Sizing Neutral and Ground Busbars with High SMPS Density

Introduction and Context of Modern Non-Linear Loads

In the contemporary landscape of electrical power engineering, the transition from linear resistive and inductive loads to power electronics-based systems has redefined the design paradigms of low-voltage distribution systems. Switched-Mode Power Supplies (SMPS), which power data center servers, LED lighting systems, variable frequency drives (VFDs), and information technology equipment, impose a highly non-linear operating regime. These loads do not consume a continuous sinusoidal current, but rather discrete current pulses of high amplitude and short duration. This high-frequency switching phenomenon generates a severe harmonic spectrum, characterized by a high presence of zero-sequence harmonics (especially the third harmonic and its odd multiples, known as triplen harmonics).

Historically, neutral conductors and grounding busbars were sized under the premise of balanced systems, where the neutral current was negligible or limited to fundamental unbalance currents (50 Hz or 60 Hz). In such scenarios, a neutral conductor with a cross-sectional area of 50% of the phase conductor was a common and normatively accepted practice. However, in modern installations with a massive presence of SMPS, the current in the neutral conductor can far exceed the steady-state phase current, reaching theoretical values of up to 173% ($\sqrt{3}$) of the phase current under extreme distortion conditions, and even higher if fundamental load unbalances are superimposed. This anomalous thermal and dynamic behavior demands a rigorous and mathematical rethinking of the sizing of neutral and ground busbars in main distribution boards (MDBs) and sub-distribution boards.

The purpose of this technical paper is to provide an exhaustive analysis, from the physical fundamentals of electromagnetism to advanced calculation methodologies and simulation, for the correct sizing of neutral and ground busbars. The thermal effects derived from the skin and proximity effects in flat busbars under multi-frequency excitation, the electrodynamic stresses under short-circuit currents with high harmonic content, and the high-frequency leakage currents that saturate grounding systems will be examined. Finally, the use of the Vexten Suite engineering software will be integrated as the reference tool for short-circuit analysis, cable sizing, and resonance mitigation in high-tech density industrial and commercial environments.

Phenomenology of Zero-Sequence Harmonics in Three-Phase Systems

Behavior of Switched-Mode Power Supplies (SMPS)

Single-phase switched-mode power supplies typically utilize a full-wave bridge rectifier followed by a capacitive filter to obtain a stable direct current (DC) bus. The input current to this circuit is non-sinusoidal; the rectifier only conducts when the instantaneous alternating current (AC) line voltage exceeds the voltage stored in the filtering capacitor. This results in narrow current pulses with a high crest factor (the ratio of peak value to root-mean-square [RMS] value, which can range between 2.5 and 4, compared to the 1.414 value of a pure sine wave).

Fourier analysis of this current waveform reveals an extremely rich harmonic content. Odd-order harmonics that are not multiples of three (5th, 7th, 11th, 13th, etc.) correspond to positive and negative sequences, which partially cancel out at the neutral node of a balanced three-phase system. However, odd multiples of the third harmonic (3rd, 9th, 15th, 21st, etc.), termed triplen harmonics, possess a critical mathematical property: their phase components are in phase with each other (zero sequence or homopolar sequence). This means that, instead of canceling out at the star (wye) point of the three-phase system, they add up arithmetically in the neutral conductor.

Vector and Arithmetic Summation in the Neutral Conductor

To understand the accumulation of currents in the neutral, let us consider a balanced three-phase system with phase currents of the following form:

Where $I_h$ is the root-mean-square (RMS) value of the harmonic current of order $h$, and $\theta_h$ is the corresponding phase angle. The current in the neutral conductor $i_N(t)$ is the instantaneous sum of the three phase currents:

If we analyze the spatial phase shift of the individual harmonic components in the summation, we find that for any harmonic $h$:

When $h$ is a multiple of 3 (that is, $h = 3k$ for $k \in \mathbb{N}$), the angular phase shift becomes an integer multiple of $2\pi$:

Therefore, the trigonometric functions for the three phases become identical and in phase:

Substituting this into the neutral equation, we obtain that the zero-sequence currents sum directly arithmetically in the neutral, while the positive and negative sequence currents cancel out (assuming perfect balance of phase amplitudes):

The resulting root-mean-square (RMS) value of the neutral current is:

If the fundamental phase current is $I_1$ and the individual harmonic distortion rate of the third harmonic is, for example, 60% ($I_3 = 0.6 \cdot I_1$), and we neglect other higher harmonics, the current in the neutral will be:

This result mathematically demonstrates that the neutral current can exceed 180% of the nominal phase current, generating a thermal current density that is unacceptable for conventional, non-oversized neutral busbars.

