We neglected the viscous forces and the base pressure in estimating the forces acting on the sharp cone of Example 12.2. Consider a sharp cone \left(\theta_{c}=10^{\circ}\right) \mathrm{ex}- posed to the Mach 8 flow of Tunnel B at the Arnold Engineering Development Center (AEDC), as shown in Fig. 12.18. For this problem, the subscript t 1 designates the flow conditions in the nozzle reservoir, the subscript 1 designates those in the test section, the subscript e designates those at the edge of the boundary layer of the sharp cone (and which are constant along the entire length of the cone), and the subscript w designates conditions at the wall of the cone. If T_{t 1}=1350^{\circ} \mathrm{R}, p_{t 1}=850 \mathrm{psia}, T_{w}=600^{\circ} \mathrm{R}, and \alpha=0^{\circ}, develop expressions for the forebody pressure coefficient \left(C_{p, e}\right), the base pressure coefficient \left(C_{p, b}\right), and the skin friction. What is the total drag acting on the vehicle?
Let us use Figs. 8.15 \mathrm{~b} and \mathrm{c} to obtain values for the pressure coefficient and for the Mach number of the inviscid flow at the edge of the boundary layer for a 10^{\circ}-half-angle cone in a Mach 8 stream. Inherent in this use of these figures is the assumption that the boundary layer is thin and that there are no significant viscous/inviscid interactions which perturb the pressure field. Thus, M_{e}=6 and C_{p, e}=0.07. Since q_{1}=\frac{1}{2} \rho_{1} U_{1}^{2} =(\gamma / 2) p_{1} M_{1}^{2},
p_{e}=p_{1}\left(1+\frac{\gamma}{2} M_{1}^{2} C_{p, e}\right)
We can use Table 8.1 to calculate the free-stream static pressure \left(p_{1}\right) in the Mach 8 flow of the wind-tunnel test section:
p_{1}=\frac{p_{1}}{p_{t 1}} p_{t 1}=\left(102 \times 10^{-6}\right)(850)=0.867 \text { psia }
Thus,
p_{e}=0.0867[1.0+(0.7)(64)(0.07)]=0.3586 \mathrm{psia}
Since M_{e}=6, we can use Table 8.1 and the fact that the edge flow is that for an adiabatic flow of a perfect gas, so that T_{t 1}=T_{t e}. Thus,
T_{e}=\frac{T_{e}}{T_{t e}} T_{t e}=(0.12195)(1350)=164.63^{\circ} \mathrm{R}
To aid in our decision as to whether the boundary layer is laminar or turbulent, let us calculate the Reynolds number for the flow at the boundarylayer edge:
\operatorname{Re}_{l}=\frac{\rho_{e} U_{e} l}{\mu_{e}}=\left[\frac{p_{e}}{R T_{e}}\right]\left[M_{e} \sqrt{\gamma R T_{e}}\right]\left[\frac{T_{e}+198.6}{2.27 \times 10^{-8} T_{e}^{1.5}}\right] l
where, as shown in Fig. 12.18, l is the wetted distance along a conical generator. Thus,
\begin{aligned} \operatorname{Re}_{l} & =\left(0.0001828 \frac{\mathrm{lbf} \cdot \mathrm{s}^{2}}{\mathrm{ft}^{4}}\right)\left(3773.80 \frac{\mathrm{ft}}{\mathrm{s}}\right)\left(7.575 \times 10^{6} \frac{\mathrm{ft}^{2}}{\mathrm{lbf} \cdot \mathrm{s}}\right) l \\ & =5.226 \times 10^{6} l \end{aligned}
Based on the wetted length of a conical ray \left(l_{c}=17.276 ~\mathrm{in}.\right),
\operatorname{Re}_{l c}=7.523 \times 10^{6}
It should be noted that, although hypersonic boundary-layers are very stable, boundary-layer transition should occur for this flow, probably within the first one-half of the cone length. Thus, we can use the correlation presented in Fig. 12.19 to determine the base pressure:
\frac{p_{b}}{p_{e}}=0.02so that p_{b}=0.00717~ \mathrm{psi}.
