From circulatory and respiratory systems to chemical and plumbing networks, controlling flows is important in many natural settings and engineering applications1,2,3,4,5. Perhaps the simplest means for directing flows is through the geometry of vessels, pipes, channels, and networks of such conduits. How geometry maps to flow patterns and distribution, however, is a challenging problem that depends on flow regime, as characterized by dimensionless quantities involving length- and time-scales and fluid material properties6. The field of microfluidics focuses on low Reynolds numbers in which small volumes are conveyed at slow speeds, and recent progress stems from advances in microscale manufacturing and lab-on-a-chip applications7. The flow physics at these scales is dominated by pressures overcoming viscous impedance, and the linearity of the governing Stokes equation enables theoretical and computational approaches that greatly aid in the design of microfluidic devices8. At larger scales and faster rates, the applications are as numerous and important2,3 but the flow physics quite different. The underlying Navier–Stokes equation is nonlinear, theoretical results are fewer, simulations are challenging, and the mapping between geometry and desired fluidic objectives all the more complex6. The phenomenology of high-Reynolds-number or inertia-dominated flows is well documented: Flows are slowed in boundary layers near surfaces and tend to separate in a manner sensitive to geometry to yield vortices, wakes, jets, and turbulence6,9. Such complexities are exemplified by the breakdown of reversibility: Running a given system in reverse, say by inverting pressures, does not in general cause the fluid to move in reverse but instead triggers altogether different flow patterns6.

Here we explore how the physics of inertial flows is exploited in an intriguing device proposed by the inventor Nikola Tesla10. Tesla intended this ‘valvular conduit’—an image of which is reproduced from his 1920 patent in Fig. 1a—to allow fluid to pass easily in one direction while presenting substantially higher resistance to flows in the reverse direction. Such a fluidic diode or valve can be used as a fundamental component for directing flows. While it is unclear if Tesla ever fabricated and tested a prototype, its unique geometry of linked and looped lanes has attracted many studies into its operation and potential applications11,12,13,14,15,16,17,18,19,20,21,22,23,24,25,26,27,28,29,30,31,32,33,34,35,36,37,38,39,40,41. Previous fluid mechanical tests have focused on steady conditions of constant flow rate, confirming the resistance asymmetry or diodicity at high Reynolds numbers (Re) for geometries modified from Tesla’s original design11,12,13,14,15. While it is clear that valving action is absent at low \({\rm{Re}}\ll 1\) for which flows are reversible39 but permissible for sufficiently high \({\rm{Re}}> 1\)13,14,15,16,17,18,19,20,21, there is lacking a characterization spanning flow regimes that would reveal how diodicity varies over a wide range of Re. Consequently, it is unclear if and how diodicity relates to internal flow phenomena such as the laminar-to-turbulent transition6,9. Further, Tesla’s patent emphasizes unsteady or pulsatile flow conditions10, which arise in pumping or rectification applications11,12,13,15,17,24,33 but for which the potential for enhanced diodic performance remains to be determined.

Fig. 1: Experimental tests of Tesla’s conduit under steady pressures.
figure 1

a Schematic modified from Tesla’s patent10 showing a planform view of the `valvular conduit’. b Rendering of the conduit used in experiments. Upper and lower lids sandwich the internal geometry, which is digitized from Tesla’s design, laser-cut, and bonded. Relevant dimensions include total length L, average wetted width w, and depth d. c Schematic of the pressure chamber. Overflow mechanisms ensure fixed water levels that drive flow through the conduit, whose actual orientation is upright as shown in b. The height differential Δh is varied and volumetric flow rate Q measured for both forward and reverse directions.

In this work, we aim to experimentally test the valvular conduit across a wide range of steady and unsteady conditions. On a conduit whose planform shape is faithful to Tesla’s original design, we first carry out systematic characterizations of flow resistance or friction for fixed pressure differences. Following measurement and analysis procedures established for flows through long, slender pipes and ducts, our experiments reveal abrupt changes in fluidic properties that are reminiscent of the laminar-to-turbulent transition, albeit triggered at anomalously low \({\rm{Re}}\). We then seek to evaluate Tesla’s conjecture10 that diodic performance is strongest when flow “is supplied in pulses and, more especially, when the same is extremely sudden and of high frequency.” We propose and implement a fluidic circuit or network subject to unsteady forcing via imposed oscillatory flows, which the diodic conduits transform or rectify into one-way flows, the whole system serving as an AC-to-DC converter or pump. A quasi-steady model links these two studies by using the steady-forcing characteristics to predict the response for unsteady forcing. Our results indicate that pulsatile flows significantly enhance pumping performance, thus bearing out Tesla’s conjecture and suggesting optimal operating conditions for rectifying conduits more generally.


Experimental tests under steady forcing

We first characterize experimentally the fluidic resistance or flow-induced pressure losses for Tesla’s diode under conditions of fixed pressure differences, this quantity varied systematically to explore flow rates in both directions. We realize a conduit whose planform or overhead-view geometry is faithful to Tesla’s original design10, and we pursue Reynolds numbers ranging over orders of magnitude, the latter being important for our later comparison of steady versus unsteady (oscillatory) forcing. We digitize the planform of Fig. 1a and manufacture a macroscale version of the conduit via laser-cutting and bonding clear acrylic plastic, a 3D rendering of which is shown in Fig. 1b. We select a scale that, together with the use of water and water-glyercol mixtures as the working fluids, allow for characterization of the channel across low to high Re. The overall length is L = 30 cm, average wetted width w = 0.9 cm and depth d = 1.9 cm.