Skin Effect and Proximity Effect at High Frequencies

The sizing of copper or aluminum busbars cannot be based solely on the total RMS current calculated by summing harmonics, due to the increase in the effective resistance of the conductor with frequency. This increase is governed by two electromagnetic phenomena ruled by Maxwell's equations: the skin effect and the proximity effect.

The skin effect describes the tendency of alternating current to distribute non-uniformly within a conductor, concentrating near the outer surface. The skin depth ($\delta$), or skin thickness, is mathematically defined as:

Where:

• $\rho$ is the electrical resistivity of the conductor material ($\Omega \cdot m$).
• $f$ is the frequency of the harmonic component ($Hz$).
• $\mu$ is the absolute magnetic permeability of the material (H/m ")), which for copper and aluminum is approximately equal to the permeability of free space \mu_0 = 4\pi \times 10^{-7} \ H/m.

As the frequency of the harmonics increases (for example, the 9th harmonic in a 60 Hz system corresponds to 540 Hz), the skin depth $\delta$ decreases substantially. For commercial electrolytic copper (E-Cu) at 20 °C ($\rho \approx 1.72 \times 10^{-8} \ \Omega \cdot m$), the values of $\delta$ are:

• Fundamental Frequency (60 Hz): $\delta \approx 8.5 \ mm$
• Third Harmonic (180 Hz): $\delta \approx 4.9 \ mm$
• Ninth Harmonic (540 Hz): $\delta \approx 2.8 \ mm$

If the physical thickness of the neutral busbar is greater than $2\delta$, the interior of the conductor carries almost no current, which reduces the effective conduction area and drastically raises the alternating current resistance ($Rac$) for that specific harmonic. The busbar resistance for each harmonic of order $h$ is modeled by:

Where $y_s(h)$ is the skin effect factor for harmonic $h$, and $y_p(h)$ is the proximity effect factor, which arises from the interaction of magnetic fields generated by adjacent conductors (phase and ground busbars within the same switchboard), further distorting the current distribution. For rectangular cross-section busbars, these factors present high analytical complexity and are typically resolved using numerical methods or normative approximations such as those established in the IEC 60287 standard.

Forensic Analysis of Failures in Electrical Infrastructure

Thermal Degradation in Distribution Transformers and K-Factor

When neutral and ground busbars in distribution boards are subjected to severe harmonic currents without proper sizing, the thermal and inductive feedback effects propagate upstream to the distribution transformers (typically with Delta-Wye connection). Zero-sequence currents (triplen harmonics) circulate through the neutral of the transformer secondary and are reflected as circulating currents within the primary delta winding. This does not cause triplen harmonic currents in the primary supply lines, but it causes severe internal heating in the transformer windings due to eddy current losses ($PEC$) and stray magnetic losses ($POSL$).

Eddy current losses in the windings increase proportionally to the square of the current and the square of the frequency:

Where $P_{EC-R}$ represents the eddy current losses at fundamental frequency and rated current. To prevent accelerated thermal degradation of the transformer insulation (thermal class of insulating papers such as Nomex or Kraft), the K-Factor derating must be applied, as defined by the IEEE C57.110 standard:

A standard transformer not designed for harmonic loads (K-1) operating with a switched-mode power supply load with a real K-Factor of 13 or 20 will experience premature thermal aging of the insulation, reducing its service life from 30 years to less than 5 years, or causing a catastrophic failure due to inter-turn short circuits resulting from the carbonization of the insulating paper.

Core Saturation and Nuisance Tripping of Protections

The presence of high levels of triplen harmonics alters the magnetic flux density ($B$) in the cores of transformers and current transformers (CTs) associated with protection relays. The neutral current, having high-frequency components, induces spurious voltages in control and communication circuits due to mutual inductive coupling. Furthermore, thermomagnetic protections and molded case circuit breakers (MCCBs) that do not use True RMS sensing trip units will fail in their operational diagnosis:

• Nuisance tripping (false positives): Circuit breakers with peak-sensing or average-sensing units calibrated for sine waves will interpret the high crest factors of the phase and neutral currents as overcurrent or short-circuit conditions, opening the circuit unjustifiably.
• Failure to trip under real overloads (false negatives): If the circuit breaker measures only the average value of the current, it will drastically underestimate the true RMS value of a highly distorted wave, allowing neutral busbars and cables to operate at temperatures far exceeding their thermal design limits (for example, exceeding 90 °C in XLPE-insulated cables or 105 °C in copper busbars supported by epoxy insulators), triggering fires in electrical panels.

