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Effect of gas blowing on the head of thermal ablation vehicle
Advances in Aerodynamics volume 4, Article number: 10 (2022)
Abstract
The reentry vehicle will encounter thermal ablation, especially at the stagnation point regime. A theoretical work has been done to analyze the thermal effect of gas blowing due to thermal ablation of surface material on the head of a general hypersonic vehicle. By deriving the formulation, research takes into account the effect of gas blowing on the thermal dynamics balance, and then solves them by numerical discretization. It is found that gas blowing will increase the temperature and heat flux at the surface of stagnation point regime.
1 Introduction
Reentry vehicle is crucial for many aerodynamic applications, such as Luna or Moon probe project, etc. One inevitable issue is that the stagnation point of the reentry body usually experiences very high temperature, leading to the thermal ablation problem [1,2,3,4,5,6,7,8,9,10]. The thermal ablation problem is a multiphysics process. In general, the detached bow shock wave forms over the head of hypersonic vehicle [11,12,13], the fluid flow is compressed and its thermal dynamic properties such as density, pressure and temperature increase significantly [14, 15]. The temperature of the air is ten thousand degrees, the air is dissociated electrically and chemical reactions happen simultaneously [16, 17]. Moreover, the solid material on the surface of the vehicle reacts with the ambient fluid flow due to very high temperature, the reaction products are the multicomponent gas, and the noslip and nopenetration wall condition for NavierStokes fluid dynamics model is no longer valid [1, 6,7,8]. This is one of the mass loss mechanisms of thermal ablation. Another mechanism is that, the solid particle erodes from the surface because the high temperature alters the mechanics properties of surface material, and then the ambient fluid flow carries out the surface mass in forms of rod particles [1]. The mass loss mechanism is important, because it changes the aerodynamic geometry of the vehicle; thus the aerodynamic force and heat flux is changed as well [1]. In addition, the solid particles go into the downstream boundary layer, which will affect the transition [18, 19] and turbulence [20, 21] over the surface of the vehicle, making the aerodynamic force and heat flux prediction become complicated [22, 23] to predict. It is worth noting that, the solid material experiences a chemical reaction under high temperature of fluid flow at stagnation point regime [1, 6,7,8]. Therefore, thermal dynamics of single phase stagnation point flow is one of the crucial factors to understand the complicated mass loss process during the thermal ablation.
Research focuses our attention on the near wall of thermal dynamics of the stagnation point regime of a sphere with typical physical properties. According to the dimensionless analysis, the local Mach number in the near wall regime is approximately zero due to the local high sonic speed, so we assume that the stagnation point flow in the very near wall regime of our objective problem is incompressible. If taking incompressible stagnation point flow as a prototype model to study, there are differences. The multiphysics nature of thermal ablation makes the wall inject gas into the stagnation point regime, while the effect of gas blowing on the thermal dynamics is not clear.
Research studies this effect on the thermal dynamics of a compressible stagnation point flow in a typical hypersonic vehicle cruising condition by means of theoretical research, so as to have some qualitative understanding of the thermal ablation problem, paving the way for future study and planning.