To impose and controllably vary the pressure difference across the channel, we design and construct the apparatus whose sectional view is shown in Fig. 1c. Two chambers of a tank are connected only via the conduit, and the liquid level in each can be set and stably maintained via overspill mechanisms. The level difference Δh is set by two adjustable internal drains whose heights can be independently varied. The hydrostatic pressure difference across the channel is Δp = ρgΔh, where ρ is the density of the fluid and g = 980cm/s2 is gravitational acceleration6. Liquid flows from the high side to the low side through the channel at a volumetric flow rate Q and out to the reservoir at the same rate. A pump takes fluid from the reservoir, slightly overflowing the high side and thus maintaining its level. The system is closed and runs indefinitely. In this way, a pressure difference may be imposed and recorded by measuring the column heights with rulers, and the volumetric flow rate Q is measured by intercepting the lower drain with a beaker of known volume and reading the fill-up time with a stopwatch. The flow direction is changed by simply changing which chamber has higher level.

The measured flow rate Q versus Δh for pure water is shown in Fig. 2a. As expected, increasing the height difference yields higher flow rates for both the forward and reverse directions, as defined in Fig. 1b. The flow rate Q increases monotonically but nonlinearly with Δh. Importantly, for the same Δh, Q is greater for the forward direction than reverse across all values of Δh. This anisotropy is more clearly seen in Fig. 2b, where the resistance R = Δp/Q is plotted versus Q for the forward and reverse directions. Across all Q, the resistance in reverse is greater, and this disparity increases with Q.

Fig. 2: Experimental characterization of Tesla’s conduit under steady pressures.
figure 2

a Flow rate Q across varying pressure heads Δh and pressure differences Δp = ρgΔh for the case of pure water as the working fluid. The forward (red) and reverse (blue) directions exhibit different Q for the same Δp. Here and elsewhere, error bars are suppressed when smaller than the symbol size (see text). b Hydrodynamic resistance R = Δp/Q versus Q for the forward and reverse directions. c Dimensionless forms of pressure difference (Hagen number Hg) versus flow rate (Reynolds number Re). The plot combines data on pure water and water-glycerol solutions to cover a wide range of Re. d Friction factors fD = (Δp/L)/(ρU2/2D), a dimensionless form of pressure drop appropriate for turbulent flow. Also shown are curves representing previous measurements for smooth and rough pipes. e Diodicity Di or ratio of reverse to forward resistances versus Re. The band represents propagated standard errors determined from repeated measurements.

The errors for the data of Fig. 2a and b, as determined by multiple measurements at each condition, are smaller than the symbols and have been suppressed in these plots. Errors in Δh are about a millimeter due to the height of the meniscus that obscures the reading of water level. Errors in Q are set by the reaction time in triggering a stopwatch after collecting a specified volume. Large volumes and long collection times ( > 60 s) ensure relative errors under 1%.

Pressure drop, friction and diodicity across flow regimes

Experiments carried out with pure water yield high Reynolds numbers \({\rm{Re}}=\rho UD/\mu \sim 1{0}^{3}\), where μ is the fluid viscosity, U = Q/wd is the section-averaged flow speed through the channel, and D = 4Vw/Sw = 0.8 cm is its hydraulic diameter calculated from the total wetted volume Vw and the wetted surface area Sw. (The latter generalizes the conventional form D = 4Aw/Pw for a conduit whose cross-section shape is uniform and of wetted area Aw and perimeter length Pw42.) To explore lower Reynolds numbers, we conduct further experiments with water-glycerol solutions of varying viscosity, and all results are combined in Fig. 2c. To account for the different fluid properties, we plot non-dimensional pressure or Hagen number \({\rm{Hg}}=({{\Delta }}p/L)({D}^{3}\rho /{\mu }^{2})\) versus non-dimensional flow rate or Reynolds number6,43. As expected, the disparity between the forward and reverse directions is significant only at sufficiently high Re. Also shown for comparison are reference lines indicating linear and quadratic scalings of pressure with flow rate. For low Re, it is seen that \({\rm{Hg}} \sim {\rm{Re}}\), which is expected for well-developed and laminar flow6. For higher Re, the data follow a stronger dependence of approximately \({\rm{Hg}} \sim {{\rm{Re}}}^{2}\), which is characteristic of turbulent flow6. Interestingly, the disparity in resistance occurs together with the nonlinearity of the Hg-Re scaling.

A conventional nondimensionalization of resistance used in studies of pipe and channel flow is the Darcy friction factor fD = (Δp/L)/(ρU2/2D), which normalizes pressure drop based on inertial scales42,44. In Fig. 2d we plot our measurements of \({f}_{{\rm{D}}}({\rm{Re}})\) for forward and reverse flow through Tesla’s conduit. For comparison, we include on this so-called Moody diagram previous results on circular pipes45. The two curves shown correspond to smooth pipes and one of high roughness in which wall variations measure 10% of the mean diameter. The form \({f}_{{\rm{D}}}=64/{\rm{Re}}\) corresponds to the Hagen–Poiseuille law and applies well to both smooth and rough-walled pipes in the laminar flow regime of \({\rm{Re}}\,<\,2000\)46. Following a transitional region, well-developed turbulence tends to be triggered at higher \({\rm{Re}}\,> \, 4000\), for which fD is more constant with Re and increases with roughness. By comparison, Tesla’s conduit transitions away from the laminar-flow scaling at significantly lower \({\rm{Re}}\approx 100\). Further, the order-one friction values at higher Re are substantially higher than those for turbulent flow through smooth and rough pipes, which reflects the high impedance presented by the complex geometry.