Ground Leakage Currents from EMI Filters and Ground Potential Rise (GPR)

Switched-Mode Power Supplies (SMPS) incorporate electromagnetic interference (EMI) filters in their input stage to comply with electromagnetic compatibility (EMC) regulations, such as CISPR 22 or FCC Part 15. These filters employ common-mode suppression capacitors (Y-capacitors) connected directly between the active conductors (phase/neutral) and the protective earth (PE) grounding conductor.

Under the presence of high-frequency harmonic voltages on the line, the impedance of these capacitors ($X_C = 1 / (2\pi f C_Y)$) decreases proportionally to the frequency. This causes significant high-frequency leakage currents to flow continuously to the ground busbar of the panel and, through it, to the grounding electrode system (GES). In facilities with thousands of computers or servers (data centers), these individual leakage currents of 0.5 mA to 3.5 mA per equipment accumulate, reaching tens of amperes of permanent leakage current in the ground busbar.

This permanent current in the grounding system has critical consequences:

• Ground Potential Rise (GPR): The ground busbar acquires a voltage potential other than absolute zero volts with respect to remote physical earth, due to the impedance voltage drop ($VGPR = Ifuga \cdot Ztierra$). This generates common-mode noise that corrupts high-speed data communication signals (Ethernet, RS-485, optical fiber with metallic transceivers) and can cause minor but dangerous electrical shocks to personnel handling the metallic chassis of the equipment.
• Saturation and tripping of residual current devices (RCDs): Conventional Class AC or Class A residual current devices experience erratic tripping due to high-frequency leakage currents and DC components that magnetically saturate their sensing toroids. The implementation of advanced Class B or Class F RCDs, specifically designed to handle multi-frequency leakage currents and smooth DC components, is required.

Mathematical Modeling and Formulation for Busbar Sizing

Calculation of the Root-Mean-Square (RMS) Current in the Neutral

To safely size a neutral busbar, the design engineer must determine the total expected RMS current, considering both fundamental load unbalance and total harmonic content. The generalized equation for the neutral RMS current ($I_{N,rms}$) in a three-phase, four-wire system with arbitrary and distorted phase currents is expressed as:

Where the fundamental component of the neutral ($I_{N,1}$) is obtained by phasor analysis of the fundamental phase currents ($I_{a,1}, I_{b,1}, I_{c,1}$) and their respective unbalance angles:

For harmonic components of order $h$, the current in the neutral is calculated according to its phase sequence:

• For positive-sequence harmonics ($h = 1, 4, 7, 10, \dots$) and negative-sequence harmonics ($h = 2, 5, 8, 11, \dots$), the currents partially cancel out if the phase amplitudes are balanced.
• For zero-sequence harmonics ($h = 3, 6, 9, 12, 15, \dots$), the phase currents sum vectorially in a direct manner. If the phases are balanced in amplitude for each zero-sequence harmonic, the harmonic current in the neutral is exactly three times the phase harmonic current:

Alternating Current Resistance and Joule Heating Losses

Thermal dissipation in the neutral busbar due to the Joule effect is the primary physical limitation for its sizing. The total power losses per unit length ($Ploss$, in $W/m$) in a conducting busbar carrying a current with a harmonic spectrum are calculated by summing the losses generated by each individual frequency component:

Where $Rac(h)$ is the resistance of the busbar at the frequency of harmonic $h$. For a rectangular conducting busbar of width $w$ and thickness $t$ (where $w \ge t$), the direct current resistance per unit length is:

The alternating current resistance for the harmonic of order $h$ is approximated using the skin effect correction factor $k_s(h)$:

For rectangular profiles, the factor $k_s(h)$ is evaluated as a function of a dimensionless parameter $x_s(h)$ defined as:

Where $f_1$ is the fundamental frequency and $k_p$ is a geometric shape factor of the busbar. If $x_s(h) \le 2.8$, the resistance factor is calculated as:

If $x_s(h) > 2.8$, the asymptotic approximation is used:

This increase in resistance with frequency implies that the neutral busbar will generate significantly more heat for the same RMS current value if this current is composed of high-frequency harmonics rather than a pure 50/60 Hz sinusoidal current. The steady-state thermal balance to determine the operating temperature of the busbar ($T_s$) with respect to the ambient temperature ($T_a$) is governed by the heat transfer equation:

Where the losses due to convection ($qconv$) and radiation ($qrad$) are expressed as:

Where:

• $h_c$ is the convective heat transfer coefficient ($W/m ^2\cdot^\circ C$), which depends on the orientation of the busbar (horizontal or vertical).
• $A_s$ is the exposed surface area per unit length ($m ^2/ m$).
• $\epsilon$ is the emissivity of the busbar surface (for example, $\epsilon \approx 0.15$ for bright copper and $\epsilon \approx 0.85$ for painted or oxidized copper).
• $\sigma$ is the Stefan-Boltzmann constant ($5.67 \times 10^{-8} \ W/m ^2\cdot K ^4$).

Electrodynamic Stresses under Short-Circuit Conditions

The physical sizing of neutral and ground busbars must not only respond to steady-state thermal criteria, but also to the capacity to withstand destructive mechanical stresses of electrodynamic origin during a phase-to-neutral or phase-to-ground short-circuit event. The instantaneous electromagnetic force per unit length ($F(t)$) acting on parallel busbars separated by a center-to-center distance $d$ is calculated using Laplace's force law:

Under asymmetrical fault conditions, the short-circuit current exhibits a transient unidirectional direct current component (DC offset) that raises the peak value of the current to the peak short-circuit current ($i_p$), calculated according to IEC 60909 as:

Where $I''_{k}$ is the initial symmetrical short-circuit RMS current and $\kappa$ is the peak factor depending on the reactance-to-resistance ratio ($X/R$) of the fault loop:

The maximum mechanical force per unit length ($F_m$) acting on the busbar support insulators during the first half-cycle of the fault is:

Where $\beta$ is a geometric correction factor that considers the rectangular shape of the busbars and their spatial arrangement (flat-to-flat or edge-to-edge profiles). The neutral busbar must be mechanically designed so that the resulting maximum bending stress ($\sigma_m$) does not exceed the yield strength of the conducting material (R_{p0.2}")), which for annealed copper is approximately 250 MPa and for aluminum alloy 6101-T6 is 170 MPa: σm=MmaxW≤Rp0.2\sigma_m = \frac{Mmax}{W} \le R_{p0.2}σm​=WMmax​≤Rp0.2​ Where Mmax is the maximum bending moment on the busbar (which depends on the distance between support insulators $L$) and $W$ is the section modulus of the rectangular busbar ($W = w \cdot t^2 / 6$ for bending about the weak axis, or $W = t \cdot w^2 / 6$ for bending about the strong axis).

Normative Standards and Comparative Design Criteria

Comparative Table of Design Parameters and Regulatory Limits

The design of distribution systems with high harmonic density is strictly regulated by international standards. Below is a detailed comparative analysis of the mechanical, electrical, and thermal design parameters under the most relevant standards.