2 Physical problem
2.1 Incompressible assumption in the near wall region
Firstly, in order not to lose generality, we consider a prototype of hypersonic incoming flow passing a sphere, with physical properties of air being that of altitude height around 20 ~ 30 km, which is typical parameter ranges where thermal ablation happens, see Fig. 1. By default, all the physical parameters in this paper use the ISO unit. In the current study, the typical incoming flow Mach number is around M_{1} = 8 ~ 20, the density of fluid flow is ρ_{1} = 1.8 × 10^{2} kg/m^{3}, the temperature is T_{1} = 226.5 K, the pressure is p_{1} = 1197.0 Pa, the sound speed is a_{1} = 301.7 m/s, the fluid flow velocity is U_{1} = 6034.0 m/s, the dynamic viscosity is μ_{1} = 1.5 × 10^{−5} Pa ⋅ s, and the kinematic viscosity is ν_{1} = 8.2 × 10^{−4} m^{2}/s. The incoming flow forms a detached shock wave over the sphere which can be seen in many hypersonic vehicles; behind the shock wave, the fluid flow is compressed, its entropy increases, its thermal dynamics properties, such as pressure, density and temperature increase significantly as well, and the chemical reaction of air happens due to high temperature [16, 17]. Having assumed the gas being in a perfect state, research focuses attention on the stagnation point flow region and considers neither the chemical reaction nor the electric dissociation. Therefore, research calculates the flow and thermal dynamics properties by normal shock relations [14, 15], see Eqs. (1)–(6). Let’s take M_{1} = 20 as an example, the properties behind the normal shock wave can be calculated, with the Mach number being M_{2} = 0.4, the density of fluid flow being ρ_{2} = 0.1 kg/m^{3}, the temperature being T_{2} = 1.8 × 10^{4 }K, the pressure being p_{2} = 5.5 × 10^{4 }Pa, the sound speed being a_{2} = 2667.0 m/s, the fluid flow velocity being U_{2} = 1006.0 m/s, the dynamic viscosity being μ_{2} = 1.9 × 10^{4} Pa ⋅ s, and the kinematic viscosity being v_{2} = 1.8 × 10^{−3} m^{2}/s. In addition, it is found that, for M_{1} = 8 ~ 20, the physical properties behind the shock wave are in the same order, and the variations are small.
Secondly, the detached distance of detached shock wave can be estimated by a semiempirical relation [11,12,13], see Eq. (7), which is weakly related to chemical reactions [13, 24, 25]. D is the typical diameter of blunt nose hypersonic vehicle, with D = 0.2m, δ_{h} being the distance of detached shock wave, and δ_{h} = 13.8e − 3m estimated by Eq. (7), see Fig. 1.
Research considers the near wall fluid dynamics behind the shock wave as a stagnation point flow, see Fig. 1. Keep in mind that the fluid flow is a compressible flow, which increases the complexity of the problem. In light of this, research investigates the local Mach number of near wall fluid dynamics of stagnation point flow. The bulk compression rate of stagnation point flow can be estimated as [26,27,28,29] B = U_{2}/δ_{h} ≃ 3.6 × 10^{4}s^{−1 }~ O(10^{4}s^{−1}), with the bulk viscous boundary layer thickness of stagnation point flow being \(\delta =\sqrt{\nu_2/B}\simeq 22.4\times {10}^{5}\,\mathrm{m}\), and the ratio between boundary layer thickness and detached distance being \(\frac{\delta }{\delta_h}\sim \frac{1}{60}\).
Assume that the fluid flow velocity of the stagnation point flow behind the shock wave decreases linearly \(\frac{U_{\tau }}{U_2}=\frac{\delta }{\delta_h}\) within the near wall region Z = O(δ), with the local fluid velocity being \({U}_{\tau}\simeq \frac{1}{60}{U}_2\sim O\left(10\,\mathrm{m}/\mathrm{s}\right)\), and the local sound speed being \({a}_2=\sqrt{\gamma {RT}_2}\sim O\left({10}^3\,\mathrm{m}/\mathrm{s}\right)\). Ultimately, the local Mach number in the near wall region is estimated as \({M}_{\tau}\simeq \frac{U_{\tau }}{a_2}\sim O(0.01)\); thus in the near wall region, the fluid dynamics can be approximately treated as incompressible fluid flow, which gives much mathematical convenience in theoretical analysis in later sections.
2.2 Objective problem: effect of gas blowing on the thermal dynamics of stagnation point flow
Behind the detached shock wave, the fluid flow will have very high temperature T_{2} = 1.8 × 10^{4 }K, the local Mach number is around M_{τ }~ O(0.01), the chemical reaction and electric dissociation will happen as well. For simplification, research considers neither the chemical reaction nor the electric dissociation. The flow behind the shock wave locally forms a stagnation point flow at the head of hypersonic vehicle. Research focuses attention on the near wall of stagnation point flow, where the incompressible assumption will hold, M_{τ}~O(0.01). The current study aims to understand one question: what’s the effect of gas blowing on it.
3 Effect of gas blowing on thermal dynamics at stagnation point region
3.1 Traditional incompressible dynamic and thermal dynamic equations
In the following, theoretical analysis is conducted in the Cartesian coordinate system, where coordinate (x, y) represents (R, Z), and velocity [u, v]^{T} represents [u_{r}, u_{z}]^{T} in Fig. 1, respectively.