In interpreting these results, it is important to note that the association between the scaling of \({\rm{Hg}}({\rm{Re}})\) or \({f}_{{\rm{D}}}({\rm{Re}})\) with flow state (laminar or turbulent) holds only for sufficiently long, slender conduits. For short pipes and channels, entrance effects due to the developing flow can lead to turbulent-like (\({\rm{Hg}} \sim {{\rm{Re}}}^{2}\) and \({f}_{{\rm{D}}} \sim {{\rm{Re}}}^{0}\)) rather than laminar-like (\({\rm{Hg}} \sim {\rm{Re}}\) and \({f}_{{\rm{D}}} \sim {{\rm{Re}}}^{-1}\)) scaling even for laminar flow6,42. To ensure entrance effects are negligible for turbulent flows, the length-to-diameter ratio is typically recommended to exceed about 4047, which is nearly satisfied by the value L/D = 38 for Tesla’s conduit. For laminar flow, the aspect ratio should exceed the (dimensionless) entrance length of approximately \({\rm{Re}}/30\)6, which is satisfied for \({\rm{Re}}\lesssim 1000\) for the valvular conduit. These estimates suggest that the results reported here are representative of sufficiently slender geometries for which the pressure drop scaling can be linked to flow state, and the inclusion of our measurements on the standard Moody diagram of Fig. 2d is warranted.

The performance of the channel as an asymmetric resistor can be quantified by its diodicity or ratio of reverse to forward resistance values48. Equivalently, we define this ratio using dimensionless forms of pressure drops at the same Re: \({\rm{Di}}({\rm{Re}})={{\rm{Hg}}}_{{\rm{R}}}({\rm{Re}})/{{\rm{Hg}}}_{{\rm{F}}}({\rm{Re}})={f}_{{\rm{D,R}}}({\rm{Re}})/{f}_{{\rm{D,F}}}({\rm{Re}})\), where the subscripts indicate the reverse (R) and forward (F) directions. In Fig. 2e the curve indicates how Di varies with Re, with the band representing propagated errors based on repeated measurements. For low Re, Di is close to unity and remains so up until \({\rm{Re}}\approx 100\). Over a narrow transitional range \({\rm{Re}}=100\!-\!300\), the diodic function of the channel abruptly ‘turns on’ or is activated, and for \({\rm{Re}}=300\!-\!1500\) we find Di ≈ 2. Future work should investigate the behavior for \({\rm{Re}}\,> \,2000\).

Interestingly, the turn-on of diodicity apparent in Fig. 2e comes along with the nonlinear scaling of pressure drop with flow rate (Fig. 2c) and the departure from the laminar-flow friction law (Fig. 2d). These results suggest that diodic function is closely linked to a transition to turbulent flow that occurs significantly earlier (at lower Re) than that observed for smooth and rough pipes.

Flow visualization and early turbulence

Towards understanding the mechanisms behind these observations, we next visualize the internal flows in the conduit. We focus first on a transitional value of \({\rm{Re}}=200\), for which we inject neutrally buoyant dye upstream and record photographs and video using a camera positioned to view the planform. The conduit is clear and backlit, and the resulting images reveal flow streaklines6. Two adjacent streaklines near the middle of the channel are color-coded using blue and green dyes. Figure 3a shows the case of flow in the forward direction. The streaklines remain in the central corridor along the entire length of the channel and are deflected only slightly as they pass the periodic structures. Details of the gently meandering path can be seen in the zoomed-in image of Fig. 3c. In contrast, the reverse direction involves amplified lateral deflections of the streams that eventually result in strong mixing, as shown in Fig. 3b. The incoming filaments ricochet off the internal structures, with the redirections being only slight in passing the first ‘islands’ or baffles but quickly growing downstream after repeated interactions. The flows are eventually rerouted into the recesses, and the fluid is well mixed by the end of the channel. Some of the steps that destabilize the initially-laminar flow can be seen in the zoomed-in view of Fig. 3d.

Fig. 3: Streakline flow visualization at \({\rm{Re}}=200\) using dye injected upstream.
figure 3

a, c Forward direction. Two adjacent filaments remain in the central corridor of the conduit with only small lateral deflections. b, d Reverse direction. The filaments ricochet off the periodic structures, deflecting increasingly sharply before being rerouted around the `islands’ and mixing.

We next aim to link the transition in resistance and turn on of diodicity to changes in flow state for different Reynolds numbers. In Fig. 4 we compare the reverse flows visualized at \({\rm{Re}}=50\), 200 and 400, corresponding to conditions just before, during and just after the turn-on, respectively. For \({\rm{Re}}=50\), dye filaments remain on their respective sides of the conduit, dispersed by interactions with the islands but not intermixing. The flows are observed to be laminar and steady throughout the entire channel. For \({\rm{Re}}=400\), unsteadiness of the streaklines is apparent beyond the first units, after which the filaments rapidly combine over a few units to yield well-mixed flows over most of the length. Comparatively, the transitional state of \({\rm{Re}}=200\) displays a hybrid of these features: The filaments are steady and laminar over the first 3 or 4 units, become unsteady and cross sides, and then reach near complete mixing by the end.