Technical Parameter / Criterion	IEC 60364-5-52 / IEC 61439-1 Standard	NEC (NFPA 70) Art. 310 / 250 Standard	IEEE 519 / IEEE 141 Standard	Operational Consequences and Dielectric Instability
Neutral Current Capacity	Allows reduction to 50% of phase only if there are no harmonics. Requires 100% if THDi > 15% and 200% (or a derating factor of 0.84) if THDi > 33%.	Section 310.15(C)(1) requires the neutral to be considered a current-carrying conductor if it carries harmonics. Section reduction is not permitted.	Recomends sizing the neutral to 200% in circuits supplying IT loads with THDi > 50%.	Undersizing causes cumulative overheating, premature aging of adjacent cable insulation, and an imminent risk of fire in distribution boards.
Busbar Operating Temperature	IEC 61439-1 limits the temperature rise of bare busbars to 65 °C above an ambient temperature of 35 °C (absolute maximum of 100 °C).	Thermal limit based on the rating of the support insulator (typically 90 °C or 105 °C according to UL 891).	Aligns with connection equipment temperature limits to prevent terminal degradation.	Temperatures above 105 °C accelerate copper oxidation, increasing contact resistance at joints and causing arc flash failures.
Short-Circuit Mechanical Stress	IEC 61439-1 requires validation through type tests or calculation according to IEC 60865-1 for attraction/repulsion forces.	Compliance with UL 891 for short-circuit current resistance (Withstand Rating) expressed in symmetrical kA.	IEEE 141 provides methodologies for calculating short-circuit forces on busbars and rigid supports.	Excessive electrodynamic forces plastically deform busbars, rupture epoxy insulators, and cause catastrophic three-phase short circuits.
Grounding Resistance	IEC 60364-4-41 prioritizes low fault loop impedance (Z_s) to ensure rapid disconnection of protection devices.	Art. 250.56 requires a ground electrode resistance of 25 $\Omega$ or less. Recommends < 5 $\Omega$ for industrial systems.	IEEE 142 (Green Book) recommends a grounding resistance of less than 1 $\Omega$ for data centers and sensitive electronics.	High ground impedance prevents the operation of overcurrent protections during ground faults, keeping chassis energized with dangerous voltages.
Voltage Harmonic Distortion Limits (THDv)	IEC 61000-2-4 defines electromagnetic compatibility limits in industrial environments (Class 2: THDv < 8%).	Not directly regulated by the NEC, but indirectly referenced for distribution service quality.	Table 1 of IEEE 519 limits the total voltage harmonic distortion (THDv) to a maximum of 8% for systems < 1 kV, and 5% for the general busbar.	Elevated THDv levels cause an increase in hysteresis and eddy current losses in motors and transformers across the entire grid.

Practical Sizing Methodologies and Mitigation

Oversizing the Neutral to Two Hundred Percent

In distribution boards where the dominant load consists of servers, switched-mode power supplies, and electronic ballasts, state-of-the-art engineering practice demands the use of neutral busbars oversized to 200% of the current capacity of the phase busbars. Physically, this is achieved by doubling the thickness of the neutral busbar or by using two identical busbars in parallel, properly spaced to allow cooling air circulation and mitigate the proximity effect.

By doubling the cross-sectional area of the busbar, the direct current resistance is halved ($R_{dc, 200\%} = 0.5 \cdot R_{dc, 100\%}$). Although the skin effect continues to act on high harmonic frequencies, the reduction in base resistance ensures that total Joule losses remain within the safe thermal dissipation limits of the enclosure, preventing thermal accumulation inside the metallic housing.

Grounding Configurations for High Frequency

Traditional grounding systems designed for safety at power frequency (50/60 Hz) consist of vertical electrodes (ground rods) and large cross-section interconnecting conductors. However, at the switching frequencies of SMPS and electromagnetic transients (ranging from tens of kilohertz to megahertz), the inductance of the grounding conductor completely dominates over its ohmic resistance:

The inductance of a straight conductor of length $l$ and diameter $d$ is approximated by:

For a grounding cable with a cross-section of 50 mm² and a length of 10 meters, the inductance is approximately 15 $\mu H$. At 60 Hz, the inductive reactance is a mere 0.0056 $\Omega$. However, for a high-frequency transient or a high-frequency switching harmonic of 100 kHz, the reactance rises to:

This high impedance prevents high-frequency noise currents from flowing effectively to physical earth, forcing them to seek alternative paths through the chassis of control and data equipment, causing communication failures and hardware damage. To mitigate this phenomenon, the following high-frequency grounding configurations must be employed:

• High-Frequency Coupling Network (Signal Reference Grid - SRG): Implementation of a grid of flat copper conductors or thin copper straps interconnected at all crossover points, installed beneath the raised floor of data centers. Copper straps present a much larger perimeter surface than round conductors, drastically reducing skin effect resistance and high-frequency inductance.
• Low-Inductance Grounding Conductors: Use of flat braided copper straps instead of round cables to connect cabinets to the main ground busbar, minimizing high-frequency coupling impedance.