Keep in mind that the local Mach number is around zero M_{τ }~ 0, allowing us to use incompressible Hiemenz flow to analyze the thermal dynamics of objective problem.
In order to keep generality, research takes full 2D NS equations to begin, see Eqs. (8)–(9).
In order to better understand the problem, research firstly examines the standard Hiemenz solution without thermal dynamics equation.
Take f(0) = 0, f ' (0) = 0, f '' (0) = 1.2326 to integrate numerically by the RungeKutta 4th order method, the Ordinary Equation System [30], and then theoretical solution can be found as Fig. 2 indicates. Keep in mind that the wall normal velocity v(y) is proportional to ~f(η), the streamwise velocity u(x, y) is proportional to ~x ⋅ f ' (η), and the viscous dissipation \(\frac{\partial u\left(x,y\right)}{\partial y}\) is proportional to ~f '' (η). Inside the viscous boundary layer \(\eta <\frac{y}{\delta_{\infty }}=3\), the dimensionless viscous dissipation f '' (η) is not zero, but the maximum at wall; outside the viscous boundary layer, \(\eta =\frac{y}{\delta_{\infty }}=3\), the dimensionless viscous dissipation f '' (η) vanishes, and dimensionless velocities f and f' become linear strain flow velocities.
3.2 Theoretical derivation of effect of gas blowing and suction on thermal dynamics
For the case of blowing gas from bottom wall at stagnation point regime, the governing equations are Eqs. (15)(18):
Similarily, for the case of suction gas from bottom wall at stagnation point regime, the governing equations are Eqs. (19)(22):
In this section, thermal dynamics balance is controlled by heat conduction and fluid convection. The gas blowing effect will alter the dynamics of stagnation point flow, so as to indirectly influence the thermal dynamics by convection effect. Eqs. (15)–(18) represent the dynamics with gas blowing [31], while Eqs. (19)–(22) represent the dynamics with gas suction [31].
Set f(0) = 0, f ' (0) = 0, f '' (0) = 1.2326 to satisfy the noslip and nopenetration wall boundary condition for standard, blowing and suction cases, the gas injection effect can be represented by dimensionless mass flux f_{w}. Set θ(0) = 0, θ ' (0) = 0.0 for thermal dynamics boundary condition at wall. Then integrate numerically by the RungeKutta 4th order method, the ODE system Eq. (17) and Eq. (18) for blowing case; integrate the ODE system Eq. (21) and Eq. (22) for suction case.
3.3 Results and discussions
Figure 3 shows that, the effect of dimensionless mass flux f_{w} on the wall normal velocity is to increase or decrease the wall normal velocity. Keep in mind that, thermal dynamics balance is controlled by heat conduction \(k\frac{\partial^2T}{\partial {y}^2}\) and fluid flow convection \(\rho {C}_p\mathrm{v}\frac{\partial T}{\partial y}\), and the variation of wall normal velocity profile v(η) will surely alter the thermal dynamics balance.
Figures 4 and 5 show the effect of dimensionless mass flux f_{w} on the dimensionless temperature θ and dimensionless heat flux θ' of stagnation point flow. It is clear that, the blowing increases significantly the temperature and heat flux, while suction does the contrast. This means that: in reality, thermal ablationinduced gas injection will deteriorate the heat environment of hypersonic vehicle. In terms of the effect of suction, the current conclusion is purely academic. In reality, if the very hot fluid flow is sucked into the vehicle body, the heat will be accumulated, which means it is impossible to use suction to actively control the heat over the vehicle surface, although the current study suggests that suction will diminish the surface temperature and heat flux. Nevertheless, it is valuable for basic research, which provides many options and basic knowledge for the final design.
4 Conclusion
Research conducted theoretical analysis on the thermal dynamics of stagnation point flow regime of a general hypersonic vehicle. The effect of gas blowing due to thermal ablation on the thermal dynamics has been studied by theoretical derivation of new ODE.
