# Optimal design for high-temperature broadband radome wall with symmetrical graded porous structure.

1. INTRODUCTIONA radome [1-5] is applied to protection of the delicate antennas mounted on diverse aircraft, such as airplanes or missiles, from severe environments. Those radomes used on supersonic or hypersonic aircraft, may encounter high levels of mechanical and thermal loadings [6]. For example, the radome has to withstand a high temperature of more than 1400[degrees]C, if the aircraft is flying at a velocity of more than 5 Mach [7]. More predominantly, the radome must not interfere with the utility of the antenna, which is responsible for communication, detection or imaging [8-11]. Thus, the material that makes up the radome is required to possess relatively low dielectric constant, low dielectric loss, excellent mechanical and thermal properties. A material with better mechanical and thermal properties, however, does always exhibit higher dielectric constant. Such contradiction demands optimal design for radome wall structures, especially for high-temperature broadband applications.

[FIGURE 1 OMITTED]

Nowadays, radome wall structures, as shown in Fig. 1, involve thin wall, half-wavelength wall, A-sandwich, B-sandwich, C-sandwich and multilayer structures [12-14]. The thin wall structure has relatively low mechanical properties especially for high frequency employments, since its thickness is less than 5% of the operating frequency wavelength. The half-wavelength wall, which is one-half wavelength thick, has a narrow bandwidth of only 5%, and is not suitable for broadband use. Sandwich structures composed of different dielectric layers are commonly applied, due to their broadband properties and high strength-to-weight ratio. For instance, an A-sandwich structure (Fig. 1(c)), which consists of a lightweight and low-permittivity foam core and two dense thin facings, has relatively lower weight but higher strength. This kind of structure has better broadband transmission ability than single-layered structures, and is always employed upon frequencies less than 20 GHz [13].

In high-temperature environments, extreme thermal stress may occur at interfaces of sandwich structures, due to significant temperature gradients and laminations. Sandwich structures are made of several layers with distinct mechanical and thermal properties. Such differences between two bordering layers under high-temperature conditions will result in thermal mismatch stress, which may be the critically vital factor for radome destruction. Since the 1990s, functionally graded materials have been investigated, since their functionally graded designs can efficiently help reduce thermal stress [15-17]. Hence, a symmetrical graded porous structure (Fig. 2(a)) for high-temperature broadband applications is put forward in this paper.

[FIGURE 2 MITTED]

This study carries out investigations on electromagnetic and thermo-mechanical properties of a symmetrical graded porous structure. The transmission efficiency of the proposed structure in the 1-100 GHz frequency range is investigated by the transfer matrix method [18] based on the electromagnetic theory. The thermo-mechanical property of the structure, which is a temperature-dependent problem, is investigated via numerical simulation. Results suggest that the symmetrical graded structure has broadband ability in the 1-100 GHz range, and succeeds in withstanding high-temperature conditions. Its electromagnetic and thermo-mechanical properties are demonstrated to be better than that of the A-sandwich structure for comparison.

2. SYMMETRICAL GRADED POROUS STRUCTURE

In this study, a symmetrical graded porous structure, as shown in Fig. 2(a), is proposed. The position-dependent porosity increases continuously from the outermost and innermost surfaces to the middle of the structure. For simulation simplicity, the proposed structure is assumed to be composed of plenty of layers. Each layer is equal in thickness and has a homogeneous porosity. The porosity distribution is given by the following equation as

[P.sub.i] = [P.sub.m] [(i - 1/m - 1).sup.n] (i = 1,2, ..., m), (1)

where m is one half of the total layer number ([2.sub.m]), [P.sub.i] is the ith layer porosity and n is the graded index that determines how fast or gradually the porosity varies due to position variation. For a symmetrical structure, one may derive the porosity of each layer to be

[P.sub.i] = [P.sub.2m+1-i] (i = 1, 2, ..., 2m). (2)

From Eqs. (1) and (2), the outermost and innermost layer porosities [P.sub.1] and [P.sub.2m] are both evaluated as zero, which means that the outermost and innermost layers are made of fully dense material. In this study, the intermediate layer porosity Pm or Pm+1 is the maximum porosity, and will be given in Section 3.1. Fig. 3 depicts porosity distributions of the symmetrical graded porous structure as the graded index n varies. It is seen that the porosity decreases simultaneously in each layer when the graded index becomes greater, except for P1, Pm, [P.sub.m+1] and [P.sub.2m], which are given as fixed values. If the graded index tends to zero, each layer excluding the outermost and innermost layers, has a porosity equal to the maximum porosity [P.sub.m] or [P.sub.m+1.] Thus, the whole structure resembles an A-sandwich structure with a thick foam core and two extremely thin dense skins bounded to the core on its two sides. As the graded index n tends to be infinite, all layers, except for the mth and (m + 1)th layers, are fully-densely made. The structure turns to be a sandwich structure with two thick skins and an extremely thin core in this situation.