Fig. 4: Transition in reverse flow state with increasing Reynolds number.
figure 4

a Streakline visualization at \({\rm{Re}}=50\). Blue and green dyed filaments disperse but do not intermix, and the flow is steady throughout the conduit. a At a transitional value of \({\rm{Re}}=200\), the filaments are laminar and steady for the first few units, unsteady and intermix in the middle, and are nearly completely mixed by the end of the conduit. c At \({\rm{Re}}=400\), unsteady and well-mixed flows appear throughout most of the channel.

These results confirm the high-Re irreversibility reported in previous studies, which have emphasized the circuitous route taken by reverse flows21,22,25. Our visualizations reveal the nature of the reverse flow instability and also the extent of mixing, which we associate with increased dissipation and resistance. Unsteady flows and increased resistance are hallmarks of turbulent flow, which is triggered for Re in the thousands for pipe and channel flow6,49. Our visualizations of flow destabilization in Tesla’s conduit at considerably lower \({\rm{Re}}=200\) offer further evidence for an early transition to turbulence triggered by the complex geometry.

In interpreting this early turbulence phenomenon, a concern may be that the Reynolds number defined here based on the mean speed inadequately captures the local flow conditions at various positions in the conduit. However, close inspection of the reverse flows in the Supplementary Video indicates that speeds at different sites along the central and diverted lanes are comparable to one another, with differences measuring less than 50%. Hence, the onset of turbulence at unusually low \({\rm{Re}}\approx 200\) cannot be attributed to local surges in flow speed significant enough to reach the conventional transitional value of \({\rm{Re}}\approx 2000\) for pipe flow. An alternative interpretation for the early onset of turbulence is given in our concluding discussions.

Unsteady forcing of a fluidic AC-to-DC converter

Having characterized Tesla’s conduit for steady pressure differences, we next consider unsteady forcing in which the internal flows are driven to oscillate. To assess Tesla’s conjecture of enhanced performance for pulsatile flows10, we draw on the analogy between electric and fluidic circuits and consider a full-wave rectifier that uses four diodes arranged in a bridge configuration in order to convert an imposed alternating current (AC) in one branch into directed current (DC) in a second branch50. The electric circuit is shown schematically in Fig. 5a. An AC current source is on the left, and the directionality of each ideal diode is indicated by the arrowhead. These elements are linked by conducting wires, and current directions are shown in red and blue for the two half-cycles of the AC source. When current is driven upwards through the source, only the two diodes under favorable bias conduct, and the current follows the red path. In the next half-cycle, the other pair of diodes conducts, and the current follows the blue path. Thus, while the input branch is purely AC or oscillatory, the output branch on the bottom exhibits a DC component or non-zero mean.

Fig. 5: Electronic AC-to-DC converter and an analogous fluidic pump.
figure 5

a Electric circuit with four ideal diodes that converts alternating current source (AC, left branch) to direct current (DC, lower branch). Red and blue lines highlight the path and direction of current at different phases in the AC cycle. b Sectional view of an analogous fluidic circuit with four Tesla diodes and a pulsatile flow source. The experimental device employs a reciprocating piston of amplitude A and frequency f as an AC source in one branch, and the DC flow is measured in a second branch. c Section-averaged flow imposed in the AC branch (top) and measured in the DC branch (bottom) for A = 1.9 cm and f = 4 Hz. The mean flow rate UDC > 0 indicates successful AC-DC conversion or pumping. Inset: sample flow velocity profiles measured by PIV.

Figure 5b shows the schematic of the fluidic analog that we design, construct and test. Laser-cut and bonded Tesla conduits serve as diodes, a reciprocating piston replaces the AC current source, and these elements are connected in bridge configuration through piping. The circuit is filled with water, and the position of the piston is driven sinusoidally in time with amplitude A and frequency f controllably varied via a high-torque stepper motor (Longs Motor) and Arduino controller. Because the piston completely seals the surrounding cylinder, the flow in the AC branch is purely oscillatory. The diodic behavior of the conduits then manifest as one-way or directed current (DC) in the lower branch. To assess this, we use Particle Image Velocimetry (PIV) to measure the flow velocity field along a segment of the transparent DC branch pipe. The 5-cm-long interrogation region is encased in a rectangular water jacket to minimize optical distortion51. Following procedures from earlier studies52,53,54, we seed the water with particles (hollow glass microspheres of approximate diameter 50 μm, 3M) whose near neutral buoyancy is ensured by selection from a fractionation column in water. A laser sheet (1.25W CW green, CNI) of thickness 0.5 mm is shone across the mid-plane along the PIV section, and the resulting particle motions are recorded via high-speed camera (12 MP, 150 fps, Teledyne Dalsa Falcon2). Post-processing via an established PIV algorithm55, these data provide the flow velocity profile across the pipe, resolved in time within each oscillation cycle and over a total duration of at least 10 cycles.

Representative data are shown in Fig. 5c for one set of A and f. The upper panel presents the flow speed averaged across the cross-section in the AC branch, where the sinusoidal oscillations \(2\pi Af\sin (2\pi ft)\) conform to the piston motions. The lower panel represents the measured section-averaged flow speed in the DC branch, and the inset shows the flow velocity profile furnished by PIV at two points in the cycle. At each time t, the two halves of the profile (bisectioned by the tube’s axis) are averaged and axisymmetry is assumed to arrive at the section-averaged speed. Strikingly, the flow has a dominant DC component UDC, and the flow profiles remain unidirectional throughout the oscillation cycle. Thus the circuit achieves the goal of AC-to-DC conversion or pumping. The output flow also shows a weak AC component of amplitude ΔU. These ripple oscillations occur at twice the driving frequency f, as both half-strokes of the AC input contribute to the DC output.