In terms of effect of gas blowing, increment of mass flux of gas blowing will deteriorate the heat environment of stagnation point flow, because the normal fluid convective effect on the heat is augmented by the wall normal mass flux. However, the current conclusion is based on the assumption: the gas injection temperature is by default equal to the wall temperature, and when it comes to the application, practical caution is needed. Similarly, the suction will alleviate the heat flux, but in practice, when such extreme high temperature gas is sucked into the vehicle head, the thermal ablation resist material reacts, and the material mechanical properties are deteriorated. Therefore, the current research results serve as a qualitative direction for basic understanding of thermal dynamics of hypersonic stagnation point flow.
Availability of data and materials
The datasets used or analyzed during the current study are available from the corresponding author on reasonable request.
References
Guo Y, Shi W, Zeng L, Du B (2019) Mechanism of ablative thermal protection applied to hypersonic vehicles. Science Press, Beijing (in Chinese)
AFCRL (1974) AFCRL fiscal year 1975, Air Force technical objectives document. AFCRLTR740581
Huang Z (1981) Transient shape and inner temperature distribution of ablative cone head. Acta Aerodyn Sin 1:53–65 (in Chinese)
Zhang Z, Pan M, Liu C (2003) Hypersonic aerodynamic heat and thermal protection. National Defense Industry Press, Beijing (in Chinese)
Guo Y, Gui Y, Tong F, Dai G (2013) Research on ablating mechanism of C/ZrC composite materials. Acta Aerodyn Sin 31(1):22–26 (in Chinese)
Han J, Zhang J, Du S (1996) Oxidation behaviour of 3D fine weave pierced carboncarbon composites at ultrahigh temperatures. Acta Aeronaut Astronaut Sin 17(5):577–581 (in Chinese)
Yi F (2001) Ultra high temperature properties and ablative behaviors of carbonous thermal protective composites. Dissertation, Harbin Institute of Technology ( in Chinese)
Zhang YL, Li HJ, Yao XY et al (2011) Oxidation protection of C/SiC coated carbon/carbon composites with SiMo coating at high temperature. Corros Sci 53(6):2075–2079
Reda DC (1979) Comparative transition performance of several nosetip materials as defined by ballisticsrange testing. Paper presented at the 25th international instrumentation symposium, Anaheim, CA, 7 May 1979
Kowbel W, Chellappa V, Withers JC et al (1996) Applications of netshape molded carboncarbon composites in IC engines. J Adv Mater 27(4):2–7
Lobb RK (1964) Experimental measurement of shock detachment distance on spheres fired in air at hypervelocities. In: Nelson WC (ed) The high temperature aspects of hypersonic flow. AGARDograph, vol 68. Pergamon Press Ltd., Oxford, pp 519–527
Sinclair J, Cui X (2017) A theoretical approximation of the shock standoff distance for supersonic flows around a circular cylinder. Phys Fluids 29:026102
Olivier H (2000) A theoretical model for the shock standoff distance in frozen and equilibrium flows. J Fluid Mech 413:345–353
Wu W (1983) Fluid mechanics. Peking University Press, Beijing (in Chinese)
Anderson JD Jr (1995) Computational fluid dynamics: the basics with applications. McGrawHill, Singapore
Luo K, Wang Q, Li Y, Li J, Zhao W (2021) Research progress on magnetohydrodynamic flow control under test conditions with high temperature real gas effect. Chin J Theor Appl Mech. 53(6):1515–1531 (in Chinese)
Liu P, Li Q, Huang Z et al (2019) Interpretation of wake instability at slip line in rotating detonation. Int J Comput Fluid Dyn 32(89):379–394
Loisel V, Abbas M, Masbernat O et al (2015) Inertiadriven particle migration and mixing in a wallbounded laminar suspension flow. Phys Fluids 27(12):123304
Lashgari I, Picano F, Brandt L (2015) Transition and selfsustained turbulence in dilute suspensions of finitesize particles. Theor Appl Mech Lett 5(3):121–125
