCRIPTION OF THE DRAWINGS

Fig. 1 is a bar graph reflecting outstanding shear modulus of PMR-15/PBZT honeycomb core as compared to current cores of 5.0 pcf density. Fig. 2 is a bar graph showing minimum weight required for effective transverse shear modulus of 70 Ksi for several honeycomb cores. Note that PBZT and Gr/Ep core materials have +45 deg. biaxial orientation. Figs. 3(a) and 3(b) respectively show the chemical structure of two lyotropic liquid crystal polymers, PBZT and PBO.

Figs. 4(a) and 4(b) are a schematic diagram showing orientation of single layer PBZT films. Figs. 5(a)-5(g) show several innovative designs for thin-walled, ultralightweight structures.

Fig. 6 shows the biaxial in-plane orientation of PBZT film.

Fig. 7 shows the elastic properties of a composite material as referred to Cartesian coordinates (5).

Fig. 8 shows modulus as a function of orientation angle, θ, for PBZT film, experimental. Fig. 9 is a plot of E and G for biaxially-oriented PBZT film.

Fig. 10 shows a honeycomb core sandwich. Fig. 11 shows the respective contribution of bending and shear to total deflection.

Fig. 12 shows the nomenclature for hexagonal core.

Fig. 13 shows the areal weight for PBZT core as function of cell wall t and cell size, d.

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Fig. 14 shows the effective transverse shear stiffness as a function of core wall thickness to cell size ratio, tc/d.

Fig. 15 shows core shear modulus as a function of core density for PBZT and T-300/Ep core, theory. Data points for core shear modulus of three densities of graphite/phenolic (Gr/Ph) are for comparison.

Fig. 16 shows a honeycomb core undergoing flatwise compression.

Figs. 17(a) and 17(b) show a nomenclature for in-plane buckling of honeycomb core.

Fig. 18 shows the overall buckling of plate, σ as a function of core wall thickness to cell size ratio.

Fig. 19 shows the introduction of PMR-15 monomer to encapsulate microfibril network.

Fig. 20 is a perspective view of the 4 in. W x 6 in. L Teflon-coated corrugated compression mold made of 420 SS.

Fig. 21 shows the placement of Teflon rods on PBZT/TS sheets in mold. Rods force PBZT/TS into hexagonal contours of mold.

Figs. 22(a) and 22(b) are thermoform schedules for (a) PBZT/Tactix 695 and (b) PBZT/PMR-15, respectively.

Fig. 23 is a perspective view of a primary bonded single layer hexagonal sheet.

Fig. 24 is a perspective view showing a single layer honeycomb cut into sections prior to stacking into full core.

Fig. 25 is a load-deflection curve for neat PBZT.

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Fig. 26 is a load-deflection curve for PBZT/PMR-15.

Fig. 27 is a load-deflection curve for neat PBZT. Fig. 28 is a load-deflection curve for

PBZT/Tactix.

Fig. 29 shows two failure regions for ±45 deg. biaxially-oriented films.

Fig. 30 is a schematic diagram showing a setup for four-point flexural test.

Figs. 31(a) and 31(b) show load-deflection curves for four-point flex of two PBZT/PMR-15 sandwiches.

Fig. 32 shows a setup for flatwise compression test.

Figs. 33(a) and 33(b) are load-deflection curves for flatwise compression test of PMR-15/PBZT core.

Figs. 34(a) and 34(b) illustrate how inconsistent bond lines lead to local buckling at the thin-film core walls.

Fig. 35 is a schematic diagram showing an alternative method of processing film from extruded film to final core.

DETAILED DESCRIPTION OF A PREFERRED EMBODIMENT

3. Thin-Walled ULW Honeycomb Core Foster-Miller has developed novel film processing techniques for lyotropic ordered polymers. Properties of biaxially extruded PBZT films show promise as thin, high-modulus structural material. To realize this potential, an ultralightweight thin-walled honeycomb sandwich was designed, fabricated, and tested. Section 3, et seσ. gives an overview for

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predicting elastic properties of biaxially-oriented PBZT film. Using the results of this theory, a design analysis for the honeycomb core was conducted. Section 3.2 et seσ. describes the technology developed for fabricating the stiff honeycomb sandwich cores as well as for testing the core's stiffness properties.

3.1 Design Analysis of PBZT Honeycomb Core

The design of the thin-walled structure takes advantage of PBZT's tailorable properties. Biaxially-oriented films are engineered at the molecular level to optimize a given structural design. Requirements such as high specific stiffness greater

Q than 10 in., low mass, and near-zero CTE are met by integrating specific properties of thin-film PBZT into the design of stiffened and dimpled panels, honeycomb sandwiches, tension-web beams, thin-walled tubes, and struts.

3.1.1 Micromechanics of

Biaxiallv-Oriented Thin Film PBZT One of the objectives of our invention is to apply a micromechanical model to biaxially-oriented thin film PBZT so that in-plane stiffness properties can be determined. The model is based on classical laminated plate theory ( 2 ) as applied to orthotropic laminates and shows good agreement with the experimental data. In subsection 3.1.2, we will see how the elastic constants obtained through this analysis are used to design a honeycomb sandwich structure, Figure 6 shows how PBZT film as extruded by

Foster-Miller's counter-rotating tube die exhibits a

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biaxial in-plane orientation. See Serial No. 07/098,710. This allows us to tailor the stiffness and CTE properties by molecular orientation of the rigid- rod like polymers in these films. A generalized model based on previous studies (3.) at Foster-Miller was developed with a two-ply laminate model to predict stiffness properties as a function of the orientation angle, θ.

Single-layer biaxially-oriented PBZT film is modeled as two hypothetical unidirectional plies (uniplies) oriented in the ± θ directions. The uniplies are highly oriented due to the rod-like nature of PBZT molecules, and can be modelled using the nomenclature of Figure 7. The following assumptions are made: (J3)

- Each uniply undergoes the same in-plane strains. That is, each uniply is coupled or bonded to the layers above and below so that there is no relative slip. The interlaminar shear forces required to produce the same strain in each uniply are transferred from layer to layer. It has been reported (3.) that the experimental data for in-plane modulus indicate that this assumption is at least a good approximation.