Active Harmonic Filters and Isolation Transformers with Zig-Zag Connection

When busbar oversizing is unfeasible due to space or weight constraints in existing panels, active and passive mitigation solutions must be deployed at the point of common coupling (PCC):

• Active Harmonic Filters (AHF): High-speed power electronics-based devices that continuously monitor the load current and generate a phase-opposed harmonic current (180° out of phase) in real time. This dynamically cancels the harmonic currents generated by non-linear loads, reducing the THDi at the installation point to values below 3% or 5%. Modern 4-wire active filters have the capability to inject compensation current directly into the neutral, completely eliminating triplen harmonic currents in the neutral upstream of the filter.
• Isolation Transformers with Zig-Zag Connection (Interconnected Star): The zig-zag winding presents an extremely low impedance to zero-sequence currents and a standard impedance to positive and negative sequence currents. By installing a zig-zag transformer in parallel near non-linear loads, it acts as a low-impedance sink for triplen harmonics, trapping local third-harmonic currents and preventing them from returning through the main feeder neutral to the main distribution board or the primary distribution transformer.

Advanced Simulation and Validation via Vexten Suite

Modern power system design with high harmonic penetration requires high-fidelity computational simulation tools that integrate cutting-edge numerical algorithms to validate thermal, electromechanical, and grid impedance calculations. The Vexten Suite platform stands as the industry standard for this purpose, offering specialized modules for multi-physics analysis and harmonic power flow.

Short-Circuit Calculation according to IEC 60909 and IEEE 141

The short-circuit calculation module of Vexten Suite allows precise modeling of the zero-sequence impedance ($Z_0$) of the entire system, including the geometry of the neutral and ground busbars in the panels. The computational calculation engine solves the phase impedance matrices using symmetrical components to determine single-phase asymmetrical short-circuit currents (phase-to-neutral and phase-to-ground):

Where:

• $c$ is the grid voltage factor according to IEC 60909.
• $V_n$ is the nominal line voltage.
• $Z_1, Z_2, Z_0$ are the positive, negative, and zero-sequence impedances of the fault network, respectively.

The software calculates the transient unidirectional component of the current and determines the maximum instantaneous electrodynamic stress on the neutral and ground busbars, allowing the designer to verify whether the selected support insulators and physical busbar spacing will withstand the mechanical bending and shear stresses without structural failure.

Thermal Sizing of Conductors under IEC 60287 / NEC 310

The cable sizing and ampacity analysis module of Vexten Suite incorporates the complex equations of the IEC 60287 standard for calculating steady-state multi-frequency thermal losses. The engineer inputs the measured or projected harmonic spectrum of the load (RMS values of each harmonic up to the 50th order). The software performs an iterative analysis to determine the harmonic derating factor of the neutral and phase conductors, calculating the temperature rise in the conducting core and on the outer surface of the raceway or cable tray.

Through this analysis, Vexten Suite automatically determines whether the selected neutral conductor cross-section complies with the maximum insulation temperature limits (e.g., 90 °C for XLPE/EPR), optimizing the cross-sectional area selection and preventing both catastrophic undersizing and economically inefficient oversizing.

Resonance Mitigation and Power Factor

One of the most critical risks when attempting to correct the power factor in networks with a high presence of harmonics is harmonic resonance. If conventional capacitor banks without detuning reactors (un-tuned banks) are installed, the capacitive reactance of the bank ($X_C$) will decrease with frequency, while the inductive reactance of the upstream transformer ($X_L$) will increase. At a specific frequency, both reactances will equalize, creating a parallel resonant circuit:

Where:

• $f_r$ is the parallel resonance frequency.
• $Ssc$ is the short-circuit power at the connection point of the capacitor bank ($MVA$).
• $Q_C$ is the reactive power of the capacitor bank ($Mvar$).

If the resonance frequency $f_r$ coincides with one of the harmonics generated by the switched-mode power supplies (for example, the 3rd or 5th harmonic), harmonic current and voltage amplification of destructive proportions will occur. This will cause immediate failure of the capacitors due to thermal overvoltage, breaker tripping, and intolerable levels of voltage distortion across the entire system.

The power quality analysis module of Vexten Suite allows simulating the grid impedance sweep (Impedance Scan) over a wide frequency range. The software visually identifies parallel and series resonance points and assists the engineer in designing detuned capacitor banks (detuned filter banks) through the precise selection of the detuning factor $p$ (typically 5.67%, 7%, or 14%), ensuring that the system's resonance frequency is safely shifted below the first dominant harmonic (for example, tuning the filter to 189 Hz for a 50 Hz grid with 5th harmonic issues):

The integration of Vexten Suite into the electrical engineering design workflow ensures that distribution boards, neutral and ground busbars, and associated mitigation systems operate with the highest level of reliability, safety, and operational efficiency under the most demanding load conditions of the digital age.