Zhou T, Zhao L, Huang W et al (2020) Nonmonotonic effect of mass loading on turbulence modulations in particleladen channel flow. Phys Fluids 32(4):043304
Picano F, Breugem WP, Brandt L (2015) Turbulent channel flow of dense suspensions of neutrally buoyant spheres. J Fluid Mech 764:463–487
Renard N, Deck S (2016) A theoretical decomposition of mean skin friction generation into physical phenomena across the boundary layer. J Fluid Mech 790:339–367
Li W, Fan Y, Modesti D et al (2019) Decomposition of the mean skinfriction drag in compressible turbulent channel flows. J Fluid Mech 875:101–123
Hornung HG (1972) Nonequilibrium dissociating nitrogen flow over spheres and circular cylinders. J Fluid Mech 53:149–176
Wen CY, Hornung HG (1995) Nonequilibrium dissociating flow over spheres. J Fluid Mech 299:389–405
Vigolo D, Griffiths IM, Radl S et al (2013) An experimental and theoretical investigation of particle–wall impacts in a Tjunction. J Fluid Mech 727:236–255
Li Q, Abbas M, Morris JF et al (2020) Nearwall dynamics of a neutrally buoyant spherical particle in an axisymmetric stagnation point flow. J Fluid Mech 892:A32
Li Q, Abbas M, Morris JF (2020) Particle approach to a stagnation point at a wall: viscous damping and collision dynamics. Phys Rev Fluids 5:104301
Li Q (2019) Nearwall dynamics of neutrally buoyant particles in a wallnormal flow: from viscous damping to collision. Dissertation, Institut National Polytechnique de Toulouse, France
White FM (2006) Viscous fluid flow, 3rd edn. McGrawHill. New York
Schlichting H (1979) Boundarylayer theory, 7th edn. McGrawHill. New York
Acknowledgements
The authors would like to thank the National Key Research and Development Plan of China for providing the funding through the project No.2019YFA0405200.
Funding
This work was supported by the National Key Research and Development Plan of China through the project No.2019YFA0405200.
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Appendix
Appendix
1.1 Explanation of incompressible approximation
Figure 6 represents the dimensional analysis on a hypersonic stagnation point flow. The typical particle diameter is around d_{p }~ 10^{−5 }m, and the computational domain character length is around ~ 10d_{p }~ 10^{−4 }m ~ δ.
The detached shock wave distance from the wall δ_{h}, and its relation with δ in terms of order are: δ_{h} ≈ 120 × 10^{−4 }m, δ ≈ 2 × 10^{−4 }m, δ_{h}/δ = 60.
According to the theoretical solution of Hiemenz flow, far from the bottom wall, larger than δ, fluid parcel vertical velocity can be approximately estimated as inviscid strain flow V = − By. The value of interest domain velocity is V_{δ} at δ, and that of velocity behind the detached shock is \({V}_{\delta_h}\approx 1000\,\mathrm{m}/\mathrm{s}\) at δ_{h}.
The linear relation of the theoretical solution of Hiemenz flow can be used to estimate the order of velocity in the computational domain:
In the stagnation point regime, the temperature can be estimated: T_{δ} > 10^{4 }K, a_{δ} > 2 × 10^{3 }m/s, V_{δ} ≈ 16 m/s and the local sonic speed is around a_{δ} ≈ 2000 m/s, thus \({M}_{\delta }=\frac{V_{\delta }}{a_{\delta }}\).
According to the definition,
in this respect, the blue interest domain can be treated as incompressible. In detail, starting from complete compressible fluid dynamic equations, and introducing with prior knowledge M_{δ} ≈ 0.01, the incompressible approximation can be proved.
Firstly, some important dimensional and dimensionless parameters will be defined as follows:
∞ represents the reference physical variable, and it can be the value at infinite far field, or certain specific regime that we are interested in. For example, for wallbounded turbulence, the reference velocity is U_{∞} = U_{τ}, while for homogeneous turbulence, it is U_{∞} = U_{λ}.