- Each uniply can be characterized as homogeneous and two-dimensionally orthotropic with respect to the four elastic constants used to characterize each lamina (E ^,, _f --- Ϊ ' ^G i2' ^{and v} 12^* Thus, the biaxially-oriented film is modelled as consisting of two uniplies oriented at +θ and -θ to the machine direction (MD), or longitudinal axis of the film, as shown in Figure 6.

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- The film is assumed to be balanced, that is, 50 percent of the material is oriented at +θ and 50 percent at -θ.

- The films are sufficiently thin so that any antisymmetry about the midplane is negligible. The out-of-plane moments and curvatures created by such antisymmetry are taken as sufficiently small so that they do not affect the calculation of in-plane strains. The intent of this analysis is to determine the four independent elastic constants and the orientation angle, θ, required to characterize the biaxially-oriented PBZT film. The parameters to be determined are:

^E ll ~ ^lon 9 ^tu C-i ^na l Young's modulus E ₂₂ ■ transverse Young's modulus

Egg * G ₁₂ * transverse shear modulus v ₁₂ ■ major Poisson's ratio θ ■ orientation angle of the film Table 3-1 presents the calculated parameters for biaxially-oriented film based on two cases of elastic constants for the uniply model. Figure 9 shows the results in graphical form for E and Ξ . Case i is the predicted values using high tensile modulus for the PBZT uniply, E,, = 30 Msi. The curve of case ii is for E.. « 17 Msi. Both sets of data were computed by an iterative method which will be outlined in Sections 3.1.1 (A.l) and 3.1.1 (A.2). Since the shear modulus, Gxy, is difficult to determine experimentally, laminated plate theory was applied using known (or estimated) constants, Ex and Ey, as ^v xy'

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In reference to Figure 8, one trend is to be noted. The decrease in modulus from θ ■ 10 deg. to θ = 45 deg. is due to the reduction in the microfibrils' contribution to stiffness with increasing off-axis angle, θ. Later, we will see how shear modulus G, ₂ increases as θ goes from θ » 0 deg. to a maximum of θ = 45 deg. This becomes an important criterion in designing a honeycomb core with high shear stiffness. Figure 8 shows the comparison of the calculated modulus values with measurements. The data labelled 1088 are for the neat PBZT film used in this invention. Data labelled xx88 are film runs conducted prior to the 1088 run. Axial tensile moduli, E _χ , of biaxially-oriented PBZT thin films have been measured at Foster-Miller.

Data computed from laminated plate theory is found to fit the experimental data closely from θ = 10 deg. to θ ^« 45 deg.. Stiffness properties of the PBZT film as predicted by our model can be used for optimal design of ultralightweight structures for SDI systems. High stiffness, near-zero CTE, and low weight can be achieved by proper selection of biaxially- oriented PBZT film. A PBZT honeycomb core was designed, fabricated and evaluated against aluminum and graphite honeycomb cores for application to ultralightweight sandwich structures.

3.1.1(A.1) Determination of In-Plane Shear

Modulus by an Iterative Procedure The in-plane shear modulus, G ₁₂ , was calculated by an iterative method. The test method

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developed by Rose (12.) (adopted as ASTM standard D3518-

76/1982) allows us to compute Gxy using tensile-strain data for ±45 deg. biaxially-oriented PBZT film. The film is modeled as a ±45 deg. laminate so that GENLAM, - a software using laminated plate theory, can compute off-axis properties for a given input of four elastic constants.

Equation A-l presents shear modulus, Gxy, as a function of two other elastic constants, E (longitudinal tensile modulus), and Poisson's ratio, vxy. Although this relationship holds true only for isotropic materials (properties the same in all directions), the in-plane stress-strain response of a

±45 deg. uniply PBZT laminate, as a quasi-isotropic material (E - E and v ■ v ), can be considered to be isotropic. This allows G in Equation A-l to be computed from experimentally determined values of E for ±45 deg. biaxially-oriented PBZT film. G can be determined by comparing the estimated values of v ^c to those of v ^s predicted by laminated plate theory until ^χ y they converge. The general procedure for iteration consists of first creating a (±45 deg.) s laminate in

GENLAM and using known values of E , E . An initial value of G is calculated from Equation A-l using ^v _V ^S " °« ⁵ * ^τhe steps include:

1. Create (±45 deg.) s laminate using GENLAM and note calculated value of v ^c at θ ^β 45.

2. If vxyc is not equal to vxys (as calculated for θ=45 deg.), then find mean value of vxyc and _χv s an

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will be the same as the experimentally determ ned value of Ex. This proves the validity of this iterative method. 3.1.1 (A.2) Two Case Studies of Elastic

Constants of PBZT Film

A parametric study involving effects of varying E,,, E ₂₂ , G, ₂ and v. ₂ for E as a function of orientation, θ, was conducted using laminated plate theory. Since the data plotted as Figure 3-4 exhibit variation in modulus values for a given orientation, curves for two case studies were generated using the GENLAM software. These curves established a "range" for the data points. In both cases, E was taken as 3.0 Msi and Poisson's ratio of 0.3 was used. For each case, a new value of G ₁₂ was determined using the iterative procedure outlined previously in Section

3.1.1 (A.l).

The data generated from GENLAM software is tabulated in subsection 3.1 as Table 3-1. Initial conditions for case i and ii are found as E.., & ₂₂ , G, ₂ and ₁₂ at θ » 0 deg..

3.1.2 PBZT Honeycomb Core as an ULW Structure

We have demonstrated that the ultrathin, biaxially-oriented PBZT film produces honeycomb cores superior to the current state-of-the-art graphite

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honeycomb core. For instance, the PBZT honeycomb core with the same shear stiffness as a graphite core is 34 percent lighter; or in the same case of honeycomb cores with the same areal densities, the PBZT core possesses 33 percent higher shear stiffness, as shown previously in Figure 1. With improved quality film and better fabrication techniques, weight savings of 40 to 50 percent over current graphite/epoxy cores are obtained. This weight savings, as previously shown in Figure 1-3, allow significant performance improvements for SDI space-based applications. For example, thicker facesheets and/or larger facesheet separation distance is possible, without any increase in weight over the baseline graphite honeycomb core sandwich, to enhance the structural and system performance, e.g., tracking accuracy, dimensional stability, low moment of inertia, low mass, etc. Also, cell size can be reduced without any increase in weight, using thinner walls. This reduces facesheet thickness for precision surfaces such as optical platforms, mirrors and microwave antennae.

