Abstract
A manned submersible is an underwater vehicle that is capable of operating independently. During the design process, estimating resistance and power is key to choosing the right propeller. The shape improvement of the manned submersible has a significant impact on the submersible's energy utilization and endurance. Using computational fluid dynamics (CFD), it is possible to accurately calculate the forces acting on manned submersibles. A CFD flow analysis framework has been formulated and the process applied to circular bodies of different lengths. To validate the results of the numerical analysis, the results are compared with experimental results available in the literature. The validated CFD framework was used to conduct the flow analysis on manned submersibles of different sizes and shapes to minimize the resistance. The optimized shape resistance is further utilized for thruster selection and to estimate the descent speed, ascent speed, descent time and ascent time for a 6000 m rated vehicle.
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Change history
27 September 2022
An Erratum to this paper has been published: https://doi.org/10.1007/s40722-022-00244-z
Abbreviations
- AUV:
-
Autonomous underwater vehicle
- CAD:
-
Computer-aided design
- CFD:
-
Computational fluid dynamics
- DNV-GL:
-
Det Norske Veritas-Germanischer Lloyd
- ITTC:
-
International Towing Tank Conference
- MSW:
-
Meters of seawater
- NACA:
-
National Advisory Committee for Aeronautics
- PPT:
-
Pre-pressurizing tank
- P–V:
-
Pressure–velocity
- RANS:
-
Reynolds averaged Navier–Stokes
- RNG:
-
Renormalization group
- SPH:
-
Spherical pressure hull
- SST:
-
Shear stress transport
- VBT:
-
Variable ballast tank
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Acknowledgements
The authors gratefully acknowledge the support given by the Ministry of Earth Science, Government of India, in funding this research. The authors would also like to thank the Director of the National Institute of Ocean Technology for his continued support of research activities.
Funding
This research was funded by the Ministry of Earth Sciences, Government of India.
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Appendices
Appendix 1: AUV hull shape—Myring equation
A Myring-type body is used to model the AUV hull shapes. The front side, nose section, back side, and tail section are connected by a middle cylindrical section. The parameters used to generate the AUV hull shape are a, b, c, d, n, and θ. The typical shape of the AUV hull is shown below (Fig. 15).
The nose section is described by a modified semi-elliptical radius equation:
The tail section is described by a cubic equation:
where x is the axial distance to the nose tip, a, b and c are the length of the nose, middle and tail sections, respectively, d is the middle hull diameter, n is the index of the nose shape, θ is the tail semi-angle.
Appendix 2: Descent and ascent scheme of the manned submersible
See Fig. 16.
Appendix 3: Compressibility of spherical pressure hulls and syntactic foam
-
1.
$${\mathrm{Seawater \; compressibility }C}_{\mathrm{sw}}=\frac{\left(\frac{4}{3}\right) \uppi {R}_{0}^{3} (1-\frac{{\rho }_{\mathrm{s}}}{{\rho }_{\mathrm{D}}})}{\mathrm{h}}.$$
-
2.
$${\mathrm{Pressure \; hull \; compressibility }C}_{\mathrm{hull}} =\frac{4 \uppi }{3h}\left\{{\left({R}_{\mathrm{m}}+t/2\right)}^{3}- {\left[{R}_{\mathrm{m}}+\frac{t}{2}- (1-\nu )\frac{{\mathrm{PR}}_{\mathrm{m}}^{2}}{2\mathrm{Et}}\right]}^{3}\right\}.$$
-
3.
$$\begin{aligned} & \mathrm{The \; amount \; of \; sea}-\mathrm{water \; that \; must \; be \; discharged}\\ & \;\mathrm{ from \; VBT \; or \; submerged \; weight \; of \; drop \; weights \; that}\\ & \;\mathrm{must \; be \; released \; to \; attain \; neutral \; buoyancy }= {C}_{\mathrm{sw}}- {C}_{\mathrm{hull}},\end{aligned}$$
where \({\rho }_{\mathrm{s}}\) is the density of seawater at the surface (1025 kg/m3), \({\rho }_{\mathrm{D}}\) is the density of seawater at the operating depth (1054 kg/m3 at 6000 m), Ro is the outer radius of the sphere, Rm is the mean radius of the sphere, t is the thickness of the pressure hull, h is the submerged depth, P is the hydrostatic pressure at the submerged depth “h”, E is the elastic modulus of pressure hull material, and ν is the Poisson’s ratio.