Reference mass flux: \(\frac{\rho_{\infty }{U}_{\infty }}{L_{\infty }}=\left(\frac{\rho_{\infty }{U}_{\infty }}{L_{\infty}^3}\right){L}_{\infty}^2\)
Reference momentum flux: \(\frac{\rho_{\infty }{U}_{\infty}^2}{L_{\infty }}=\left(\frac{\rho_{\infty }{U}_{\infty}^2}{L_{\infty}^3}\right){L}_{\infty}^2\)
Reference energy flux: \(\frac{\rho_{\infty }{U}_{\infty}^3}{L_{\infty }}=\left(\frac{\rho_{\infty }{U}_{\infty}^3}{L_{\infty}^3}\right){L}_{\infty}^2\)
Three basic control equations:
mass conservation:
momentum conservation:
energy conservation:
dimensionless mass conservation:
dimensionless momentum conservation:
dimensionless energy conservation:
Due to the complexity of energy equation, the terms are developed one by one in details as follows:

1st term: unsteadiness of internal and pressure energy of fluid parcel
$${\displaystyle \begin{array}{c}\frac{L_{\infty }}{\rho_{\infty }{U}_{\infty}^3}\frac{\rho_{\infty}\frac{R}{\gamma 1}{T}_{\infty }}{t_{\infty }}\frac{\partial {\rho}^{\ast }{T}^{\ast }}{\partial {t}^{\ast }}=\frac{L_{\infty }}{U_{\infty }{t}_{\infty }}\frac{R{T}_{\infty }}{U_{\infty}^2\left(\gamma 1\right)}\frac{\partial {\rho}^{\ast }{T}^{\ast }}{\partial {t}^{\ast }}\\ {}= Str\cdot \frac{1}{M{a}^2\gamma \left(\gamma 1\right)}\frac{\partial {\rho}^{\ast }{T}^{\ast }}{\partial {t}^{\ast }}=\frac{\partial {\rho}^{\ast }{C_{\mathrm{v}}}^{\ast }{T}^{\ast }}{\partial {t}^{\ast }}\end{array}}$$ 
2nd term: unsteadiness of kinetic energy of fluid parcel
$$\frac{L_{\infty }}{\rho_{\infty }{U}_{\infty}^3}\frac{\rho_{\infty }{U}_{\infty}^2}{t_{\infty }}\frac{\partial {\rho}^{\ast}\frac{{\left{V}^{\ast}\right}^2}{2}}{\partial {t}^{\ast }}={Str}\cdot \frac{\partial {\rho}^{\ast}\frac{{\left{V}^{\ast}\right}^2}{2}}{\partial {t}^{\ast }}=\frac{\partial {\rho}^{\ast}\frac{{\left{V}^{\ast}\right}^2}{2}}{\partial {t}^{\ast }}$$ 
3rd term: convection of internal and pressure energy of fluid parcel
$$\frac{L_{\infty }}{\rho_{\infty }{U}_{\infty}^3}\frac{\rho_{\infty}\frac{R}{\gamma 1}{T}_{\infty }{U}_{\infty }}{L_{\infty }}{\nabla}^{\ast}\cdot \left({\rho}^{\ast }{T}^{\ast}\overrightarrow{u^{\ast }}\right)={\nabla}^{\ast}\cdot \left({\rho}^{\ast }{C_{\mathrm{v}}}^{\ast }{T}^{\ast}\overrightarrow{u^{\ast }}\right)$$ 
4th term: convection of kinematic energy of fluid parcel
$$\frac{L_{\infty }}{\rho_{\infty }{U}_{\infty}^3}\frac{\rho_{\infty }{U}_{\infty}^3}{L_{\infty }}{\nabla}^{\ast}\cdot \left({\rho}^{\ast}\overrightarrow{u^{\ast }}\frac{{\left{V}^{\ast}\right}^2}{2}\right)={\nabla}^{\ast}\cdot \left({\rho}^{\ast}\overrightarrow{u^{\ast }}\frac{{\left{V}^{\ast}\right}^2}{2}\right)$$ 
5th term: pressure gradient work \(\overrightarrow{u^{\ast }}\cdot {\nabla}^{\ast }{p}^{\ast }\) and pressure work on the compressible fluid parcel \({p}^{\ast }{\nabla}^{\ast}\cdot \overrightarrow{u^{\ast }}\)
$$\frac{L_{\infty }}{\rho_{\infty }{U}_{\infty}^3}\frac{\rho_{\infty }{U}_{\infty}^3}{L_{\infty }}{\nabla}^{\ast}\cdot \left(\overline{\overline{I}}\cdot \overrightarrow{u^{\ast }}{p}^{\ast}\right)={\nabla}^{\ast}\cdot \left(\overline{\overline{I}}\cdot \overrightarrow{u^{\ast }}{p}^{\ast}\right)$$ 