A traditional A-sandwich structure (Fig. 2(b)) is applied to comparison with the proposed symmetrical graded porous structure (Fig. 2(a)) in this study. It is assumed that the two structures are made of the same material with the same mass. Once the skin and core porosities [P.sub.s] and [P.sub.c], the skin and core thicknesses [d.sub.s] and [d.sub.c] of the A-sandwich structure are given, the thickness of each layer [DELTA]d in the proposed structure can be derived as

[DELTA]d = (1 - [P.sub.s]) x [d.sub.s] + (1 - [P.sub.c]) x [d.sub.c]/[2m.summation over (i = 1)] (1 - [P.sub.i]) (3)

Once the graded index n is given, [P.sub.i] can be determined by Eqs. (1) and (2). Subsequently, [DELTA]d can be evaluated from Eq. (3). And the entire thickness of the symmetrical graded porous structure is obtained as

d = 2m x [DELTA]d. (4)

It is seen that the entire thickness d depends on the graded index n, if the mass of the whole structure is given.

[FIGURE 3 OMITTED]

[FIGURE 4 OMITTED]

3. METHODS

3.1. Transfer Matrix Method

The transfer matrix method (TMM) [18] is used to investigate electromagnetic property of the symmetrical graded porous structure, since it exhibits high efficiency in dealing with transmission and reflection problems of a stratified medium. Consider a plane wave incident upon a stratified medium with boundaries at z = [z.sub.0], [z.sub.1], ..., [z.sub.2m], as shown in Fig. 4. It is assumed that the 0th and (2m + 1)th layers are half-infinite, and in this study they are air media. The transfer matrix method displays the relationship between the incident, reflected and transmitted waves as

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII], (5)

where [[V.sub.i]] is the forward propagation matrix, [A.sub.0], [B.sub.0] and [B.sub.2m+1] represent the amplitudes of the reflected, incident and transmitted waves respectively. Thus, the transmission efficiency is found to be

[t.sub.e] = 1/ [[absolute value of [V.sub.22]].sup.2]. (6)

Before using Eq. (6) to estimate the transmission efficiency of the symmetrical graded porous structure, one should first obtain the permittivity of each layer. The permittivity of porous material can be evaluated by Maxwell-Garnett's Formula [19]:

[[epsilon].sub.i]/[[epsilon].sub.1] = 1 + 3[P.sub.i]/3[[epsilon].sub.1] / (1 - [[epsilon].sub.1]) + (1 - [P.sub.i]), (7)

where [[epsilon].sub.1] is the permittivity of the first layer with fully dense material, and [[epsilon].sub.i] is the ith layer permittivity. In this study, silicon nitride is chosen as the construction material, for it has excellent thermal and mechanical properties with relatively low permittivity. The permittivity of fully dense silicon nitride is approximately 8.0 [20]. Hence the ith layer permittivity can be estimated by Eq. (7), if [P.sub.i] is given.

[FIGURE 5 OMITTED]

As for the A-sandwich structure for comparison, the thicknesses [d.sub.s] and [d.sub.c], the permittivities [[epsilon].sub.s] and [[epsilon].sub.c] are chosen as 0.6 mm, 5.6 mm, 8.0 and 2.0 respectively. The porosities [P.sub.s] and [P.sub.c] estimated by Eq. (7) are 0% and 81.0% respectively. Fig. 5 shows the transmission efficiency of the A-sandwich structure in the 1-100 GHz frequency range by TMM. It is seen that the structure is feasible for employments in the 1-12 GHz and 82-96 GHz frequency ranges. In the 12-82 GHz range, however, the structure is limited in its ability to provide sufficient transmission efficiency.