To assess the pumping performance of the circuit more generally, we systematically vary the AC input parameters A and f and measure the section-averaged DC flow speed UDC, which is equivalent to volumetric flux (volume per unit cross-sectional area and time). Figure 6a shows how UDC varies with A and f. Across all driving conditions, UDC > 0 and the system achieves AC-to-DC conversion. As expected, the output UDC increases with the inputs A and f. Less apparent in Fig. 6a is that the response is nonlinear. To clarify this, we define the effectiveness of the pump as E = UDC/4Af. This normalization is chosen such that ideal or perfect diodes yield E = 1: A volume of fluid proportional to the piston displacement 2A is injected into the DC branch in each stroke of duration 1/2f, with the two strokes in each cycle contributing equally. In Fig. 6b we plot effectiveness E versus frequency f and dimensionless amplitude A/D. The fact that E < 1 for all conditions reflects the non-ideal nature or ‘leakiness’ of the diode. Interestingly, it is seen that E itself increases with both A and f, quantifying the nonlinear response of UDC. That is, doubling either A or f leads to disproportionately higher UDC. For the conditions studied here, we achieve E ≈ 0.5, and the trends suggest yet higher efficacy would be attained for stronger driving.

Fig. 6: Performance of the fluidic AC-to-DC converter or pump.
figure 6

a Average DC flow speed UDC versus driving amplitude A and at different frequencies f. Representative error bars (black) show standard errors of the mean. b Effectiveness of rectification versus amplitude normalized by the hydraulic diameter D. c Experimentally measured effectiveness. The axes correspond to normalized amplitude and non-dimensional frequency or Womersley number Wo2f. White markers indicate data points, and the colormap is interpolated and extrapolated elsewhere. The dashed hyperbolic curves are contours of the driving or oscillatory Reynolds number \({\rm{Re}}\propto {{\rm{Wo}}}^{2}\cdot A/D\).

A fully dimensionless characterization is displayed in Fig. 6c, where E is mapped across varying A/D and the (squared) Womersley number Wo2 = πρfD2/2μ, which assesses the unsteadiness of pulsatile flow by comparing frequency to the timescale for diffusion of momentum56. The high values of Wo2 = 50 to 500 explored here suggest plug-like flow profiles in the AC sections. The variations in the map again highlight the nonlinearity of the pump, which is most effective in the red region of high Wo2f. For reference, we include contours (dashed hyperbolic curves) of constant driving or oscillatory Reynolds number, defined as \({\rm{Re}}=\rho AfD/\mu =2/\pi \cdot {{\rm{Wo}}}^{2}\cdot A/D\). Significant pumping of E > 0.1 occurs for \({\rm{Re}}\) in the hundreds, when diodicity is observed to turn on for steady flow (Fig. 2e).

A quasi-steady model of the AC-to-DC converter

The rectifying circuit provides a clean context for assessing Tesla’s conjecture of enhanced performance of the diode for pulsatile flows. Our strategy involves formulating a model that predicts the pump rate of the system based on its steady-flow characteristics, and then comparing this prediction to the actual performance measured experimentally. The quasi-steady model views the AC–DC rectifier as a network of nonlinear resistors whose resistance values vary with flow rate and direction as measured and characterized in Fig. 2. The network can then be analyzed by standard methods for electronic circuits, i.e. by solving for unknown currents through all segments via equations for current/flow conservation at each node or junction and voltage/pressure drops around closed loops50.

Complete model equations and calculations are available in the Methods section, and here we highlight the key assumptions and steps. We seek the instantaneous current or volumetric flux Q(t) through each segment of the circuit. The resistance-current curves for each diode are given by fitting splines to the data of Fig. 2, where the sign of Q in each diode dictates whether the forward or reverse resistance applies. The DC branch presents a constant resistance RDC estimated via the Hagen–Poiseuille law for pipe flow6. The AC source imposes \({Q}_{{\rm{AC}}}=2\pi fAwd\sin (2\pi ft)\) across the bridge. For any resistive element, pressure drops and currents are related via Ohm’s law Δp = QR, with all quantities being time dependent. Kirchhoff’s laws demand that pressure drops sum to zero around each closed loops and currents sum to zero at every node. Symmetry arguments reduce the unknowns to the DC branch current QDC and two diode currents, for example those through the rightmost pair in Fig. 5b. One loop law and two node laws give three nonlinear algebraic equations for these unknown currents at each time t. Discretizing in time and applying MATLAB’s fsolve function yields numerical solutions for the instantaneous currents. The effectiveness predicted by the model is then \({E}_{{\rm{M}}}=<{Q}_{{\rm{DC}}}(t)> /<| {Q}_{{\rm{AC}}}(t)| > \), where the brackets indicate averages over a period.

Comparing steady and unsteady performance

The model furnishes predictions across varying inputs A and f, and these results serve as a quasi-steady baseline against which the measured performance under unsteady conditions can be compared. In the colormap of Fig. 7a, we plot the so-called boost or relative enhancement of the experimentally measured effectiveness over the model prediction: B = E/EM. The axes are again dimensionless forms of amplitude A/D and frequency Wo2. Warmer colors with B > 1 indicate conditions for which the actual circuit outperforms quasi-steady expectations. It can be seen that the device performs better than expected for all but the lowest values of A and f, providing validation of Tesla’s conjecture of enhanced diodic performance for pulsatile flows10. Further, unsteady effects seem to be optimally exploited for low amplitude and high frequency oscillations (red region), for which we observe boosts as high as B ≈ 2.5 and thus more than a doubling in pump rate over the quasi-steady baseline. Extrapolation of these data suggests yet greater enhancement for higher frequencies.