6th term: heat conduction
$${\displaystyle \begin{array}{c}\frac{L_{\infty }}{\rho_{\infty }{U}_{\infty}^3}\frac{k_{\infty }{T}_{\infty }}{L_{\infty}^2}{\nabla}^{\ast}\cdot \left({k}^{\ast }{\nabla}^{\ast }{T}^{\ast}\right)=\frac{1}{\rho_{\infty }{U}_{\infty }{L}_{\infty }}\frac{\mu }{\mu}\frac{C_{\mathrm{v}}}{C_{\mathrm{v}}}\frac{k_{\infty }{T}_{\infty }}{U_{\infty}^2}{\nabla}^{\ast}\cdot \left({k}^{\ast }{\nabla}^{\ast }{T}^{\ast}\right) \\ {}=\frac{1}{Re}\frac{1}{Pr}\frac{C_{\mathrm{v}}{T}_{\infty }}{U_{\infty}^2}{\nabla}^{\ast}\cdot \left({k}^{\ast }{\nabla}^{\ast }{T}^{\ast}\right) =\frac{1}{Re}\frac{1}{Pr}\frac{\gamma R{T}_{\infty }}{\gamma \left(\gamma 1\right){U}_{\infty}^2}{\nabla}^{\ast}\cdot \left({k}^{\ast }{\nabla}^{\ast }{T}^{\ast}\right) \\ {}=\frac{1}{Re}\frac{1}{Pr}\frac{1}{\left(\gamma 1\right)M{a}^2}{\nabla}^{\ast}\cdot \left({k}^{\ast }{\nabla}^{\ast }{T}^{\ast}\right)\end{array}}$$ 
7th term: viscous work on the fluid parcel
$$\frac{L_{\infty }}{\rho_{\infty }{U}_{\infty}^3}\frac{\mu_{\infty }{U}_{\infty}^2}{L_{\infty}^2}{\nabla}^{\ast}\cdot \left(\overrightarrow{u^{\ast }}\cdot {\mu}^{\ast }{\nabla}^{\ast}\overrightarrow{u^{\ast }}\right)=\frac{1}{Re}{\phi}^{\ast }$$
dimensionless energy conservation:
dimensionless energy conservation·γ(γ1)Ma^{2}:
Thus, it is clear that, when γ(γ − 1)Ma^{2} becomes vanishingly small, certain terms can be neglected, which are the kinetic energy of fluid parcel, the pressure gradient and pressure work on the fluid parcel, and the viscous work on the fluid parcel.
Once M_{τ} = M_{δ} ≈ 0.01, the energy equation can be simplified as:
dimensionless mass conservation:
dimensionless momentum conservation:
dimensionless energy conservation:
\(\frac{\partial \rho }{\rho }={Ma}^2\frac{\partial u}{u}=0,\partial \rho =0,\rho = cte,{\rho}^{\ast }= cte=\frac{\rho }{\rho_{\infty }}=1\), here ∞ represents the character physical variable in the near wall stagnation point regime, where M_{δ} ≈ 0.01.
dimensionless mass conservation:
dimensionless momentum conservation:
dimensionless energy conservation:
Therefore, the energy equation becomes the heat convection and conduction equation, and its influence on the dynamic equation alters the dynamics viscosity \(\frac{\mu^{\ast }}{\rho^{\ast }}\), which is equivalent to the density stratification effect in incompressible fluid. Temperatureinduced density stratification effect is beyond the scope of current study. In general, in near wall stagnation point regime with extreme high temperature, M_{δ }~ 0, the complete compressible fluid dynamic equations are retrograded into incompressible equations.
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Li, Q., Yuan, X., Chen, J. et al. Effect of gas blowing on the head of thermal ablation vehicle. Adv. Aerodyn. 4, 10 (2022). https://doi.org/10.1186/s42774021000974
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DOI: https://doi.org/10.1186/s42774021000974