Parameters | Unit | SPH | VBT | PPT |
---|---|---|---|---|
Mean radius of the sphere | mm | 1090 | 360 | 336 |
Thickness of the sphere | mm | 80 | 30 | 26 |
Elastic modulus | GPa | 115 | 115 | 115 |
Poisson's ratio | – | 0.3 | 0.3 | 0.3 |
Operating depth | m | 6000 | 6000 | 6000 |
Operating pressure | MPa | 60.6 | 60.6 | 60.6 |
Density at the surface | kg/m3 | 1025 | 1025 | 1025 |
Density at the operating depth | kg/m3 | 1054 | 1054 | 1054 |
Change in volume per meter depth of sea-water | m3/m | 2.4876E−05 | 8.9619E−07 | 7.2864E−07 |
Change in volume per meter depth of unstiffened sphere | m3/m | 7.3075E−06 | 2.3417E−07 | 2.0383E−07 |
Ballast change per unit depth | m3/m | 1.7568E−05 | 6.6203E−07 | 5.2481E−07 |
Ballast change at operating depth | m3 | 0.10541 | 0.00397 | 0.00315 |
Number of pressure hull, VBT, PPT | – | 1 | 2 | 3 |
Ballast change at operating depth | m3 | 0.1054 | 0.0079 | 0.0094 |
Ballast to be adjusted to attain neutral buoyancy | 0.1228 m3 or 129.43 kg | |||
Syntactic foam | ||||
Volume of syntactic foam in air/at surface of water | m3 | 15.25 | ||
Reduced volume of syntactic foam at 6000 MSW | m3 | 14.96 | ||
Change in volume | m3 | 0.290 | ||
Reduction in buoyancy | kg | 305.66 | ||
Buoyancy due to increase in density at 6000 m | kg | 136.59 | ||
Net buoyancy reduced | kg | 169.07 | ||
Total ballast to be adjusted to attain neutral buoyancy | 298.50 kg |
Appendix 4: Initial mesh height and boundary layer thickness calculation
-
1.
$${\mathrm{Re}}=\frac{\rho \mathrm{VL}}{ \upmu }$$
-
2.
$$\nu =\frac{\mu }{\rho },$$
-
3.
$${y}^{+}=\frac{\rho \cdot {U}_{\tau } \cdot \Delta {y}_{1}}{\mu },$$
-
4.
$${U}_{\tau }= \sqrt{\frac{{\tau }_{\mathrm{w}}}{\rho }},$$
-
5.
$${\tau }_{\mathrm{w}}= \frac{1 }{2}{C}_{\mathrm{f}}\rho {V}^{2},$$
-
6.
$${C}_{\mathrm{f}}=0.0079 {\mathrm{Re}}^{-0.25}(\mathrm{for \; internal \; flows}),$$
-
7.
$${C}_{\mathrm{f}}=0.058 {\mathrm{Re}}^{-0.2}(\mathrm{for \; external \; flows}),$$
-
8.
$$\delta =0.37 {x}_{\mathrm{cr}}{\mathrm{Re}}^{-0.2},$$
where Re is the Reynolds number, \(\nu\) is the kinematic viscosity = 1.003 × \({10}^{-6}\) m2/s, μ is the dynamic viscosity in N-s/m2, ρ is fluid density = 1025 kg/m3, V is the velocity of vehicle/fluid in m/s, L is the characteristic length in m, \({y}^{+}\) is the dimensionless number of boundary layer thickness, \({U}_{\tau }\) is the frictional velocity in m/s, \({\tau }_{\mathrm{w}}\) is wall shear stress in N/m2, \(\Delta {y}_{1}\) is the estimated first cell height in m, \({C}_{\mathrm{f}}\) is the skin friction coefficient, δ is the boundary layer thickness in mm, \({x}_{\mathrm{cr}}\) is the critical length of the boundary layer in mm.