The design of an ultralightweight honeycomb core is especially adapted to space-based applications. In addition to general requirements of high stiffness- to-weight ratio and dimensional stability, the ULW honeycomb sandwich must have:

- A core of high shear stiffness at minimum possible weight. This minimizes deflections and allows for high natural frequency of vibration.

- Thin-walled core is necessary to allow for small cell size (less than 0.125 in.). Facesheet dimpling and wrinkling are reduced, permitting use of thinner facesheet materials. This allows the honeycomb

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core to provide a stable and stiff support for precision optical tracking and surveillance systems.

- High damping and stiffness is necessary to attenuate vibration caused by platform maneuvering or ejection of interceptors. This is difficult to obtain as very few structural materials have adequate passive inherent damping characteristics (1.).

- Compressive (flatwise) strength and compressive modulus are secondary considerations. The core needs to withstand the application of the facesheet during fabrication. The platform will experience severe loads only during launch acceleration (10 to 15 g's). (1).

- Potential for rapid fabrication and relatively low materials cost. The large number of structures to be deployed as part of the SDI space architecture creates a need for producibility and affordability never before experienced in space hardware production (1,). To achieve high shear modulus, ±45 deg. orientation of the PBZT core is preferred, based on the results summarized in Figure 8. In the following design analysis, the ±45 deg. biaxially-oriented PBZT film is compared to a ±45 deg.-bias weave T-300 graphite/epoxy for applications to honeycomb core. The elastic properties developed in subsection 3.1.1 for PBZT provide important material properties for predicting the performance of an ultralightweight PBZT honeycomb core. The flatwise compres ive and shear properties of several structural honeycomb cores are presented in Table 3-2. Until recently, non-metallic

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cores such as Nomex and fiberglass have been limited to applications that do not require high specific stiffness due to their low shear moduli when compared to aluminum cores. The graphite/polymer (polyimide, phenolic, epoxy) honeycomb core developed by Hexcel meets or exceeds the specific shear stiffness of comparable aluminum cores.

Considerations in Design of Honeycomb Sandwich Structures In our design analysis we consider a honeycomb core consisting of two thin facesheets as shown in Figure 10. In flexure of the sandwich structure, the facings carry tensile and compressive axial loads while the core is designed to resist the shear load. Thus, the flexural stiffness is defined by two components, as in Equation 3-1 below, where D is the effect of the facesheets and N is the effect of the core. Figure 11 illustrates how the deflection, y, is a combination of facesheet bending and core shearing.

K Pa ³ κ _β Pa y - + __ ^* (3-D

N where

E _f b(h ³ -c ³ )

D s _— Flexural Stiffness,

12 (l-v ) facesheets and

1 N = « 2, (h + c)bGC._ Shear Stiffness, honeycomb core and the variables are defined as:

E _f = modulus of elasticity of facesheet

G„c = core shear modulus

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v ■ Poisson's ratio

P = total load a = span b = width of core c = core depth

K, and K * constants depending on the beam loading h = total sandwich thickness Optimum design of the core will minimize the deflection, y, with respect to the weight; that is, we need to maximize sandwich stiffness, D, and shear stiffness, N, and minimize the facesheet weight and core density.

For our design comparison, we considered the same facesheet material to evaluate the PBZT and the graphite/epoxy cores. Furthermore, we considered cores of the same thickness, since separation of facesheets is a function of geometry. The flexural stiffness-to-weight ratio of sandwich structures, then, can be improved through the following approaches:

- Using facesheets of higher specific stiffness, as thin as possible

- Increasing the facesheet separation distance by using a deeper core for higher section modulus

- Using a core material with high shear modulus.

Since the object of the invention is to produce ultralightweight structures, primary consideration is given to achieving low core densities using thin-film PBZT core with stiffness properties similar to those of a T-300 graphite/epoxy system.

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Substitution of the lightweight PBZT core for a graphite core in a sandwich structure allows performance improvements through the second and third approaches, without increasing the structural weight. Also, since PBZT film is ultrathin, the cell size can be reduced without increasing core density. This has the added benefit of eliminating dimpling or wrinkling of facesheets. Stiff and precise support of optical tracking and surveillance systems as well as antenna arrays is possible. The analysis that follows evaluates the PBZT core against the graphite core for application to ULW sandwich structures.

Design of PBZT Honeycomb Core

The theoretical honeycomb core density, P',-.' is defined as (7):

3t.

P\ (3-2)

where tc * core wall thickness d = core cell size p « core material density as described in Figure 12.

The properties as reported by Hexcel for T- 300/Ep(Table 3-2) (8.) are nominal values based on: p' _c - 5 pcf d - 0.25 in. p _c - 0.056 lb/in. ³

For the T-300/Ep system, the minimum core wall thickness that can be achieved is t„ c = 0.005 in.

(0.127 mm) . Biaxially-oriented PBZT film can be produced much thinner, thus giving the capability to

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develop ultralightweight honeycomb cores with smaller cell size, and lower density, in addition to benefits mentioned above.

To demonstrate the weight advantage of the thin-walled PBZT core, a performance curve constructed as Figure 13 shows how cell wall thickness, tc, and cell isize, d, affects the areal weight. The weight per unit area of a honeycomb structure can be optimized by: (9,10)

(W-W _ad ) = 2p _f t _{f + c} p _c (3-3)

3d where p^ and t _f are the facesheet density and thickness, respectively; h is the total sandwich depth and w - is the weight of the adhesive used in the bonding of the core and facesheet.

Consider h , p- and t to be the same for both the T-300/Ep and PBZT sandwich structures. Reference to Figure 13 shows a 30 percent weight savings by substituting a PBZT core of t ■ 0.0015 in. (0.04 mm) for a T-300/Ep core of 0.005 in. (0.127 mm) thick core wall. Next, we will demonstrate that the ultrathin PBZT film can produce a honeycomb core with the requisite shear stiffness-to-weight ratio. The PBZT honeycomb core design was developed by imposing the following performance requirements that are equal or superior to the graphite/epoxy core material:

- Effective transverse shear modulus

- Local buckling due to flatwise compression of core wall

- Overall in-plane elastic instability.