In this study, the outermost and innermost layers of the symmetrical graded porous structure are assumed to be made of fully dense material, namely [P.sub.1] = [P.sub.2m] = 0. And the maximum porosity [P.sub.m] or [P.sub.m+1] is assumed to be equal to [P.sub.c]. Thus, the transmission efficiency of the proposed structure only depends on the graded index n. And we can investigate the effect of the graded index on the transmission efficiency using TMM.

3.2. Method for Steady Temperature Field

The steady temperature field should be obtained in advance before estimation of the steady thermal stress field. As shown in Fig. 4, the temperature at the interface z = [z.sub.i] is assumed to be [T.sub.i], which is a variable to be determined. The boundary conditions for the steady heat conduction problem are [T.sub.0] = 1400[degrees]C and [T.sub.2m] = 20[degrees]C. As for the ith layer, the one-dimensional steady heat conduction equation is given as

d/dz [[lambda](T, [P.sub.i]) dT/dz] = 0, (8)

where [lambda] (T, [P.sub.i]) is the temperature-dependent and porosity-dependent thermal conductivity. The thermal conductivity due to porosity variation [21] is given as

[lambda](P) = [[lambda].sub.0](1 -P)/1 + P/2, (9)

and the thermal conductivity due to temperature variation [22] is presented by

[[lambda].sub.0](T) = (43.03 x [e.sub.-T/495-59] + 15.64) W/(m x [degrees] C). (10)

By substituting Eq. (10) into Eq. (9), the double-variable-dependent conductivity is obtained as

[lambda](T,P)= g(P) x [[lambda].sub.0](T), (11)

where g(P) = 1 - P/1 + P / 2 is the porosity factor. Substituting Eq. (11) into Eq. (8) yields

d/dz [g([P.sub.i]) x [[lambda].sub.0](T) dT/dz] = 0. (12)

The implicit solution for Eq. (12) is found to be

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (13)

where [MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (T) is a primitive function of X0 (T), Mi and Ni are constants to be determined.

At the boundary z = [z.sub.i] (i = 1, 2, ..., 2m - 1), one may obtain

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (14)

The boundary condition leads to

[M.sub.1] = [M.sub.2] = ... = [M.sub.2m] = M. (15)

For the ith layer, we may obtain the following equations:

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (16)

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII]. (17)

By subtracting Eq. (17) from Eq. (16), one can obtain

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (18)

Thus, one may have

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (19)

Hence, M can be determined as

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (20)

By substituting Eq. (20) into Eq. (13) and using the boundary conditions, [N.sub.i] can be determined. Thus, the implicit solutions for the steady temperature filed are acquired.

3.3. Method for Stress Field

For thermo-mechanical optimal design, the thermal stress field in the steady temperature field is to be calculated. The strain only depends on z and can be written as

[epsilon](z) = [epsilon](0) + k x z, (21)

where [kappa] is the curvature and [epsilon](0) is the strain at z = 0. And the thermal stress [23] is found to be

[sigma](z) = E(T, P)/1 - v(T, P) [[epsilon](z) -[alpha](T, P) x [DELTA]T] = E(T, P)/1 - v)T, P) [[epsilon](0) + k x z - [alpha](T, P) x (T - 20[degrees]C)], (22)

where the temperature-dependent and porosity-dependent parameters E (T, P), v (T, P) and [alpha] (T, P) are the Young's modulus, Poisson's ratio and linear expansion coefficient, respectively. It should be emphasized that the temperature T and the porosity P in Eq. (22) are functions of the coordinate z.

The linear expansion coefficient a, Young's modulus E, Poisson's ratio v and strength [sigma]F due to porosity variation [24-26] are as follows:

[alpha](P) = [a.sub.0], (23)

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (24)

v(P) = [v.sub.0], (25)

and

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (26)

where [[alpha].sub.0,] [E.sub.0], [v.sub.0] and [[sigma].sub.F0] are the fully dense material parameters respectively. The parameters due to temperature variation of [Si.sub.3][N.sub.4] ceramic [21, 27-29] are as follows respectively:

[alpha]0(T) = 2.85 x [10.sub.-6]/[degrees]C, (27)

[E.sub.0](T) = 320.4 - 0.0151 * (273.15 + T) x [e.sup.-445/(273.15+T)](GPa), (28)

[v.sub.0](T) = 0.267 (29)

and

[[sigma].sub.F0](T) = 1.03 - 8.26/(1505.20 - T)(GPa). (30)

By substituting Eqs. (27) ~ (30) into Eqs. (23) ~ (26), the material parameters as functions of T and P are obtained as follows:

[alpha] = [[alpha].sub.0], (31)

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (32)

v = [v.sub.0], (33)

and

[[sigma].sub.F](T, P) = [[sigma].sub.F0] x [e.sub.- [beta] x P] (34)

where [beta] = 4.24 [30]. The linear expansion coefficient and Poisson's ratio obtained are not relevant to neither temperature nor porosity.