Appendix 5: Estimation of viscous drag based on ITTC-1957 and power
-
1.
$${R}_{\mathrm{f}}=\frac{1}{2}{C}_{\mathrm{f}}\rho {A}_{\mathrm{w}}{V}^{2},$$
-
2.
$${C}_{\mathrm{f}}=\frac{0.075}{{({\mathrm{log}}_{10}\mathrm{Re}- 2)}^{2}},$$
where \({R}_{\mathrm{f}}\) is the viscous drag in N, \({C}_{\mathrm{f}}\) is the skin friction coefficient, ρ is the density of fluid = 1025 kg/m3, V is the velocity of vehicle/fluid in m/s, \({A}_{\mathrm{w}}\) is the wetted surface area in m2.
-
3.
$$\mathrm{Quasi \; propulsive \; coefficient }\left(\mathrm{QPC}\right)=\frac{\mathrm{useful \; power}}{\mathrm{power \; delivered \; to \; the \; propeller} \; \mathrm{thruster}},$$
-
4.
$$\mathrm{QPC}= {\eta }_{\mathrm{H}}{\eta }_{\mathrm{P}},$$
-
5.
$$\mathrm{Propulsive} \; \mathrm{Coefficent} \left(\mathrm{PC}\right)= {\eta }_{\mathrm{H}}{\eta }_{\mathrm{P}}{\eta }_{\mathrm{M}},$$
-
6.
$${\eta }_{\mathrm{P}}= {\eta }_{\mathrm{O}}{\eta }_{\mathrm{R}},$$
-
7.
$${\eta }_{\mathrm{O}}={(0.9)}^{n},$$
-
8.
$${\eta }_{\mathrm{M}}=\frac{\mathrm{Propulsive} \; \mathrm{power}}{\mathrm{Shaft} \; \mathrm{power}},$$
where \({\eta }_{\mathrm{H}}\) is the hull efficiency = 1.00 for a well-designed stern and propeller (Allmendinger 1990), \({\eta }_{\mathrm{P}}\) is the propeller efficiency, \({\eta }_{\mathrm{O}}\) is the open water propeller efficiency \(=0.73 @3 \mathrm{knots}\), \({\eta }_{\mathrm{R}}\) is the relative rotational efficiency = 0.95 to 1.00 for submersibles (Allmendinger 1990), \({\eta }_{\mathrm{M}}\) is the machiner efficiency = 0.95 to 0.99 (it depends on the shaft length and number of bearings) (Allmendinger 1990), n is the speed of the submersible in knots.