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The theoretical stiffness properties of the ±45 deg. biaxially-oriented PBZT film are presented in Table 3-3. The ±45 deg. web orientation design of the core benefits from the maximum shear modulus property available from the film. The PBZT core was compared to a baseline core made of T-300 graphite/epoxy, corresponding to Hexcel's HFT-G honeycomb core. The goal is to optimize the stiffness-to-weight ratio by using the thin-walled PBZT core in place of the graphite/epoxy core.

Shear Stiffness Analysis

Vinson and Shore (ljO) in their method of analysis for honeycomb core sandwich structures, define effective transverse shear stiffness as: 4t _c

G' = _i G_ (3-4) ^c 3d ^c where Gc„ = shear modulus of the core itself. The effective transverse shear modulus, G'c, is taken to be in the ribbon direction, L, where the nodes along this direction are. bonded, as previously indicated in Figure

12. This would give a relative increase in effective shear modulus over the W direction.

A performance curve shown in Figure 14 gives effective transverse shear modulus, G*c as a function of core thickness to cell size ratio (tc/d) using the following core material properties:

- ±45 deg. T-300 Gr/Ep (G _c = 4.85 Msi)

- ±45 deg. T-300 Gr/Ep from Hexcel (G ■ 2.96 Msi, estimated)

- ±45 deg. biaxially-oriented PBZT (G = 4.62, see Table 3-3).

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The estimated value of Gc„ - 2.96 Msi is based upon Hexcel's data for G' ■ 71 Ksi and normalized values of p' ■ 5 pcf and d » 0.25 in. The curve for a typical ±45 deg. T-300 Gr/epoxy material (G (_» = 4.85 Msi) represents an upper limit based on a tow of < 1000 filaments and tc < 5 mils, which would be difficult to fabricate into a core.

PBZT as a ±45 deg. biaxially-oriented thin- film can theoretically achieve an effective transverse shear modulus of _71 Ksi with a core thickness-to-cell size ratio <.l/85. In keeping with the first criterion of achieving tc < 4 mils, one will find a tc__ mi..n. of

1.47 mils for 1/8 in. cell size (for t _Q/d = 0.01176). In conclusion, a minimum effective transverse shear modulus of 71 Ksi is required of the

PBZT honeycomb core. This criterion is met with a PBZT honeycomb core with the following properties:

- t - 1.47 mils

Calculation for areal weight (Equation 3-3) for PBZT film with these properties can yield almost 30 percent weight savings over Hexcel's HFT-G core (5 pcf, d = 0.25). This was shown graphically in Figure 13 for ^w ~ ^w ad ^{as a} ^ ^unct i° ⁿ °f *■ ^an< d. In Figure 15, the theoretical core density for ±45 deg. PBZT is found to be 3.3 pcf for shear stiffness of 71 Ksi, giving a core density which is 34 percent less than that of the HFT-G core with similar stiffness properties.

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Flatwise Compressive Modulus Analysis

The compressive modulus of a honeycomb core sandwich undergoing flatwise compression, as shown in Figure 16, is primarily a function of core density, p . Bruhn (J) expresses an empirical formula for a design curve as: p'

Ec' = 2.13 — ^C 1.415 E„c (3-5) c where E is the compressive modulus of the core material and E ' is the flatwise compressive modulus of the honeycomb core.

High compressive strength or modulus as compared to aluminum cores is not demanded, since the orientation of the PBZT film is maximized to obtain high shear stiffness of the core. A nearly uniaxial film would be used as the core material if the design requirements called for a core of high compressive modulus. For SDI structures, compressive loading is a secondary consideration when designing honeycomb sandwich structures.

Analysis for Overall In-Plane Buckling

The overall buckling of honeycomb core sandwich structure is an important design criterion as it combines the effects of both compression and shear stresses on the sandwich. The critical stress for buckling of composite plate is given by Vinson and Shore (iP_) as:

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the x and y directions, respectively. Figures 17 a and 17(b) show the geometry of the core height, h __., and width, b, which is transverse to applied axial load, N . The critical buckling strength, ° ^* _cr # given here takes into consideration the effects of orthotropic laminate properties. K , a constant determined by a parametric equation, is essentially a weighting factor for flexural stiffness and shear modulus properties (10). Application of Equation 3-6 to ±45 deg. biaxially-oriented PBZT and T-300 Gr/Ep system as a function of t /d is graphically shown in Figure 18. Two cases are considered.

1. T-300 Gr/epoxy core with T-300 Gr/epoxy faces (±45 deg. bias weave for both)

2. ±45 deg. PBZT core with T-300 Gr/epoxy faces (±45 deg. bias weave).

Although the curves for cases 1 and 2 are similar, PBZT, as an ultrathin material, is shown to achieve the same critical buckling stress as the

Gr/epoxy core. For example, a PBZT core with t of only 0.0025 in. and d * 0.125 in. would achieve the same critical buckling strength as that of the nominal Gr/Ep core. The buckling mode given by Equation 3-6 is for a load applied in the axial direction (x-direction) of the sandwich structure. This mode of buckling will be the lowest failure mode if the following condition is met:

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where V is tion (10).

If the condition in Equation 3-7 is not met, then there is the possibility of failure due to core shear instability. This will occur at a load lower than that necessary to induce overall buckling of the honeycomb sandwich structure. For both PBZT and Gr/Ep system, this lower limit is reached at t /d of 1/125 and σ _c∑ . of 200 Ksi. This lower limit can only be achieved by Gr/Ep core if the core wall thickness can be made 0.002 in. (0.051 mm) thick, which is not possible by current processing methods. The portion of the curve for the Gr/Ep system shown as dashed lines represents limits placed on achieving a minimum ratio of wall thickness to cell size for the core and yet maintaining a critical buckling strength of at least 200 Ksi. PBZT, as an ultra-thin film, can be fabricated into an ultralightweight honeycomb core with cell walls as thin as 0.001 in (0.025 mm) for 0.125 in. (3.18 mm) cell size for the same buckling strength. Thus, the PBZT core design is dictated by the ability to achieve the thinnest wall possible rather than mechanical properties of the core material.