Fig. 7: Comparison of pump rate and pulsatility in experiments and a quasi-steady model.
figure 7

a Boost factor B quantifying enhancement of pumping effectiveness in experiments relative to the model prediction. Markers indicate locations of measurements, and the colormap is interpolated and extrapolated elsewhere. b Pulsatility of the experimentally-measured rectified flow, defined as the ratio of ripple amplitude to mean flow rate in the DC branch.

Another point of comparison between the model and experiment involves the oscillations or ripples apparent in the DC branch signal, an example from experiments shown in the lower panel of Fig. 5c. We define the pulsatility P = ΔU/UDC as the ratio of the ripple amplitude to the mean pump rate, which can be assessed from the experimental measurements and from the model output. In both cases, we fit the form \({U}_{{\rm{DC}}}+{{\Delta }}U\sin (2\pi ft+\phi )\) to the section-averaged flow speed to extract the necessary quantities. Smooth output flows and thus low P are generally preferable in pumping applications. In the quasi-steady model, we observe uniformly high PM ≈ 1 for all driving conditions (data not shown). This behavior is similar to an electronic diode-bridge rectifier, whose output current reaches a minimum of zero whenever the source current crosses zero, leading to oscillations as large as the mean. As shown in the map of Fig. 7b, the actual fluidic circuit proves to be much smoother with P ≈ 0.1 across the conditions explored here. Thus the fluctuations are an order of magnitude less than that predicted by the quasi-steady model. Surprisingly, the DC output in experiments is less pulsatile for stronger AC driving, and high A in particular yields low P. This effect and the general mitigation of pulsatility as compared to quasi-steady expectations may be due to flow inertia, which tends to filter out fluctuations but which is absent from the quasi-steady framework. This hypothesis might be explored in models or simulations that include inertia.


This work presents systematic experimental characterizations of Nikola Tesla’s fluidic valve or diode across a wide range of both steady and unsteady flow conditions. The case of steady pressure/flow-rate considered in previous studies on Tesla-like channels provides a point of comparison to our results13,16,17,18,21,22,23,24,31,34,35,13. No earlier work reports on the abrupt rise in diodicity, which likely reflects the singular values or narrow ranges in \({\rm{Re}}\) explored. Further, previous experiments and simulations have reported weaker diodicity for corresponding conditions11,12,13,15,18, e.g. Di = 1.0 − 1.3 at \({\rm{Re}}=500\) for which we measure Di = 2.0. This may be due to differences in geometry, both in that the diodes are variations on Tesla’s original design and the measurement systems may not isolate the channel, thereby introducing additional pressure drops that dilute diodicity. The more encouraging results reported here are in better alignment with values Di = 2 − 4 reported14,15,17,18,20 for various Tesla-inspired geometries and at select \({\rm{Re}}\) values between 103 and 106. This regime of \({\rm{Re}}\,> \, 2000\) would benefit from a systematic characterization of diodicity as presented here for \({\rm{Re}}\,<\,2000\). Future research might also include shape optimization towards improving performance12,13,14,15,17,18,18,19,24,34, though it seems that the diodicity value of 200 stated in Tesla’s patent10 seems well beyond reach, at least for the fluid dynamical regime studied here. Tesla may have envisioned air or other gases as the working fluid, in which case compressibility may affect performance but only at the extreme flow rates needed to achieve Mach numbers of order one.

Previous experimental and computational visualizations for Tesla-inspired channels have confirmed the reversible and irreversible flows expected at low39 and high Re21,22,25, respectively. Studies of the latter validate Tesla’s picture of the reverse flows taking a circuitous path around the periodic internal structures10. Our work bridges flow regimes by focusing on the transitional \({\rm{Re}}=200\) and thereby revealing the destabilization mechanism for the reverse mode: Repeated interactions of the central flow with these structures lead to amplified lateral deflections that reroute streamlines and eventually induce complete mixing. These flow observations together with our resistance characterizations point to the conclusion that Tesla’s conduit induces a turbulent-like flow state at unusually low Re. Namely, the signatures of pipe flow turbulence that first appear in smooth and rough-walled pipes at \({\rm{Re}}\approx 2000\) are triggered in Tesla’s conduit at \({\rm{Re}}\approx 200\). Signs of such early turbulence, though with less pronounced changes in the transitional Re, have been observed for textured channels and corrugated pipes46,57,58. Our measurements establish a link between early turbulence and the turn-on of diodicity, a connection that should be tested in other asymmetric conduits59,60,61,62 and might be exploited in the design of fluidic rectifiers and their applications.

Towards interpreting the apparently early onset of turbulence, we first note that the system might be viewed as having qualities of both internal and external flows. This duality stems from the fact that the conduit width and its internal structures that ‘invade’ the flow are of the same scale. Said another way, the relative roughness is of order one. For external or open flow around a bluff body, intrinsic unsteadiness in the form of vortex shedding first appears at \({\rm{Re}}\approx 100\) and is accompanied by a transition from linear to quadratic scaling of drag with flow speed6,42. Analogous events would seem to occur for the local flows around the intruding structures in Tesla’s device. Hence, the signatures of turbulence observed here may be viewed as arriving early from the standpoint of conventional internal or pipe flow but as expected for external flows.