For free mechanical boundary conditions, the force and moment equilibrium equations are as follows:

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (35)

and

[MATHEMATICAL EXPRESSION NOT REPRODUCIBLE IN ASCII] (36)

We can solve Eqs. (35) and (36) for k and [epsilon] (0). Thus, the thermal stress field can be given by Eq. (22).

4. RESULTS AND DISCUSSION

In this section, investigations both on electromagnetic and thermal-mechanical performances of the symmetrical graded porous structure are enforced by computational simulations. Before the procedure of optimal design, the symmetrical graded porous structure is assumed to be composed of 500 layers, namely m = 250. In fact, five hundred layers are rather sufficient to simulate a structure with continuously graded porosity distribution, because each layer would be merely 0.02 millimeter thick for a radome wall structure with a conventional thickness of approximately 10 millimeters. As discussed in Section 3, the properties of the proposed structure merely depends on the graded index n, in case that the entire mass is given as a constant value. Thus, the influences of the graded index on the electromagnetic and thermal-mechanical properties are simultaneously studied below.

4.1. Effect of the Graded Index on the Transmission Property

The effect of the graded index n on the transmission property of the symmetrical graded porous structure is shown in Fig. 6. The figure manifests a descending transmission ability of the structure due to an increase in the graded index. As the graded index is barely 0.01, which is considerably close to zero, the transmission efficiency maintains a high lever (greater than 80%) in the whole frequency range. Such superior transmission ability results from the fact that the symmetrical graded porous structure tends to be a foam core with two extremely thin facings, if the grade index approaches zero. As the graded index approaches infinity, the graded structure tends to be composed of fully dense material, because the intermediate porous layer is extremely thin and can be neglected. Such a high-permittivity material apparently results in deficiency of transmission ability. The simulation result also indicates that the symmetrical graded porous structure satisfies broadband transmission requirement in the 1-100 GHz range, if the graded index is less than 0.1. It is seen that the graded structure, with a graded index less than 0.1, exhibits much better broadband transmission property than the A-sandwich structure, which is only feasible in the 1-12 GHz and 82-96 GHz ranges.

4.2. Effect of the Graded Index on the Thermo-mechanical Property

Figure 7 shows the stress ratio distributions when the graded index varies. The stress ratio [sigma]/[[sigma].sub.F], due to temperature gradients and laminations, is required to be greater than -1.0 and less than 1.0 in order to withstand high-temperature conditions [31]. For the A-sandwich structure, we can see that the stress ratio at the boundary of the outer skin layer and the core layer is stepped. The stress ratio [sigma]/[[sigma].sub.F] at Point [K.sub.H] in Fig. 7 is merely -0.26, while it is approximately -1.0 ([sigma]/[[sigma].sub.F] = -0.96) at Point [K.sub.L]. The difference of the stress ratios is on account of different strengths due to porosity variation at Points Kh and Kl. It is seen from Fig. 7 that the stress ratio in the symmetrical graded porous structure becomes as low as -2.3 near the outermost skin (at Point [I.sub.L]), if the graded index n approaches zero. In fact, the outermost skin material is fully dense, while the intermediate layer consists of foam material with a maximum porosity, if the graded index is equal to zero. The two bordering layers are significantly distinct in thermal and mechanical properties. Furthermore, the strength of near the outermost skin is relatively low due to high temperature, and the temperature gradient is relatively high as well. All these factors result in the high thermal stress ratio near the outermost layer. As the graded index increases, thermal stress is efficiently reduced, resulting from impaired gradients of thermal and mechanical properties. Fig. 7 also indicates that the symmetrical graded structure is feasible for high-temperature (up to 1400[degrees]C) employments, if the graded index n is in the vicinity of 0.09. It is seen that the thermal stress of the graded structure is reduced in contrast to the A-sandwich structure, especially at the interface between the outermost skin and its bordering layer, where the stress ratio is at a considerably dangerous value (-0.96 at Point [K.sub.L]) for the A-sandwich structure and a relatively safe value (-0.85 at Point [J.sub.L]) for the proposed structure. If a safe factor of about 1.05 is considered [31], the A-sandwich structure would fail to fulfill the requirement of high-temperature conditions. According to the discussion above, we come to a conclusion that the symmetrical graded structure is feasible for high-temperature broadband applications, if its graded index is about 0.09. And its electromagnetic and thermo-mechanical abilities precede that of the A-sandwich structure for comparison.