3.2 Fabricating PBZT Honeycomb Core

In this section, a method for fabricating PBZT honeycomb core is described. The process comprises three basic steps: extrusion of biaxially- oriented film, introduction of secondary material, lay- up and curing of the core to final dimension. Emphasis

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is placed on demonstrating the potential for low-cost, high-production-rate manufacturing.

3.2.1 Film Processing

Approximately 100 ft. of biaxially blown PBZT film tubing was extruded from 30 intrinsic viscosity (IV) dope. See Serial No. 07/098,710. The dope was previously degassed in a vented twin-screw extruder for at least one minute to ensure homogeneity and eliminate air bubbles. The PBZT film was extruded in two different orientations, ±10 deg. and ±45 deg. from machine direction (MD). Final thickness upon coagulation and drying, see Serial No. 07/098,710, was 1.5 ± 0.7 mils. The tubes were infiltrated with resin as described next to form a "prepreg."

3.2.2 Secondary Material

Two resins were selected to form an interpenetrating network in PBZT film. Both resins, Tactix 695 epoxy resin, available from Dow Chemical Co., and PMR-15 thermosetting polyimide, available from Hysol, which is a norbornenyl-lapped addition-type polyimide resin, which is based on the polyermization reaction of three monomers: (a) mono-methylester of 5-norbornene-2,3-dicarboxylic acid (NB); (b) 4,4'- methylenedianianiline (MDA) ; and (c) di ethylester of 3,3' ,4,4'-benzo-phenontetracarboxylic acid (BTDE), in neat form, show good mechanical properties and have excellent thermo-oxidative resistance. Furthermore, these resins are supplied in oligomeric form, ideal for infiltrating the microporous PBZT network.

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Figure 19 illustrates how water in coagulated film is replaced by solvent in a solvent- exchange process. 100 percent water-swollen film is exchanged in stepwise fashion for 100 percent solvent such as tetrahydrofuraπ (THF) or methanol to prevent the microporous PBZT structure from collapsing. The open structure then allows the monomers to infiltrate and encapsulate the microfibrillar network throughout the film during the curing process. Infiltrated PBZT tubes are dried in a tube furnace for 5 hrs. at 200°F under axial tension and radial pressure to drive off the excess solvents. After drying, the tubes were removed and slit open in the machine direction into flat sheets. The resin- impregnated PBZT film was then ready to be fabricated into honeycomb cores.

3.2.3 Fabricating the Honeycomb Cores

A mold was specially designed by Foster- Miller and machined of 420 stainless steel. Figure 20 shows the two halves of the mold. The upper and lower pieces consist of corrugated channels shaped as 1/8 in. hexagonal cells when closed and viewed end-on. A PBZT sheet 4 in. wide x 6 in. long x 1 to 1.5 mil thick can be placed in the Teflon-coated mold to yield a 12-cell corrugated sheet.

The procedure for fabricating the core consists of several operations. First, two 6 in. sheets of PBZT/PMR-15 or PBZT/Tactix prepregs (referred to generally as PBZT/TS, where TS stands for "thermoset resins", although PMR-15 is considered to be psuedo- thermoplastic) are cut from the slit tube. Two sheets

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of 4 x 6 in. film will yield a 1.5 in. W x 3.0 in. L core of 0.5 in. height. Steps to complete the process include thermoforming, application of primary node and secondary node adhesive, and bonding of facesheets, for example uniaxial (0 deg.) 2-ply graphite/epoxy facesheets.

Thermoforming

A thermoforming operation cures the resins in the PBZT film to "lock" in the hexagonal geometry of the PBZT/TS sheets. To do this, the two 4 x 6 in. sheets of the TS "prepregs" are placed in between the two halves of the mold (which is slightly separated by a gap of 0.050 in.). One-eighth inch diameter x 8 in. long Teflon rods are then inserted in between the sheets as shown in Figure 21. Due to the relatively great thermal expansion of the compliant Teflon rods, they will expand upon heating, forcing the PBZT/TS film to conform to the exact geometry of the mold during the processing cycle. The mold is then placed, for example, in the programmable MTP 14 Tetrahedron press with active cooling. Figures 22(a) and 22(b) give the cure cycle used for each resin system. In each case, a pressure of 100 psi is applied to the mold throughout the cycle. Fully cured, corrugated PBZT/TS sheets are produced at the end of the thermoforming cycle.

Primary and Secondary Bonding

The primary bond is the first of two bonding steps required to complete the core. In this step, the two thermoformed PBZT/TS sheets are bonded

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together to form a single layer hexagonal sheet as shown in Figure 23.

Hysol's EA93 6 aerospace adhesive is used for node bonding. This is a one-component paste bisphenol-A-based epoxy adhesive that has high peel strength and high shear strength. The adhesive cures in 1 hr. at 250°F.

Primary Bonded Single

Layer Hexagonal Cellular Sheet To prepare the PBZT/TP sheets for bonding, the mold is again used to align the sheets and apply even pressure along the 6 in. long bond line. To minimize running of the adhesive into the interior of the cell walls, the 1/8 in. diam. Teflon rods are, again, inserted between the PBZT/TP sheets. The assembled mold is then placed in the Tetrahedron press and the adhesive is cured under an applied pressure of 100 psi. Very smooth, consistent bond lines are achieved with this method.

Secondary Bonding

Once the primary bond lines are cured, 0.5 in. wide strips are carefully sliced from the hexagonal cellular sheets as shown in Figure 24. Adhesive is applied along the 0.5 in. long bond lines on the outward-facing outer surfaces of the individual strips, and then the individual strips are stacked up. Teflon rods are inserted, again, to contain the adhesive at the bond nodes. Curing of the adhesive is carried out at 250°F. This final step produces a 3 in. L x 1.5 in. W x 0.5 in. thick PBZT/TS honeycomb core.

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Application of Graphite/Epoxy Facesheet

Graphite/epoxy was selected as the facesheet material based on our design analysis. The AS-4/3501-6 composite is well characterized and, at 0.056 lb./in. , complements our object of fabricating an ultralightweight PBZT/TP sandwich structure. Application of the graphite/epoxy facesheet is straightforward.

The facesheets can also be made of the core film material.