Appendix 6: Different thruster models and their details
Tecnadyne | ||||||||
---|---|---|---|---|---|---|---|---|
S. No | Models | Input power | Bollard thrust generated | Thrust generated at 3 knots speed | Effective or useful power | Weight in air | Diameter of propeller | Ratio between effective power/Input power |
kW | kgf | kgf | kW | kg | mm | --- | ||
1 | Model 260 | 0.350 | 5.40 | 3.81 | 0.06 | 0.9 | 76 | 0.16 |
2 | Model 280 | 0.350 | 6.10 | 4.72 | 0.07 | 1.0 | 115 | 0.20 |
3 | Model 300 | 0.500 | 8.20 | 5.44 | 0.08 | 1.0 | 88 | 0.16 |
4 | Model 521 | 0.500 | 10.40 | 7.14 | 0.11 | 1.8 | 121 | 0.21 |
5 | Model 540 | 0.500 | 10.00 | 6.67 | 0.10 | 2.3 | 150 | 0.20 |
6 | Model 560 | 0.975 | 17.30 | 11.79 | 0.17 | 2.3 | 121 | 0.18 |
7 | Model 580 - DD | 0.975 | 17.30 | 12.61 | 0.19 | 1.9 | 150 | 0.19 |
8 | Model 1020 | 1.10 | 25.00 | 17.24 | 0.25 | 4.8 | 153 | 0.23 |
9 | Model 1040 | 1.25 | 25.00 | 17.01 | 0.25 | 4.3 | 203 | 0.20 |
10 | Model 1060 - DD | 2.20 | 48.00 | 38.10 | 0.56 | 6.8 | 181 | 0.25 |
11 | Model 1080 - DD | 2.20 | 48.00 | 34.99 | 0.51 | * | 203 | 0.23 |
12 | Model 2020 | 6.20 | 118.00 | 81.65 | 1.20 | 12.2 | 246 | 0.19 |
13 | Model 2020-DD | 6.00 | 118.00 | 86.02 | 1.27 | 19.0 | 246 | 0.21 |
14 | Model 2040 | 5.20 | 85.00 | 60.00 | 0.88 | 10.0 | 254 | 0.17 |
15 | Model 8020 | 12.60 | 230.00 | 163.29 | 2.40 | 26.3 | 305 | 0.19 |
16 | Model 8040 | 12.10 | 172.00 | 121.11 | 1.78 | 23.5 | 339 | 0.15 |
*Data is not available in the public domain | Average | 0.20 |
Innerspace Corporation | ||||||||
---|---|---|---|---|---|---|---|---|
S. No | Models | Input power | Bollard thrust generated | Thrust generated at 3 knots speed | Effective or useful power | Weight in air | Diameter of propeller | Ratio between effective power/Input power |
kW | kgf | kgf | kW | kg | mm | --- | ||
1 | 1002H - 14150 | 6.00 | 139.00 | 121.11 | 1.78 | 27.7 | 236 | 0.30 |
2 | 1002H - 14300 | 9.50 | 190.00 | 165.11 | 2.43 | 27.7 | 236 | 0.26 |
3 | 1002H - 14550 | 12.50 | 228.00 | 197.31 | 2.90 | 27.7 | 236 | 0.23 |
4 | 1004B - 3150 | 1.50 | 24.00 | 20.64 | 0.30 | 6.4 | 109 | 0.20 |
5 | 1004B - 3300 | 2.70 | 36.00 | 30.96 | 0.46 | 6.4 | 109 | 0.17 |
6 | H106 - 9150 | 4.30 | 64.00 | 57.61 | 0.85 | 11.3 | 236 | 0.20 |
7 | H106 - 9300 | 7.48 | 93.00 | 82.55 | 1.21 | 11.3 | 236 | 0.16 |
Average | 0.22 |
Forum Energy Technologies | ||||||||
---|---|---|---|---|---|---|---|---|
S. No | Models | Input power | Bollard thrust generated | Thrust generated at 3 knots speed | Effective or useful power | Weight in air | Diameter of propeller | Ratio between effective power/Input power |
kW | kgf | kgf | kW | kg | mm | --- | ||
1 | SPE - 75 | 1.62 | 26.00 | 18.96** | 0.28 | 3.3 | 144 | 0.17 |
2 | SPE - 180 | 2.50 | 45.00 | 32.81** | 0.48 | 5.9 | 178 | 0.19 |
3 | SPE - 250 | 6.20 | 100.00 | 72.90** | 1.07 | 13.0 | 246 | 0.17 |
**Calculated based on an open water efficiency of 0.73 | Average | 0.18 |
Appendix 7: Flow analysis plots in sway and heave directions
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Pranesh, S.B., Rajput, N.S., Sathianarayanan, D. et al. CFD analysis of the hull form of a manned submersible for minimizing resistance. J. Ocean Eng. Mar. Energy 9, 125–143 (2023). https://doi.org/10.1007/s40722-022-00232-3
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DOI: https://doi.org/10.1007/s40722-022-00232-3