[FIGURE 6 OMITTED]

[FIGURE 7 OMITTED]

5. CONCLUSION

This study focuses on both electromagnetic and thermo-mechanical optimal design for high-temperature broadband radome wall with symmetrical graded porous structure. Optimal results suggest that the symmetrical graded porous structure possesses the best abilities if the porosity graded index is chosen as approximately 0.09. The symmetrical graded structure is demonstrated to be better than the A-sandwich structure in the broadband transmission ability. And the thermo-mechanical investigation also indicates that the novel structure meets the requirement for high-temperature (up to 1400[degrees]C) applications.

Received 2 March 2012, Accepted 27 March 2012, Scheduled 5 April 2012

ACKNOWLEDGMENT

This work was supported by National Natural Science Foundation of China (Grant No. 91016021, 90816019), National Basic Research

Program of China (973 Program, 2010CB8327001, 2011CB610303), and Foundation of the Author of National Excellent Doctoral Dissertation of China (No. 201029).

REFERENCES

[1.] Kozakoff, D. J., Analysis of Radome Enclosed Antennas, Artech House, Norwood, MA, 1997.

[2.] Persson, K., M. Gustafsson, and G. Kristensson, "Reconstruction and visualization of equivalent currents on a radome using an integral representation formulation," Progress In Electromagnetics Research B, Vol. 20, 65-90, 2010.

[3.] Sukharevsky, O. I. and V. A. Vasilets, "Scattering of reflector antenna with conic dielectric radome," Progress In Electromagnetics Research B, Vol. 4, 159-169, 2008.

[4.] Meng, H. F. and W.-B. Dou, "Fast analysis of electrically large radome in millimeter wave band with fast multipole acceleration," Progress In Electromagnetics Research, Vol. 120, 371-385, 2011.

[5.] Xiao, K., S. L. Chai, and L.-W. Li, "Comparisons of coupled VSIE and non-coupled VSIE formulations," Journal of Electromagnetic Waves and Applications, Vol. 25, No. 10, 1341-1351, 2011.

[6.] Amin, A. M. and R. L. Sierakowski, "Effect of thermomechanical coupling on the response of elastic solids," AIAA Journal, Vol. 28, No. 7, 1319-1322, 1990.

[7.] Chen, F., Q. Shen, and L. Zhang, "Electromagnetic optimal design and preparation of broadband ceramic radome material with graded porous structure," Progress In Electromagnetics Research, Vol. 105, 445-461, 2010.

[8.] Karim, M. N. A., M. K. A. Rahim, H. A. Majid, O. B. Ayop, M. Abu, and F. Zubir, "Log periodic fractal Koch antenna for UHF band applications," Progress In Electromagnetics Research, Vol. 100, 201-218, 2010.

[9.] Xu, H.-Y., H. Zhang, K. Lu, and X.-F. Zeng, "A holly-leaf-shaped monopole antenna with low RCS for UWB application," Progress In Electromagnetics Research, Vol. 117, 35-50, 2011.

[10.] Hong, T., M.-Z. Song, and Y. Liu, "RF directional modulation technique using a switched antenna array for communication and direction-finding applications," Progress In Electromagnetics Research, Vol. 120, 195-213, 2011.

[11.] Zhu, F., S.-C. Gao, A. T. S. Ho, T. W. C. Brown, J. Li, and J. D. Xu, "Low-profile directional ultra-wideband antenna for see-through-wall imaging applications," Progress In Electromagnetics Research, Vol. 121, 121-139, 2011.

[12.] Koetje, E. L., F. H. Simpson, and J. F. Schorsch, "Broadband and high temperature radome apparatus," US Pat., 4677443, Jun. 30, 1987.

[13.] Mackenzie, S. B., "Radome wall design having broadband and mm-wave characteristics," US Pat., 5408244, Apr. 18, 1995.