Two AS-4/3501-6 prepregs were laid-up and cured according to standard curing cycle in an autoclave. The unidirectional panels were cut into 1.5 in. W X 3.0 in. L facesheets with the fibers along the L direction. A thin coating of the EA9346 adhesive was spread on the facesheet and the core carefully placed on top. Only one facesheet at a time was applied and cured so as to minimize any running of adhesive into the interior of the cell walls. Twelve samples of a 1.5 in. W x 2.0 in. L x

0.5 in. thick PBZT/TS sandwich with graphite/epoxy facesheets were fabricated. Six were of the PBZT/Tactix type and the remainder PBZT/PMR-15.

3.3 Testing and Characterization In this task, a test matrix for PBZT/TP sandwich structure was designed to correlate experimental values with those of the design analysis. Tensile and modulus properties were measured for neat PBZT and PBZT/TS films to study the effects of impregnation of films with resins. Stiffness

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properties were derived from four-point flexural tests of the novel PBZT/TS sandwich structures. Also, the sandwich structures were subjected to flatwise compression tests to determine compression modulus. Finally, thermomechanical analyses were conducted to determine coefficient of thermal expansion for the sandwich structures. Test results as well as a study on optimizing the ULW PBZT/TS sandwich structures is discussed.

3.3.1 Tensile Testing of Neat

PBZT and Impregnated PBZT Film

Tensile tests were conducted for both neat

±45 deg. biaxially-oriented PBZT film and for films impregnated with Tactix and PMR-15 resins. Two sets of neat PBZT films were stage dried according to cycles used for curing Tactix and PMR-15 resins (see subsection 3.2.2.) to act as controls for the impregnated films. The impregnated films were also cured under pressure according to the cure cycle for each resin. This provides a comparative measure between neat and treated films.

A 20K universal testing machine was set up with a 100 lb. load cell and cross-head mounted extensometer. Tests were conducted in accordance with the ASTM D882/11-86 standard for tensile properties of thin plastic sheeting. A strain rate of 10 percent/min. was applied to the samples.

The results of tensile testing are summarized in Table 3-4 along with modulus values. Figures 25 through 28 show typical load-versus- extension curves for both neat and impregnated PBZT films tested in machine direction (MD).

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A decrease in modulus and increase in elongation of impregnated PBZT is apparent over that of neat PBZT films. Even in low quantities (about 10 percent volume), the PMR-15 and Tactix resins have an pronounced effect on the properties of PBZT/TS microcomposites. Both films show greater than 60 percent loss in modulus. Of interest is that for PMR-15 impregnated films, only a 24 percent loss in tensile strength was noted compared to 61 percent loss in Tactix 695. Furthermore, the films should have similar tensile strengths when tested in either machine-(MD) or transverse-(TD) direction. So despite the loss in strength and modulus of both impregnated PBZT films, the PMR-15 polyimide resin shows promise as a secondary material for PBZT microcomposites.

All samples failed in shear along the ±45 deg. axis to machine direction (or transverse direction). An interesting feature is noted on some of the load-extension curves. Figure 29 shows such a curve for a PBZT/PMR-15 tensile specimen. There are two regions where failures take place. Region I shows one of the two ±45 deg. "uniplies" of PBZT "laminate" (as discussed in subsection 3.1) failing in shear. Once the first uniply has failed, the load is taken up by the second ply of higher shear strength, which sustains the applied load until total failure occurs.

3.2.2 Four-point Flexural Text of PBZT/Tp Sandwich Structures

Four-point flexural tests were conducted for the PBZT/Tp sandwich structures. Two-ply unidirectional AS-4/3501-6 facesheets were applied to

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all samples tested. Prior to testing, core densities were determined based on dimensions of the cores: t * 1.47 mil (average) d = 0.125 in. h = 0.50 in.

L = 3.0 in. W - 1.5 in. and their actual weight (without the Gr/p facesheets). As indicated before, test specimens were fabricated to meet ASTM C-393 standards for flexure test of flat sandwich construction. Test specimens were loaded at two-quarter span points, as Figure 30 illustrates. Data taken from the load-deflection curves shown in Figures 31(a) and 31(b) were used to determine sandwich stiffness, core shear strength, and modulus.

Deflection was measured at the midpoint of the lower facesheet. Three samples of PBZT/Tactix and four of the PBZT/PMR-15 were subjected to flexural testing. When a typical specimen was subjected to four-point loading, local buckling and 45 deg. diagonal striations of microfibrils were noted at the PBZT/TS core walls. These elastic instability features were constrained to the region between the upper and lower loading bars. This is an excellent example of a hexagonal core sandwich undergoing core shear. No other failure modes, such as debonding of facesheets or facesheet failure, were noted. This demonstrates that the facesheet's material and adhesive are compatible with the PBZT/TS material.

Table 3-5 tabulates core density, shear strength, and modulus of the PBZT/TS sandwich structures. The PBZT/PMR-15 core exhibits higher shear

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strength and superior shear modulus over that of

PBZT/Tactix 695 cores.

The following gives a method for calculating core shear modulus G'c. Sandwich stiffness, D, is calculated using typical modulus properties of the AS-4/3501-6 facesheet material.

Equation 3.1 can be rewritten to solve for shear stiffness, N, in terms of maximum load, P, and deflection, y: KsPaD

N = = Eq.c.l

D - KbPa ^J

Core shear modulus, G' , then is found as: (14)

2N G' = Eq.c.2 ^c (h+c)b using variables previously defined under subsection

3.1.

The validity of core shear modulus, G' is checked by comparing the contributions to total deflection, Y _τ , by Y _β (due to bending) and Y _g (due to shear), that is:

The short specimen geometry of the honeycomb core was specifically designed so that the deflection due to shear, Y , would yield a greater contribution to overall deflection, Y., that the deflection due to bending, Y_. That is, Y > Y _β . In fact, calculations for Ys_ and Y o _n in Equation 3.1 of subsection 3.1 give a ratio of Y : Y_ of approximately 3.5 : 1.0. The PBZT core does behave as a beam undergoing shear.