The case of unsteady or pulsatile flow, while less studied, has been considered in previous experiments11,12,13,15,33,63 and simulations17,24 that demonstrate pumping using Tesla-inspired geometries. Our quantifications of performance offer concrete guidelines that might be generally useful for such applications: (1) Reynolds numbers should be kept in the hundreds or higher to fully activate diodic response; (2) The output pump rate can be expected to increase stronger than linearly in both the amplitude and frequency of driving pulsations; (3) Stronger AC driving and high frequencies in particular can be used to optimally exploit unsteady effects and boost pump rate; and (4) Stronger driving and high amplitudes in particular optimally exploit inertial effects for low-pulsatility output flow. The second and third properties seem to bear out Tesla’s vision that diodicity is amplified for highly unsteady conditions10. Future work might assess these findings in simulations, test whether they are general features of asymmetric conduits59,60,61,62, and optimize shape for pulsatile flow conditions.

While this work emphasizes fluid mechanical characterization rather than practicalities, many applications of Tesla-like valves have been proposed, investigated, and implemented11,12,13,15,16,17,18,20,24,26,27,28,29,30,32,33,34,35,41,63. Here we touch on two engineering contexts and their physiological analogs. First, the pumping applications discussed above speak to Tesla’s original motivation of a no-moving-parts valve that is resistant to wear or failure. Our findings indicate that its valving action is best at high frequencies. This motivates the specific application in which the vibrations intrinsic to all forms of machinery are harnessed to pump coolants, fuels, lubricants, or other fluids needed for proper operation59. Here the leakiness or lossiness of the diode is no major detriment as the kinetic energy of the vibrational source is ample, ever-present and otherwise unused. This use is reminiscent of the return flow of blood up leg veins and of transport in the lymphatic system, both of which are driven by ambient muscle contractions that squeeze vessels and activate serial valvular structures1,64,65. Secondly, the device may be exploited for its direction-dependent flow states and especially the turbulent mixing available at unusually low Re. A fluid drawn in reversely can be readily mixed with other fluids, heated/cooled or otherwise conditioned or treated, after which it may be expelled for further processing or use. Biological analogs exist in respiratory systems, where inhaled air is heated and humidified by so-called turbinates in the nasal cavity1,66 and where structures resembling Tesla valves have recently been discovered in the turtle lung67.

In summary, our findings support two main conclusions: (1) For steady forcing, an abrupt turn-on of diodic behavior is linked to the transition to turbulent flow, which is triggered at anomalously low Re; and (2) For unsteady forcing, the diodic performance is enhanced several-fold and especially so for high-frequency pulsatile flow. In more detail, our steady pressure/flow-rate investigation reveals a transitional Reynolds number \({\rm{Re}}\approx 200\) marking the appearance of significant differences in the reverse versus forward resistances. This turn-on of diodicity is accompanied by the onset of nonlinear scaling of pressure drop with flow rate, departure from the laminar-flow friction law, and flow instabilities that induce unsteadiness and strong mixing. These steady-forcing results serve as a baseline for understanding unsteady performance, which we assess using an AC-to-DC converter that transforms forced oscillations into one-way flows. The system acts as a pump or rectifier whose output rate varies nonlinearly with input driving parameters. While significant pumping is observed only when the diodic response is activated, a quasi-steady model informed by steady-flow characteristics tends to underestimate the observed pump rates. The model also does not account for the smooth operation of the pump, as quantified by the low pulsatility of its output DC flow, nor the counter-intuitive decrease in DC pulsatility for stronger AC driving.


Circuit model for the AC-to-DC converter

We model the AC-to-DC converter as the equivalent electronic circuit shown in Fig. 8a. Each Tesla conduit is represented by a combination of two ideal diodes and two resistances RF(Q) and RR(Q) ≥ RF(Q) whose values depend nonlinearly on flow rate. For terminals I and O connected to an oscillating source QAC(t), we seek the time-averaged DC current \(<{Q}_{{\rm{DC}}}(t)> \) going from node 2 to node 4 through a resistor of constant resistance RDC. We seek the solution by applying Kirchhoff’s laws for nodes and loops: Total incoming flows and total outgoing flows are equal at a node, and the sum of all pressure drops around a closed loop is equal to zero. Ohm’s law Δp = QR describes the relationship of pressure Δp across and flow rate Q through any given resistor of resistance R.

Fig. 8: Circuit model with nonlinear resistances.
figure 8

a Equivalent electronic circuit of the fluidic AC-to-DC converter, where the Tesla conduit is modeled as a `leaky diode’ with asymmetric resistance values. b Resistances vs. flow rate for forward (red) and reverse (blue) flow through Tesla’s conduit, as inferred from the data shown in Fig. 2. The DC branch resistance value is estimated via the Hagen-Poiseuille law.

In general, given a time-dependent input flow rate QAC, the resulting flow rates Q12, Q23, Q43, Q14, and QDC also depend on time and thus so do RF and RR. To simplify the notation, the time dependence of these quantities is suppressed in what follows. The number of unknown currents can be reduced by invoking symmetry. Consider when the source polarity is as indicated in Fig. 8a, that is, positive rate QAC enters at I and exits at O. In the direction indicated by arrows, the sign of QDC is positive, while the signs of Q12, Q43, Q23, and Q14 are not known a priori. Symmetry demands that Q12 = Q43 and Q23 = Q14. In the labelled directions, Q12 and Q14 must be like-signed (both positive or both negative) so that the net pressure drop around the closed loop 1-2-4-1 is zero. Further, in order for the flow rates to conserve at node 1, the sign in question must be positive. It then follows that all flow rates are positive in the labelled directions. There are then two independent equations corresponding to Kirchhoff’s node law and one corresponding to the loop law:

$$\begin{array}{lll}{Q}_{12}-{Q}_{23}-{Q}_{{\rm{DC}}}&=&0\\ {Q}_{12}+{Q}_{23}-{Q}_{{\rm{AC}}}&=&0\\ {Q}_{12}{R}_{{\rm{F}}}({Q}_{12})-{Q}_{23}{R}_{{\rm{R}}}({Q}_{23})+{Q}_{{\rm{DC}}}{R}_{{\rm{DC}}}&=&0.\end{array}$$