[14.] Mackenzie, S. B. and D. W. Stressing, "W-band and X-band radome wall," US Pat., 6028565, Feb. 22, 2000.

[15.] Niino, M. and S. Maeda, "Recent development status of functionally gradient materials," ISIJ International, Vol. 30, No. 9, 699-703, 1990.

[16.] Javaheri, R. and M. R. Eslami, "Thermal buckling of functionally graded plates," AIAA Journal, Vol. 40, No. 1, 162-169, 2002.

[17.] Vel, S. S. and R. C. Batra, "Exact solution for thermoelastic deformations of functionally graded thick rectangular plates," AIAA Journal, Vol. 40, No. 7, 1421-1433, 2002.

[18.] Kong, J. A., Electromagnetic Wave Theory, John Wiley & Sons, Inc., New York, 1986.

[19.] Garnett, J. C. M., "Colors in metal glasses and in metallic films," Philosophical Transactions of the Royal Society of London, Series A, Mathematical, Physical & Engineering Sciences, Vol. 203, No. 359-371, Royal Society, London, 1904.

[20.] Huang, X., F. Peng, F. Yan, and H. Tang, "Research on the dielectric properties of composite made with [Si.sub.3]N4-Si[O.sub.2]," Journal of Wuhan University of Technology, Vol. 28, No. 12, 21-23, 2006.

[21.] Zhou, Y., Science of Ceramic Material, Harbin Institute of Technology Press, Harbin, China, 1995.

[22.] Kuriyama, M., Y. Inomata, T. Kujima, and Y. Hasegawa, "Thermal conductivity of hot-pressed [Si.sub.3]N4 by the laser flash method," American Ceramic Society Bulletin, Vol. 57, No. 12, 1119-1122, 1978.

[23.] Miao, X., X. Zhang, B. Wan, J. Han, and S. Du, "Research on thermoelastic problems computation methods of FGM," Journal ofFunctional Materials, Vol. 30, No. 2, 122-125, 1999.

[24.] Kingery, W. D., H. H. Bowen, and D. R. Uhlmann, Introduction to Ceramics, 2nd edition, Wiley, New York, 1976.

[25.] Kondo, R., Porous Materials, Gihodo, Tokyo, Japan, 1973.

[26.] Coble, R. L. and W. D. Kingery, "Effect of porosity on physical properties of sintered alumina," Journal ofthe American Ceramic Society, Vol. 39, No. 11, 377-385, 1956.

[27.] Huseby, I. C., G. A. Slack, and R. H. Arendt, "Thermal expansion of Cd[Al.sub.2][O.sub.4], [beta]-[Si.sub.3][N.sub.4] and other phenacite-type compounds," Bulletin of the American Ceramic Society, Vol. 60, No. 9, 919-920, 1981.

[28.] Bruls, R. J., H. T. Hintzen, G. de With, and R. Metselaar, "The temperature dependence of the Young's modulus of MgSiN2, AlN and Si3N4," Journal of the European Ceramic Society, Vol. 21, No. 3, 263-268, 2001.

[29.] Tomeno, I., "High temperature elastic moduli of Si3N4 ceramics," Japanese Journal of Applied Physics, Vol. 20, No. 9, 1751-1752, 1981.

[30.] Shao, Y., D. Jia, and Y. Zhou, "Effect of porosity on mechanical and dielectric properties of 20% BN/[Si.sub.3]N4 composite porous ceramics," Rare Metal Materials and Engineering, Vol. 38, No. 2, 479-482, 2009.

[31.] Liu, H., Mechanics of Materials, Higher Education Press, Beijing, China, 2007.

L. C. Zhou, Y. M. Pei *, R. B. Zhang, and D. N. Fang

State Key Lab for Turbulence and Complex Systems, College of Engineering, Peking University, Beijing 100871, China

* Corresponding author: Yongmao Pei (peiym@pku.edu.cn).

Printer friendly Cite/link Email Feedback | |

Author: | Zhou, L.C.; Pei, Y.M.; Zhang, R.B.; Fang, D.N. |
---|---|

Publication: | Progress In Electromagnetics Research |

Article Type: | Report |

Geographic Code: | 9CHIN |

Date: | May 1, 2012 |

Words: | 4159 |

Previous Article: | Performance analysis of polarization-space-time three-domain joint processing for clutter suppression in airborne radar. |

Next Article: | An electronically controllable method for radar cross section reduction for a microstrip antenna. |

Topics: |