Table 1-1 (mentioned previously) compares properties of PBZT/PMR-15 cores with other commercially

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available cores. While core shear strength is low, we have demonstrated, through design analysis and testing, that a core of high shear modulus can be achieved with thin film PBZT/PMR-15. Specific shear stiffness as high as 34 x 10 in. (8.6 x 10 m) has been recorded. Furthermore, copious use of adhesive in node bonding would allow further reduction in core weight for improved specific stiffness. Theoretical core density of PBZT core with 0.0015 in. thick core walls and 0.125 in. cell size is 3.19 pcf. However, this does not take the adhesive's weight into consideration. Using typical bond lines of 5 to 7 mils (11) for Hysol's EA 9346 adhesive, calculations show that adhesives should account for only 34 to 40 percent of total core weight. As an example, consider the 5.68 pcf

PBZT/PMR-15 core. Optimizing this core for adhesive content would give a 29 percent reduction in weight. If the 4.04 pcf core exhibits the same shear stiffness of 112.6 Ksi, its specific shear stiffness would increase significantly to over 40 x 10 in. Finally, thin-walled (less than 5 mil) PBZT cores can be fabricated with cell size of 1/8 in. or less and yet achieve low core density (5 pcf or less) required of " ultralightweight structural design. The thin, high- modulus core walls and small cell size minimize facesheet wrinkling and dimpling. This allows future designs to use thin, high-modulus facesheets such as PBZT or PBO, giving further reduction in weight.

3.3.3 Flatwise Compressive Strength and Modulus Flatwise compression tests were conducted for two PBZT/PMR-15 honeycomb cores. Both samples

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exhibit low values of compressive strength and modulus compared to Gr/Ep and 5052 aluminum cores. A discussion on improving compressive strength and modulus by improvements in design and fabrication techniques is presented in this subsection.

Figure 32 is a schematic diagram of a test set-up using self-aligning discs for loading of samples. 3.0 in. L by 1.5 in. W samples were subjected to a constant loading rate of 0.025 in./min. Deflection was measured from a cross-head mounted extensometer. Samples were loaded until steady-state loading was reached.

The low compressive strength and modulus observed can be attributed to the design and hand fabrication of the PBZT cores. The ±45 deg. core walls are designed to provide a sandwich structure of high shear stiffness. The high shear modulus film has a low Young's modulus, E^, as predicted by laminated plate theory. The effect is that the microfibrils, being off-axis to loading direction, contribute very little resistance to loading. Furthermore, the cell walls between nodes buckle at a relatively low stress level, which requires the nodes to operate at a higher stress level than that of a uniform stress distribution of the total cell wall cross-section (2) .

In terms of test standards, the small samples (1.5 in W x 3.00 in. L) tested have an aspect ratio (L to W) , of 2 to 1. This introduces large edge effects, leading to instability at the edges of the core during loading and hence, low resistance to load. Standards call for sample sizes to be at least 4 x in. to minimize these effects.

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Finally, since reticulating adhesive was not used for bonding facesheets to core, the handmade cores have stress concentrations. Figures 34(a) and 34(b) show how inconsistent bond lines would lead to local buckling of the thin-film core wall due to nonuniform stress loading during flatwise compression.

3.3.4 Coefficient of Thermal Expansion

Coefficient of thermal expansion (CTE) was measured for both PMR-15 and Tactix impregnated honeycomb sandwich cores in out-of-plane direction. Samples show near-zero CTE behavior over a wide temperature range of -50°C to +150°C.

0.0625 in. square (40.3 mm ) samples were extracted by cutting along the cell axis direction from bulk PBZT honeycomb sandwich cores with AS-4/3501-6 facesheets and mounted in a modified quartz glass sample holder. CTE's in the cell axis direction were measured from -50 to +150 ^β C with the Perkin-Elmer thermal mechanical analyzer (TMA) . Table 3-7 compares the results of CTE measurements for the two samples against other honeycomb cores.

Dimensional control of platforms for SDI space-based applications requires materials with high specific stiffness and near-zero CTE. Honeycomb core sandwich structures using PBZT as the structural material can achieve these goals. In addition to high specific shear stiffness (34 x 10 in.), we have demonstrated that near-zero CTE is possible for PBZT honeycomb sandwich structures.

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4. Conclusion

We have demonstrated, through design and testing, that an ultralightweight honeycomb sandwich core with high specific stiffness properties can be fabricated from ultrathin, biaxially-oriented PBZT film. The dimensionally stable core will allow platform-mounted tracking and surveillance systems to maintain accuracy and precision under constant thermal cycling. The potential for rapid fabrication and scale-up will enhance stiffness properties as optimum weight adhesive and consistency in bonding will eliminate built-in areas of stress concentrations and local buckling failures at the core walls.

4.1 Further Embodiments of PBZT Honeycomb Core The PBZT honeycomb core can be scaled-up for low-cost, high production rate manufacturing using currently available fabrication techniques, including Foster-Miller's techniques for processing thin, biaxially-oriented ordered-polymer films such as PBZT and PBO from lyotropic solutions, mentioned above.

High speed personal computers (PCs), microprocessors and state-of-the-art sensors can be used for "smart" processing of biaxially extruded ordered-polymers (both thermotropic and lyotropic liquid crystalline polymers). Tight control over the film's orientation and processing conditions plus feedback loops permits high-performance, high-quality films to be extruded for subsequent processing into stiff, ultralightweight structures. Other continuous corrugating methods can be employed. For example, a corrugating process

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illustrated in Figure 35 for fabricating ultralightweight cores takes the extruded films through impregnation, thermoforming, adhesive application and stacking for final cure at a high production rate. Novel cutting tools, such as excimer lasers and high- pressure water jets, allow thin-walled honeycomb cores having complex contours to be machined to tight geometrical tolerances as required of parabolic antenna dishes, optically flat benches and arrays. The ordered-polymer films, such as PBZT and

PBO, can be tailored by the impregnation process with respect to their strength and stiffness properties. Experimentally determined elastic constants of the ordered-polymer films provide direct comparison of their behavior with laminated plate theory. Resin contents of impregnated films can be varied to determine the extent of property loss as a function of the volume percent of resin used. The coefficient of thermal expansion may also be affected. A higher resin content may lead to higher or lower CTE, depending on the specific resin system used. Finally, various high- performance, psuedo-thermoplastic resins, such as PMR- 15, are usable as compatible matrices. These variations have the potential of further improving the performance of ULW structures.