Symmetry ensures that the same equations hold when the polarity of the source is reversed, i.e.QAC − QAC. So the system of equations is valid in general and describes the circuit with an oscillating source at all instances in time. The algebraic system of 3 equations is nonlinear in the 3 unknowns Q12, Q23, and QDC, all of which depend on time, and involves the harmonic forcing QAC(t) = Q0sin(2πft). Hence the system is periodic in time, so it is sufficient to solve and average over a single period T = 1/f. This together with the symmetry of the system under reversing QAC as discussed above leads to the conclusion that it is only necessary to solve and average over a half-period. We solve the system numerically using MATLAB by stepping time through a half-period t [0, T/2], where the exact functions for RF(Q) and RR(Q) are specified by spline fits to the experimental measurements, as shown in Fig. 8b.

Since the DC branch pipe has only a weak oscillatory component, we estimate its resistance RDC using Hagen-Poiseuille theory for developed and laminar pipe flow6. Accordingly, the resistance R = 128μL/πD4 of a pipe is constant in time and depends on the fluid (water at room temperature) viscosity μ = 8.9 × 10−3dyn  s/cm2 as well as the pipe length L and diameter D. For experimental reasons, the DC branch consists of four different segments connected in series. Segments 1, 2, and 3 are pipes with different lengths (30, 150, 30 cm) and diameters (1, 2.4, 1 cm respectively), and segment 4 is a flow conditioner consisting of a bundle of 50 parallel straws, each 0.25 cm in diameter and 20 cm in length. Following the law of adding linear resistors, the resistance of segment 4 is 1/50 the resistance of each straw. We then estimate RDC as the sum of four resistances, \({R}_{{\rm{DC}}}=(128\mu /\pi )({L}_{1}/{D}_{1}^{4}+{L}_{2}/{D}_{2}^{4}+{L}_{3}/{D}_{3}^{4}+{L}_{4}/20{D}_{4}^{4})=70\) g  cm−4 s−1. At each time step, an instantaneous value of QDC(t) is obtained using the MATLAB root-finding function fsolve. Averaging the solutions over the half-period [0, T/2] yields the rectified flow rate \(<{Q}_{{\rm{DC}}}(t)> \). The effectiveness of rectification is then

$${E}_{{\rm{M}}}=\frac{\langle{Q}_{{\rm{DC}}}(t)\rangle}{\langle| {Q}_{{\rm{AC}}}(t)| \rangle}=\frac{\langle{Q}_{{\rm{DC}}}(t)\rangle}{\frac{1}{T/2}\mathop{\int}\nolimits_{0}^{T/2}{Q}_{0}\sin (2\pi ft)\ {\rm{d}}t}=\frac{\langle{Q}_{{\rm{DC}}}(t)\rangle}{2{Q}_{0}/\pi }=\frac{{U}_{{\rm{DC}}}}{4Af},$$

which is consistent with the definition of E given in the text in the context of the experiments. Here Q0 = (2πAf)wd and \(\langle{Q}_{{\rm{DC}}}(t)\rangle=\langle{U}_{{\rm{DC}}}(t)\rangle wd={U}_{{\rm{DC}}}wd\), where wd is equal to the average cross-sectional area of the conduit.

Though not true for Tesla’s conduit, the simplified case of RF and RR being constants independent of flow rate gives some intuition for EM. The system of equations (1) are then a linear system in the 3 unknowns Q12, Q23 and QDC. The output DC flow rate can be calculated analytically as


which is valid at all instances for time-dependent flow rates QDC(t) and QAC(t). As in the full problem with rate-dependent resistance values, given the input QAC(t) = Q0sin(2πft) and averaging over a half-period t [0, T/2] yields

$$\langle{Q}_{{\rm{DC}}}(t)\rangle=\frac{1}{T/2}\mathop{\int}\nolimits_{0}^{T/2}\frac{{R}_{{\rm{R}}}-{R}_{{\rm{F}}}}{{R}_{{\rm{R}}}+{R}_{{\rm{F}}}+2{R}_{{\rm{DC}}}}{Q}_{0}\sin (2\pi ft)\ {\rm{d}}t=\frac{2{Q}_{0}}{\pi }\frac{{R}_{{\rm{R}}}-{R}_{{\rm{F}}}}{{R}_{{\rm{R}}}+{R}_{{\rm{F}}}+2{R}_{{\rm{DC}}}}.$$

Following Eq. (2), the effectiveness EM is then given by


where Di = RR/RF. Because Di ≥ 1 and all resistance values are non-negative, EM ≤ 1. Some special cases and limits:

  • For ideal diodes with RF = 0 and RR = , Di =  and EM = 1, indicating perfect rectification.

  • For symmetric resistors with RF = RR, Di = 1, and EM = 0, indicating no rectification.

  • If RDCRFRR, then EM = (Di − 1)/(Di + 1) depends on the resistance values RR and RF only through their ratio Di.