Mach number for turbulent flow. [From Cassanto (1973).]
Note that since p_{b}=0.02 p_{e},
\begin{aligned} C_{p, b} & =\frac{p_{b}-p_{1}}{q_{1}}=\left(\frac{p_{b}}{p_{1}}-1\right) \frac{2}{\gamma M_{1}^{2}} \\ & =\left(\frac{p_{b}}{p_{e}} \frac{p_{e}}{p_{1}}-1\right) \frac{2}{\gamma M_{1}^{2}}=-0.0205 \end{aligned}
Recall that the assumption for Newtonian flow is C_{p, b}=0.0.
To calculate the skin friction contribution, let us use Reynolds analogy (see Chapter 4). For supersonic flow past a sharp cone, the heat-transfer rate (or, equivalently, the Stanton number) can be calculated using the relatively simple approximation obtained through the Eckert reference temperature approach [Eckert (1955)]. In this approach, the heat-transfer rates are calculated using the incompressible relations [e.g., equation (4.103)]
\mathrm{St} \equiv C_h=\frac{\dot{q}}{\rho u_e c_p\left(T_e-T_w\right)} (4.103)
with the temperature-related parameters evaluated at Eckert’s reference temperature \left(T^{*}\right). According to Eckert (1955),
T^{*}=0.5\left(T_{e}+T_{w}\right)+0.22 r\left(T_{i e}-T_{e}\right)
where r is the recovery factor. For turbulent flow, the recovery factor is \sqrt[3]{P r}, which is equal to 0.888 . Thus,
\begin{aligned}T^* & =0.5(164.63+600)+0.22(0.888)(1350-164.63) \\& =613.89^{\circ} R\end{aligned}
Thus,
\begin{aligned} \mathrm{Re}_{l}^{*} & =\left[\frac{p_{e}}{R T^{*}}\right]\left[U_{e}\right]\left[\frac{T^{*}+198.6}{2.27 \times 10^{-8} T^{* 1.5}}\right] l \\ & =\left(0.00004901 \frac{\mathrm{lbf} * \mathrm{~s}^{2}}{\mathrm{ft}^{4}}\right)\left(3773.80 \frac{\mathrm{ft}}{\mathrm{s}}\right)\left(2.353 \times 10^{6} \frac{\mathrm{ft}^{2}}{\mathrm{lbf} \cdot \mathrm{s}}\right) l \\ & =4.353 \times 10^{5} l \end{aligned}
Thus, using Reynolds’ analogy, we have
C_{f}=\frac{0.0583}{\left(\operatorname{Re}_{l}^{*}\right)^{0.2}}=\frac{0.004344}{l^{0.2}}
Thus,
\tau=C_{f}\left(\frac{\gamma}{2} p_{e} M_{e}^{2}\right)=\frac{0.03926}{l^{0.2}} \frac{\mathrm{lbf}}{\mathrm{in}^{2}}
To calculate the total drag,
D=\int p_{e} 2 \pi r d l \sin \theta_{c}+\int \tau_{w} 2 \pi r d l \cos \theta_{c}-p_{b} \pi R_{b}^{2}
Noting that p_{e} is constant along the length of the conical generator, d l \sin \theta_{c}=d r, and r=l \sin \theta_{c},
\begin{aligned} D & =p_{e} \pi R_{b}^{2}+0.03926(2 \pi)\left(\cos \theta_{c} \sin \theta_{c}\right) \int_{0}^{l_{c}} l^{0.8} d l-p_{b} \pi R_{b}^{2} \\ & =(0.3586)(9 \pi)+(0.04218) \frac{l_{c}^{1.8}}{1.8}-(0.00717)(9 \pi) \\ & =10.139+3.956-0.203=13.892 \mathrm{lbf} \end{aligned}