Larger core sizes (up to 6 x 6 in.) can allow other stiffness properties to be controlled. In- plane buckling as well as plate shear performance can be improved. Improvements in fabricating cores and larger sample size will improve flatwise compression modulus. Core walls of different orientations and thicknesses can be specified, depending on specific

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performance requirements, to test the predictions of the design analysis. Finally, different facesheet materials can be applied to the core to provide different sandwich stiffness properties. As small cell sizes (0.125 in. or less) are now possible, ultrathin facesheet materials such as PBZT or PBO can be applied to the already ultralightweight PBZT cores for further improvements in specific stiffness properties.

The high-modulus, ordered-polymer film represents a new class of high performance structural materials that meets the severe requirements of space- based SDI systems. Ordered-polymer films can be applied to other ultralightweight structures of unique designs, such as those illustrated in Figures 5(a)- 5(g).

Although the present invention has been described in relation to particular embodiments thereof, the scope of the appended claims is not limited by the specific disclosure herein, bur rather includes many variations and modifications and other uses, which will become apparent to those skilled in the art.

REFERENCES

1. Andriulli, J.B., et al., Annual Program Resort: Thermoplastic Composites for Space

Applications. Oak Ridge Nat'l Lab., Oak Ridge, TN, September 1988, pp 6-15, 20, 29-31.

2. Haplin, J.C., Primer on Composite Materials: Analysis. Techno ic Publishing, 1984, pp 1- 33.

3. Lusignea, R. , J . Racich , and W. Ishida , Processing of Rod-Like Polymers , Interim Report , October 1983-1985 , AFWAL-TR-86-4046.

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4. Lusignea, R. , and J. McCoy, Ordered Polymers for Large Mirror Substrates, Final Report, January 1985-November 1986, AFWAL-TR-87-4029.

5. Harris, B., Engineering Composite Materials, The Institute of Metals, 1986.

6. Tsai, S.W. and H. Thomas Hahn, Introduction to Composite Materials, Technomic Publishing Co., 1980, pp. 1-98.

7. Bruhn, E.F., "Sandwich Construction and Design," Analysis and Design of Flight Vehicle

Structures, Tristate Offset Company, Cincinnati, OH, 1965, pp cl2.2-cl2.7.

8. Bitzer, T.N. , and J.J. Castillo, "Graphite Honeycomb," Proceedings from 33rd International SAMPE Symposium, March 7-10, 1988, pp 73- 77.

9. Vinson, J.R. , and S. Shore, "Methods of Structural Optimization for Flat Sandwich Panels," U.S. Naval Air Engineering Center Technical Report NAEC-ASL- 1083, 1965.

10. Vinson, J.R. and Sierokowski, Composite Materials and Their Use as Structures, Wiley & Sons, 1975, pp 82-83, 104-113.

11. Klapprott, David, Hysol Corporation, personal communication, March 1989.

12. Rosen, B.W. , "A Simple Procedure for Experimental Determination of the Longitudinal Shear Modulus of Unidirectional Composites," J. of Composite Materials, October 1972, pp 552-554. 13. Tsai, S.W., Composites Design, United

States Air Force Materials Laboratory, Think Composites, Dayton, OH, 1986, pp 7-1 - 7-18.

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14. Schwartz and Rosato, "Structural Sandwich Construction," Composite Engineering Laminates. A.G. Dietz, ed. , MIT Press, 1960, pp 173- 174.

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Table 1-1. Honeycomb Core Properly Comparison Based on 5.0 pcf, 0-50 in. Thick Cores

'Value based on results of four point flexural test (ASTM C-393). All other values reported based on plate shear test in flatwise plane (ASTM C-273).

Table 1-2. Coefficient of Thermal Expansion (CTE) for Several Honeycomb Cores of 10 v/o Resin Content

Table 3-2. Honeycomb Property Comparisons (all 5.0 pcf, 0.50 in. Thick Cores)

Plate Shear

Compression Stabilized "L" Direction "W" Direction

Core type Strength Moduius Strength Moduius Strength Moduius

(psi) (Ksi) (psi) (Ksi) (psi) (Ksi)

Graphite (HFT-G) 940 103 455 92 290 35

Aluminum

(5052) 645 180 410 78 262 34

Fiberglass (HFT) 775 60 410 36 200 13

"Nomex" (HRH-10) 810 45 325 11 175

Table 2-1. Specific Stiffness for PBZT, PBO Films and Gr/Ep or Tp Composites

Density Tensile Modulus Specific Stiffness g/cc lb in. ³ GPa Msi m x 10 ⁶ iπ. x 10 ^β

Anisotropic PBZT film [uniaxial]

PBO film [uniaxial]

Gr/Ep or Tp 1.58 0.056 251 36.4 16.5 6.5

[0 deg] High moduius

Quasi-isotropic

PBZT film 1.55 0.055 27 3.9 1.8 0.7

[balanced biaxial] 137 ^* 20 ^* 8.1 ^* 3.2 ^*

Gr/Ep or Tp 1.58 0.056 81 11.8 5.3 2.1

[quasi-isotropic]

'target values

Table 3-3. Theoretical Stiffness Properties for j45 deg = θ Biaxially-Oriented PBZT Film

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Table 3-1. Calculated Values for Biaxial PBZT Film using Laminate Plate Theory

Table 3-4. Tensile Strength and Modulus for +45 deg Neat PBZT and PBZT Tp Films, Tested in Machine (MD) and Transverse Direction (TD)

Note: All modulus values corrected to 7.0 in. gage length

WO 91/02646 ^{" δ3 "} PCT/US90/04578

Table 3-5. Core Density, Strength and Stiffness Properties for Two PBZT Ts Cores

Table 3-6. Flatwise Compressive Strength and Modulus for PBZT/PMR-15 Honeycomb Core with 0.5 in. Core Thickness

Density Compressive Compressive

Core Type (pcf) Strength (psi) Modulus (Ksi)

PBZT/PMR-15 5.20 330.0 13.7 PBZTPMR-15 5.14 322.0 13.4

Table 3-7. Coefficient of Thermal Expansion (CTE) for Several Honeycomb Cores of 10 v/o Resin Content